[go: up one dir, main page]

 
 

Topic Editors

School of Resources and Safety Engineering, Central South University, Changsha 410083, China
Hunan Provincial Key Laboratory of Safe Mining Techniques of Coal Mines, Hunan University of Science and Technology, Xiangtan 411201, China
School of Civil Engineering, Hefei University of Technology, Hefei 230009, China
School of Civil Engineering, Sun Yat-sen University, Zhuhai 519082, China
School of Resources and Safety Engineering, Central South University, Changsha 410083, China

New Trends in Rock Materials Mechanics and Engineering Geology

Abstract submission deadline
closed (20 March 2024)
Manuscript submission deadline
closed (20 May 2024)
Viewed by
95884

Topic Information

Dear Colleagues,

Rock mechanics is a complicated science compared with solid mechanics, fluid mechanics, and physics. The research object of rock mechanics is various types of rock mass engineering, whose rock mass material properties are affected by a series of defects (fissures, cracks, pores, voids, faults, etc.). The scale region of these defects is above the mesoscopic and microscopic scales, and below the macroscopic scale, where it is difficult to find statistical laws. Therefore, it is difficult to determine the reasonable statistical scale of volume units when constructing the theoretical system of mechanics.

As an independent applied basic discipline, rock mechanics has the following basic elements: independent research object, independent service field, independent testing machine and method, independent constitutive or physical law, and independent theoretical system. Research from the direction of these elements has guided the science and engineering technology of various rock mass problems in the past, and future advances will still revolve around them.

Hence, the aim of this Special Issue is to publish original research and review articles on new trends in these directions including test instruments and methods, mechanical properties of rock and rock mass, the theoretical analysis of mechanics, numerical simulation and intelligent algorithms, engineering rock mass techniques, and prediction and prevention techniques for rock mass disaster.

Prof. Dr. Hang Lin
Prof. Dr. Yanlin Zhao
Prof. Dr. YiXian Wang
Dr. Yu Chen
Dr. Rihong Cao
Topic Editors

Keywords

  • test instruments and methods
  • mechanical properties of rock and rock mass
  • theoretical analysis of mechanics
  • numerical simulation and intelligent algorithms
  • engineering rock mass techniques
  • prediction and prevention techniques for rock mass disaster

Participating Journals

Journal Name Impact Factor CiteScore Launched Year First Decision (median) APC
Applied Sciences
applsci
2.5 5.3 2011 17.8 Days CHF 2400
Minerals
minerals
2.2 4.1 2011 18 Days CHF 2400
Materials
materials
3.1 5.8 2008 15.5 Days CHF 2600
Energies
energies
3.0 6.2 2008 17.5 Days CHF 2600
Buildings
buildings
3.1 3.4 2011 17.2 Days CHF 2600

Preprints.org is a multidiscipline platform providing preprint service that is dedicated to sharing your research from the start and empowering your research journey.

MDPI Topics is cooperating with Preprints.org and has built a direct connection between MDPI journals and Preprints.org. Authors are encouraged to enjoy the benefits by posting a preprint at Preprints.org prior to publication:

  1. Immediately share your ideas ahead of publication and establish your research priority;
  2. Protect your idea from being stolen with this time-stamped preprint article;
  3. Enhance the exposure and impact of your research;
  4. Receive feedback from your peers in advance;
  5. Have it indexed in Web of Science (Preprint Citation Index), Google Scholar, Crossref, SHARE, PrePubMed, Scilit and Europe PMC.

Published Papers (51 papers)

Order results
Result details
Journals
Select all
Export citation of selected articles as:
18 pages, 5562 KiB  
Article
The Laser Scanner Technique: A Tool for Determining Shear Strength Parameters of Rock Mass Discontinuities
by Margherita Zimbardo, Alessandra Nocilla and Anna Scotto di Santolo
Appl. Sci. 2024, 14(13), 5793; https://doi.org/10.3390/app14135793 - 2 Jul 2024
Viewed by 716
Abstract
When evaluating the shear strength of rock mass discontinuities, certain challenges arise due to the difficulty in quantifying the roughness characteristics of surfaces and the strength of asperities. Recent research has focused on enhancing techniques for assessing these characteristics and exploring the application [...] Read more.
When evaluating the shear strength of rock mass discontinuities, certain challenges arise due to the difficulty in quantifying the roughness characteristics of surfaces and the strength of asperities. Recent research has focused on enhancing techniques for assessing these characteristics and exploring the application of laser scanning to aid in evaluating discontinuity features. The analysis of reflectivity values (I) obtained through a laser scanner survey presents an efficient method for assessing mechanical characteristics, such as joint compressive strength (JCS). Reflectivity measurements demonstrate correlations with Schmidt hammer rebound values (r). The laser scanner technique would enable the measurement of JCS without the direct application of the Schmidt hammer on rocks in areas where rebound values (r) measurements are unavailable. The use of a laser scanner allows for the acquisition of high-precision geometrical information concerning the 3D roughness and anisotropy of rock surfaces. In this study, an innovative technique was introduced that utilizes laser scanner data from six previous experimental surveys conducted on rock formations in Southern Italy. This technique facilitates the evaluation of roughness profiles, considering potential variations along kinematically admissible sliding directions, allowing for the estimation of the Joint Roughness Coefficient (JRC). This new methodology aids in evaluating the parameters of Barton’s equation to determine the strength characteristics of rock mass discontinuities. Full article
Show Figures

Figure 1

Figure 1
<p>Schmidt hammertest JCS estimation chart showing correlation between Schmidt hammer rebound number, hammer orientation, UCS, and rock density [<a href="#B52-applsci-14-05793" class="html-bibr">52</a>].</p>
Full article ">Figure 2
<p>Monte Pellegrino: portions of the wall characterized by different degrees of alteration. Schmidt hammer estimations (<span class="html-italic">r<sub>m</sub></span>) and reflectivity measured by the laser scanner (<span class="html-italic">I<sub>m</sub></span>): (<b>a</b>) smooth surfaces (<b>b</b>) altered but smooth surfaces with a uniform texture (<b>c</b>) intact and slightly altered rock.</p>
Full article ">Figure 3
<p>Monte Catalfano: points cloud of rock mass collected using a laser scanner. Highlighting the seventy discontinuities from which the sections have been extracted.</p>
Full article ">Figure 4
<p>Monte Catalfano: Discontinuity 1–7 on the mesh in layer format reflectivity.</p>
Full article ">Figure 5
<p>Photo of the seven discontinuities chosen for the assessment of rebound and reflectivity values. Discontinuity 1–7 of the <a href="#applsci-14-05793-f004" class="html-fig">Figure 4</a>. The arrow indicates the portion of discontinuity investigated.</p>
Full article ">Figure 6
<p>Castronovo di Sicilia. Chosen zones within the quarry area.</p>
Full article ">Figure 7
<p>Latomiae del Paradiso (Syracuse). Photo of the investigated area.</p>
Full article ">Figure 8
<p>Palazzo Jung (Palermo). Altered column (on the right) and intact column (on the left).</p>
Full article ">Figure 9
<p>Relationships between reflectivity (I) and rebound (r) for the six surveys.</p>
Full article ">Figure 10
<p>Influence of the decay of the texture on the reflectivity index (I) and the rebound values (r).</p>
Full article ">Figure 11
<p>(<b>a</b>) Measurement of joint roughness amplitude, (<b>b</b>) diagram [<a href="#B29-applsci-14-05793" class="html-bibr">29</a>], and (<b>c</b>) example of measurement on a discontinuity in Monte Catalfano.</p>
Full article ">Figure 12
<p>Bundle of planes with axis orthogonal to the discontinuity.</p>
Full article ">Figure 13
<p>Inclination of asperity (<span class="html-italic">i°</span>)—base amplitudes (a): values measured on roughness profiles.</p>
Full article ">
22 pages, 6434 KiB  
Article
Experimental Study on the Effect of Cyclic Heating and Water Cooling on Mixed-Mode I-II Fracture Characteristics of Sandstone
by Wenyu Zhang, Wen Hua, Mao Zhou, Fengfei He, Yaozhong Xu, Yunru Wang, Shiming Dong and Jialin Kuang
Buildings 2024, 14(7), 1903; https://doi.org/10.3390/buildings14071903 - 21 Jun 2024
Viewed by 573
Abstract
In the process of underground resource extraction, deep rock masses are often subjected to cyclic-heating and water-cooling effects, which cause significant damage to the mechanical properties of rocks. In order to study the degradation mechanism of sandstone under cyclic heating and water cooling, [...] Read more.
In the process of underground resource extraction, deep rock masses are often subjected to cyclic-heating and water-cooling effects, which cause significant damage to the mechanical properties of rocks. In order to study the degradation mechanism of sandstone under cyclic heating and water cooling, many fracture experiments have been carried out. The effect of cyclic heating and water cooling at 200 °C on the tensile strength and the mixed-mode I-II fracture toughness of sandstone was investigated. The similarities and differences in the rock fracture characteristics and deterioration response of tensile properties are also examined. Meanwhile, the correlation between the microstructure and macroscopic fracture mechanical properties was revealed by observing the evolutionary pattern of rock microstructure. The findings demonstrate that the heating and water-cooling-induced variations in the tensile strength and fracture toughness of rock exhibit a consistent trend. The effective fracture toughness of sandstone decreases exponentially with increasing cycle times. The impact of the heating and water-cooling cycles on the fracture toughness of pure mode I is found to be more pronounced compared to that observed in mixed modes and pure mode II specimens. The failure mode of the rock sample undergoes a transition from abrupt to gradual, accompanied by an augmented development of cracks on the failure surface and finer fragmentation of rock debris. The results of this study can provide theoretical references for engineering practices such as the exploitation of geothermal resources and hydraulic fracturing. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of the CSTBD specimen.</p>
Full article ">Figure 2
<p>Microstructures of the sandstone.</p>
Full article ">Figure 3
<p>Preparation of CSTBD and BD specimens.</p>
Full article ">Figure 4
<p>Prepared samples of sandstone and experimental instruments.</p>
Full article ">Figure 5
<p>Typical loading diagram of the CSTBD specimens.</p>
Full article ">Figure 6
<p>Typical load–displacement curves of the CSTBD samples.</p>
Full article ">Figure 7
<p>Mean peak load of the tested sandstone.</p>
Full article ">Figure 8
<p>Averaged values of mode I and mode II fracture toughness.</p>
Full article ">Figure 9
<p>Degradation degree of the tested sandstone samples.</p>
Full article ">Figure 10
<p>Averaged effective fracture toughness: (<b>a</b>) variation in the <span class="html-italic">K</span><sub>eff</sub> with <span class="html-italic">N</span> and (<b>b</b>) variation in the <span class="html-italic">K</span><sub>eff</sub> with <span class="html-italic">β</span>.</p>
Full article ">Figure 11
<p>Deterioration degree of <span class="html-italic">K</span><sub>eff</sub> under mixed mode I-II loading.</p>
Full article ">Figure 12
<p>Load–displacement curves of BD specimens.</p>
Full article ">Figure 13
<p>Test results of tensile strength.</p>
Full article ">Figure 14
<p>Fracture pattern diagram of sandstone.</p>
Full article ">Figure 15
<p>Relation between <span class="html-italic">K</span><sub>IC</sub>, <span class="html-italic">K</span><sub>IIC</sub>, and <span class="html-italic">σ</span><sub>t</sub> of sandstone: (<b>a</b>) <span class="html-italic">K</span><sub>IC</sub> and <span class="html-italic">σ</span><sub>t</sub>; (<b>b</b>) <span class="html-italic">K</span><sub>IIC</sub> and <span class="html-italic">σ</span><sub>t</sub>.</p>
Full article ">Figure 16
<p>Relation between <span class="html-italic">K</span><sub>IIC</sub> and <span class="html-italic">K</span><sub>IC</sub> of sandstone.</p>
Full article ">Figure 17
<p>SEM images of tested sandstone specimens: (<b>a</b>) N = 0, (<b>b</b>) N = 6, (<b>c</b>) N = 12.</p>
Full article ">
16 pages, 3154 KiB  
Article
Numerical Simulation Analysis of Control Factors on Acoustic Velocity in Carbonate Reservoirs
by Jiahuan He, Wei Zhang, Dan Zhao, Nong Li, Qiang Kang, Kunpeng Cai, Li Wang, Xin Yao, Guanqun Wang, Bi’an Dong, Wei Li, Hongbin Chen and Wei Long
Minerals 2024, 14(4), 421; https://doi.org/10.3390/min14040421 - 19 Apr 2024
Viewed by 835
Abstract
The conventional Archie formula struggles with the interpretation of water saturation from resistivity well log data due to the increasing complexity of exploration targets. This challenge has prompted researchers to explore alternative physical parameters, such as acoustic characteristics, for breakthroughs. Clarifying the influencing [...] Read more.
The conventional Archie formula struggles with the interpretation of water saturation from resistivity well log data due to the increasing complexity of exploration targets. This challenge has prompted researchers to explore alternative physical parameters, such as acoustic characteristics, for breakthroughs. Clarifying the influencing factors of porous media acoustic characteristics is one of the most important approaches to help understanding the mechanism of acoustic characteristics of carbonate reservoirs. The article uses digital rock technology to characterize the pore structure, quantitatively identify fractures and pore structures in carbonate rocks, and establish digital models. Through conventional acoustic testing, the pressure wave (P-wave) and shear wave (S-wave) velocities of rock samples at different water saturations are obtained, and the dynamic elastic modulus is calculated. A finite element calculation model is established using the digital rock computational model to provide a basis for fluid saturation calculation methods. Based on real digital rock models, different combinations of virtual fractures are constructed, and factors affecting acoustic parameters are analyzed. The study finds that as porosity increases, the velocity difference between porous cores and fractured cores also increases. These findings provide important technical support and a theoretical basis for interpreting acoustic well logging data and evaluating carbonate reservoirs with different pore and fracture types. Full article
Show Figures

Figure 1

Figure 1
<p>Representative carbonate samples and corresponding identification numbers: (<b>a</b>) vuggy-fractured type, sample number: 201402320031; (<b>b</b>) vuggy-filled-fractured type, sample number: 202103150006; (<b>c</b>) matrix-porosity type, sample number: 201402320019.</p>
Full article ">Figure 2
<p>Statistical distribution of pore throat in representative carbonate samples: (<b>a</b>) vuggy-fractured type, sample number: 201402320031; (<b>b</b>) vuggy-filled-fractured type, sample number: 202103150006; (<b>c</b>) matrix-porosity type, sample number: 201402320019.</p>
Full article ">Figure 3
<p>T2 spectrum distribution of representative carbonate samples: (<b>a</b>) vuggy-fractured type, sample number: 201402320031; (<b>b</b>) vuggy-filled-fractured type, sample number: 202103150006; (<b>c</b>) matrix-porosity type, sample number: 201402320019.</p>
Full article ">Figure 4
<p>Detailed model of representative carbonate sample: (<b>a</b>) 3D grayscale data; (<b>b</b>) mineral skeleton and pore structure; (<b>c</b>) pore structure.</p>
Full article ">Figure 5
<p>Schematic representation of the equivalence between the pixelated digital rock computational model and the finite elements.</p>
Full article ">Figure 6
<p>Comparison between simulated and measured P-wave velocities.</p>
Full article ">Figure 7
<p>Comparison between simulated and measured P-wave/S-wave velocity ratio.</p>
Full article ">Figure 8
<p>Schematic diagram of virtual fracture construction.</p>
Full article ">Figure 9
<p>Bulk modulus of various virtual fracture network models.</p>
Full article ">Figure 10
<p>P-wave velocity of various virtual fracture network models.</p>
Full article ">
13 pages, 11755 KiB  
Article
The Difference in Shear Behavior and Strength between Loess and Paleosol and Their Prediction of Unsaturated Strength
by Pan Liu, Fuchu Dai, Zhiquan Huang and Jiaqi Wu
Appl. Sci. 2024, 14(8), 3301; https://doi.org/10.3390/app14083301 - 14 Apr 2024
Viewed by 551
Abstract
In recent decades, loess landslide events have attracted increasing attention in the South Jingyang tableland. To elucidate the mechanical mechanism of landslide initiation in the region, this work collected undisturbed loess and paleosol samples taking from the Q2 strata in the South [...] Read more.
In recent decades, loess landslide events have attracted increasing attention in the South Jingyang tableland. To elucidate the mechanical mechanism of landslide initiation in the region, this work collected undisturbed loess and paleosol samples taking from the Q2 strata in the South Jingyang tableland. A range of direct shear tests were carried out to explore the strength evolution law of shear zone soil subjected to a varying initial moisture content. In addition, soil water characteristic curves (SWCCs) were also charted and used for predicting the unsaturated shear strength. The findings show that the basic physical properties of the paleosol are different from those of loess due to their different pedogenic environments. The normal stress level and initial moisture content jointly determine whether the shear behavior is strain hardening or strain softening. The shear strength and strength parameters evidently diminish with an increasing initial moisture content, and cohesion contributes to the vast majority of strength attenuation. Paleosol samples possess higher values in shear strength and strength parameters than loess samples due to their stronger inter-particle cementation. The predictive formulas of unsaturated shear strength for undisturbed loess and paleosol are proposed, respectively, based on the Vanapalli model, and the calculated values of the strength prediction model are in perfect agreement with the experimental values. Full article
Show Figures

Figure 1

Figure 1
<p>The location and acquisition process of samples (modified according to [<a href="#B4-applsci-14-03301" class="html-bibr">4</a>,<a href="#B35-applsci-14-03301" class="html-bibr">35</a>,<a href="#B36-applsci-14-03301" class="html-bibr">36</a>]).</p>
Full article ">Figure 2
<p>Curves of shear stress versus shear displacement for loess samples.</p>
Full article ">Figure 3
<p>Curves of shear stress versus shear displacement for paleosol samples.</p>
Full article ">Figure 3 Cont.
<p>Curves of shear stress versus shear displacement for paleosol samples.</p>
Full article ">Figure 4
<p>Shear strength envelopes of samples with different initial moisture contents.</p>
Full article ">Figure 5
<p>Relationship between cohesion and initial moisture content.</p>
Full article ">Figure 6
<p>SWCCs of loess and paleosol samples (note that the <span class="html-italic">AEV</span> is the air entry value).</p>
Full article ">Figure 7
<p>Relationship between shear strength and matrix suction.</p>
Full article ">Figure 8
<p>Comparison of test and predictive shear strengths for unsaturated loess and paleosol (note that the subscripts L and S denote loess and paleosol, respectively).</p>
Full article ">
16 pages, 2545 KiB  
Article
Spatial Variations of Deformation along a Strike-Slip Fault: A Case Study of Xianshuihe Fault Zone, Southwest China
by Jinxuan Li, Songfeng Guo, Shengwen Qi, Qianhui Wei, Bowen Zheng, Yu Zou, Yongchao Li, Yaguo Zhang and Xiao Lu
Appl. Sci. 2024, 14(6), 2439; https://doi.org/10.3390/app14062439 - 14 Mar 2024
Viewed by 961
Abstract
The distribution of damage zones around a fault has long been regarded as a frontier and hot spot in the field of geoscience but is still not fully understood. In this study, we conducted field investigations and tests around the Xianshuihe fault zone [...] Read more.
The distribution of damage zones around a fault has long been regarded as a frontier and hot spot in the field of geoscience but is still not fully understood. In this study, we conducted field investigations and tests around the Xianshuihe fault zone (XSHF), a left-lateral strike-slip fault with a length of about 400 km located in the eastern margin of the Tibetan Plateau. The results reveal that the fracture frequency and rock strength parameters present a spatially asymmetric distribution along the fault and have a negative power-law correlation with the distance from the fault. The widths of the damage zones are approximately 20.8 km and 17.1 km in the southwest and northeast directions, respectively. Combined with the previous studies, we presented a negative power-law function to depict the correlation between slip displacement and the width of the damage zone and found that the growth rate of damage zone in faults with low displacement is greater than that in those with large displacement. The study demonstrates that the asymmetric distribution of the damage zone surrounding the XSHF is mainly due to the stress redistribution in different damage zones stemming from the left echelon and different activity rates of the blocks on both sides of the XSHF. Full article
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>). Topography and principal active faults of Qinghai–Tibet plateau and adjacent regions. White arrows indicate motions of India, central Tibet, northeastern most Tibet, and Sichuan relative to Siberia (modified after Tapponnier, et al., 2001 [<a href="#B37-applsci-14-02439" class="html-bibr">37</a>], based on the Geographic Coordinate System—GCS_WGS_1984, DEM (Digital Elevation Model) data from ASF Data Search (alaska.edu)); (<b>b</b>). Spatial distribution and seismic development of XSHF; historical earthquake data are from Wen et al., 2008 [<a href="#B39-applsci-14-02439" class="html-bibr">39</a>] and China Earthquake Network (<a href="http://www.ceic.ac.cn" target="_blank">http://www.ceic.ac.cn</a>). (XSHF—Xianshuihe fault zone, GZ-YSF—Ganzi–Yushu fault zone, XJF—Xiaojiang fault zone, ANHF—Anninghe fault zone, DLSF—Daliangshan fault zone, LTF—Litang fault zone, LRBF—Longriba fault zone, MEKF—Maerkang fault, YLXF—Yulongxi fault zone, LMSF—Longmenshan fault zone; LHS—Luhuo segment, DFS—Daofu segment, QNS—Qianning segment, KDS—Selaha–Kangding segment, YLS—Yalahe segment, ZDS—Zheduotang segment, MGS—Mugecuo segment, MXS—Moxi segment).</p>
Full article ">Figure 2
<p>(<b>a</b>). Locations of the investigation sites and geological map of XSHF (the geological data are from the engineering geological petrofabric database [<a href="#B45-applsci-14-02439" class="html-bibr">45</a>]); (<b>b</b>). Simple 2D schematic illustration of the fault damage zones around a segmented left-lateral fault (modified after Kim et al. 2004 [<a href="#B1-applsci-14-02439" class="html-bibr">1</a>]).</p>
Full article ">Figure 3
<p>Exposure of bedrock at different positions of two walls in the XSHF.</p>
Full article ">Figure 4
<p>Fault damage zone distributions (strike-slip fracture frequency as bar diagrams against distance from the fault core at each profile).</p>
Full article ">Figure 5
<p>(<b>a</b>) Damage decay parameters of different damage zones in the XSHF; (<b>b</b>) Trends of damage decay parameters with displacement (modified after Savage and Brodsky (2011) [<a href="#B59-applsci-14-02439" class="html-bibr">59</a>], Savage et al. (2021) [<a href="#B50-applsci-14-02439" class="html-bibr">50</a>]; (<b>c</b>) Distributions of the width of the damage zones in normal faults and strike-slip faults with the cumulative slip on the faults (expressed in logarithmic form, normal faults and strike faults are represented by circles and squares; the blue and red dashed lines represent the fitting curves for the width of damage zone of normal and strike slip faults) [<a href="#B4-applsci-14-02439" class="html-bibr">4</a>,<a href="#B9-applsci-14-02439" class="html-bibr">9</a>,<a href="#B23-applsci-14-02439" class="html-bibr">23</a>,<a href="#B50-applsci-14-02439" class="html-bibr">50</a>,<a href="#B54-applsci-14-02439" class="html-bibr">54</a>,<a href="#B59-applsci-14-02439" class="html-bibr">59</a>,<a href="#B60-applsci-14-02439" class="html-bibr">60</a>,<a href="#B61-applsci-14-02439" class="html-bibr">61</a>,<a href="#B62-applsci-14-02439" class="html-bibr">62</a>,<a href="#B63-applsci-14-02439" class="html-bibr">63</a>,<a href="#B64-applsci-14-02439" class="html-bibr">64</a>,<a href="#B65-applsci-14-02439" class="html-bibr">65</a>].</p>
Full article ">Figure 6
<p>Two-dimensional numerical simulation of faults with different strikes and composite forms: the stress magnitude of an isolated fault between 0 and 45 MPa and the stress magnitude of two neighboring faults between 0 and 70 MPa ((<b>a</b>) regional principal compressive stress at 0° to the fault strike; (<b>b</b>) 30°; (<b>c</b>) 60°; (<b>d</b>) 90°; (<b>e</b>) Schematic diagram of the orientation of regional principal stress at an angle α to the fault strike; the regional principal stress comes from the clockwise rotation of the Sichuan–Yunnan block).</p>
Full article ">
20 pages, 4519 KiB  
Article
Shaft Wall Damage to High-Depth Inclined Ore Passes under Impact Wear Behavior
by Lichun Jiang, Haoyu Ji and Luanluan Xue
Appl. Sci. 2023, 13(24), 13065; https://doi.org/10.3390/app132413065 - 7 Dec 2023
Cited by 1 | Viewed by 983
Abstract
In order to study shaft wall damage resulting from ore drawing in ore passes, a theoretical model for predicting the shaft wall damage to high-depth inclined ore passes is constructed based on field surveys of 25 ore passes in a deep mine in [...] Read more.
In order to study shaft wall damage resulting from ore drawing in ore passes, a theoretical model for predicting the shaft wall damage to high-depth inclined ore passes is constructed based on field surveys of 25 ore passes in a deep mine in Yunnan, China. The mathematical expression of the total shaft wall damage volume is derived using the contact mechanics theory. Considering the structural characteristics of ore passes, and taking No. 1, 2, 3, and 9 ore passes as examples, combined with numerical simulation and an engineering case, the rationality of the proposed theoretical model is verified with respect to the initial collision position and the damage conditions of the shaft wall. The influence of, and sensitivity to, the ore block size P and the structural parameters of high-depth inclined ore passes on the total shaft wall damage volume Qtol are quantitatively analyzed. The results show that the calculation results of the theoretical model and numerical simulation are in good agreement with the actual engineering situations. Moreover, the ore-pass dip angle θ and the inclined angle of the chute α have a significant impact on the damage to the shaft wall, while the effects of the ore-pass depth H and the shaft diameter D are comparatively minor. With an increase in θ or α, Qtol generally first increases and then decreases. Qtol increases exponentially with P and increases steadily with D. H affects Qtol by influencing the collision frequency between the ore and the shaft wall. Therefore, in the mining design of deep mines, θ and α should be minimized as much as possible or adjusted to approach 90°, thereby reducing damage to the shaft wall. Secondly, ore block size should be strictly controlled to prevent collapses in the shaft wall caused by large ore blocks. This work provides technical support for the long-term safe operation of high-depth inclined ore passes. Full article
Show Figures

Figure 1

Figure 1
<p>The basic structure of a high-depth inclined ore pass.</p>
Full article ">Figure 2
<p>Shaft wall damage model of high-depth inclined ore pass.</p>
Full article ">Figure 3
<p>An ore pass drilled using a raise-boring machine.</p>
Full article ">Figure 4
<p>Ore collision points in a high-depth inclined ore pass of a deep mine.</p>
Full article ">Figure 5
<p>Numerical simulation results of the maximum ore indentation depth at the initial collision positions. (<b>a</b>) Operating Condition 1; (<b>b</b>) Operating Condition 2; (<b>c</b>) Operating Condition 3; (<b>d</b>) Operating Condition 4.</p>
Full article ">Figure 6
<p>Comparison of the results of the theoretical model and numerical simulation.</p>
Full article ">Figure 7
<p>Bottom of No. 2 ore pass of the deep mine.</p>
Full article ">Figure 8
<p>Initial collision position between the ore and the shaft wall of No. 1 ore pass: (<b>a</b>) laser measurement line schematic; (<b>b</b>) site diagram of initial collision position.</p>
Full article ">Figure 9
<p>Variation in the total shaft wall damage volume <span class="html-italic">Q</span><sub>tol</sub> with respect to ore-pass depth <span class="html-italic">H</span> across ore-pass dip angles.</p>
Full article ">Figure 10
<p>Variation in total shaft wall damage volume <span class="html-italic">Q</span><sub>tol</sub> with respect to ore-pass dip angle <span class="html-italic">θ</span> across ore-pass depths.</p>
Full article ">Figure 11
<p>Variation in total shaft wall damage volume <span class="html-italic">Q</span><sub>tol</sub> with respect to the inclined angle of the chute <span class="html-italic">α</span> across ore-pass depths.</p>
Full article ">Figure 12
<p>Variation in total shaft wall damage volume <span class="html-italic">Q</span><sub>tol</sub> with respect to the shaft diameter <span class="html-italic">D</span> across ore-pass dip angles.</p>
Full article ">Figure 13
<p>Variation in total shaft wall damage volume <span class="html-italic">Q</span><sub>tol</sub> with respect to the ore block size <span class="html-italic">P</span> across ore-pass depths.</p>
Full article ">Figure 14
<p>Sensitivity comparison of influencing factors.</p>
Full article ">
17 pages, 4732 KiB  
Article
A Numerical Study of the Dynamic Crack Behavior of Brittle Material Induced by Blast Waves
by Haijun Yu, Ming Zou, Jinshan Sun, Yuntao Wang and Meng Wang
Materials 2023, 16(22), 7142; https://doi.org/10.3390/ma16227142 - 13 Nov 2023
Viewed by 967
Abstract
Blast stress waves profoundly impact engineering structures, exciting and affecting the rupture process in brittle construction materials. A novel numerical model was introduced to investigate the initiation and propagation of cracks subjected to blast stress waves within the borehole-crack configuration. Twelve models were [...] Read more.
Blast stress waves profoundly impact engineering structures, exciting and affecting the rupture process in brittle construction materials. A novel numerical model was introduced to investigate the initiation and propagation of cracks subjected to blast stress waves within the borehole-crack configuration. Twelve models were established with different crack lengths to simulate sandstone samples. The influence of crack length on crack initiation and propagation was investigated using those models. The linear equation of state was used to express the relationship between the pressure and density of the material. The major principal stress failure criterion was used to evaluate the failure of elements. A triangular pressure curve was adopted to produce the blast stress wave. The results indicated that the pre-crack length critically influenced the crack initiation and propagation mechanism by analyzing the stress history at the crack tip, crack propagation velocity, and distance. The inducement of a P-wave and S-wave is paramount in models with a short pre-crack. For long pre-crack models, Rayleigh waves significantly contribute to crack propagation. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of fractured rock mass blasting.</p>
Full article ">Figure 2
<p>Numerical model.</p>
Full article ">Figure 3
<p>An acoustic velocimeter (Sonic Viewer-SX, Output voltage: 500 V, Pulse width: 6 μs).</p>
Full article ">Figure 4
<p>Stress wave-induced particle velocity vectors.</p>
Full article ">Figure 5
<p>Displacements along the crack surface.</p>
Full article ">Figure 6
<p>Velocity vectors on crack surface induced by Rayleigh wave.</p>
Full article ">Figure 7
<p>Illustration of the bilinear relationship.</p>
Full article ">Figure 8
<p>Loading curve.</p>
Full article ">Figure 9
<p>Particle velocity vectors near the crack surface.</p>
Full article ">Figure 10
<p>Stress history curves at the crack tip.</p>
Full article ">Figure 11
<p>Motion paths of particles along the crack’s upper surface ((<b>a</b>–<b>h</b>), motion paths of particles; (<b>i</b>), display of measurement point layout).</p>
Full article ">Figure 12
<p>Velocity vectors around a running crack tip.</p>
Full article ">Figure 13
<p>The continuous decrease in crack propagation velocity and distance of different crack lengths until stable variation characteristics.</p>
Full article ">Figure 14
<p>The explosion experiment and the crack-propagating velocity were recorded in the experiment [<a href="#B5-materials-16-07142" class="html-bibr">5</a>].</p>
Full article ">
15 pages, 8626 KiB  
Article
The Influence of Different Shear Directions on the Shear Resistance Characteristics of Rock Joints
by Xipeng Lai, Wei Yuan, Wei Wang, Ruifeng Sun, Pengzhao Du, Hang Lin, Xiaodong Fu, Qinghe Niu and Chao Yin
Buildings 2023, 13(10), 2556; https://doi.org/10.3390/buildings13102556 - 10 Oct 2023
Viewed by 955
Abstract
The joint roughness coefficient JRC of rock joints is an important parameter for measuring the geometric morphology of rock joints. However, the parameter obtained from traditional calculation methods has certain limitations in reflecting the differences in shear strength of rock joints in different [...] Read more.
The joint roughness coefficient JRC of rock joints is an important parameter for measuring the geometric morphology of rock joints. However, the parameter obtained from traditional calculation methods has certain limitations in reflecting the differences in shear strength of rock joints in different shear directions with the same orientation. Firstly, native joint surface test blocks were cast using three-dimensional reverse reconstruction technology. Subsequently, direct shear tests were conducted under different normal stress and shear direction conditions, followed by numerical simulations using the finite difference software Flac3d. The JRC coefficient calculation method proposed by Yuan was modified and extended by considering the percentage of climbing sections and the effective contact area during the ramping process. This study indicates that the numerical simulation results are in good agreement with the shear test results. The introduction of the shear climbing rate SCR and the curvature coefficient of profile CCP is used to reflect the geometric differences of the joint surfaces in different shear directions. These two parameters are nonlinearly fitted with the experimental results, leading to a calculation formula that characterizes the shear strength characteristics of the joint surfaces in different shear directions. This novel formula is an extension of the JRC–JCS model. Full article
Show Figures

Figure 1

Figure 1
<p>The manual specimen casting process.</p>
Full article ">Figure 2
<p>Installation of anchorage performance tester and accessories for anchored structural plane.</p>
Full article ">Figure 3
<p>Boundary conditions for joint shear simulation.</p>
Full article ">Figure 4
<p>Schematic diagram of normal stiffness calculation: (<b>a</b>) normal stress vs deformation relations of intact and fractured specimens; (<b>b</b>) maximum closure V<sub>m</sub> calculation chart.</p>
Full article ">Figure 5
<p>Schematic diagram of shear stiffness calculation.</p>
Full article ">Figure 6
<p>Shear stress variation diagram under different conditions.</p>
Full article ">Figure 7
<p>Shear failure condition: (<b>a</b>) shearing damage process, (<b>b</b>) shear-damaged surface.</p>
Full article ">Figure 8
<p>Peak shear strength comparison chart: (<b>a</b>) The stress–displacement comparison curve, (<b>b</b>–<b>d</b>) comparison of peak shear strength for different shear directions in S-S, M-M, and H-H combination.</p>
Full article ">Figure 8 Cont.
<p>Peak shear strength comparison chart: (<b>a</b>) The stress–displacement comparison curve, (<b>b</b>–<b>d</b>) comparison of peak shear strength for different shear directions in S-S, M-M, and H-H combination.</p>
Full article ">Figure 9
<p>Schematic diagram of 2D section line index calculation.</p>
Full article ">Figure 10
<p>Schematic diagram of the rock joint 3D printing area: (<b>a</b>) profile line selection; (<b>b</b>) rock joint morphology information.</p>
Full article ">Figure 11
<p>Schematic diagram of profile line discretization.</p>
Full article ">Figure 12
<p>Multivariate nonlinear fitting.</p>
Full article ">Figure 13
<p>Comparison chart of calculation results: (<b>a</b>–<b>c</b>) Values of peak shear strength in different shear directions under normal stress conditions of 1 MPa, 2 MPa, and 3 MPa.</p>
Full article ">
15 pages, 11185 KiB  
Article
Simulation Study on Fire Product Movement Law and Evacuation in a University High-Rise Teaching Building
by Yan Cui, Hao Wang, Bo You, Chuan Cheng and Ming Li
Appl. Sci. 2023, 13(18), 10532; https://doi.org/10.3390/app131810532 - 21 Sep 2023
Cited by 2 | Viewed by 1188
Abstract
High-rise teaching buildings are complex public buildings that combine the evacuation risks of school buildings and high-rise buildings. In this regard, studying fire product transport patterns and personnel evacuation characteristics of high-rise school buildings is crucial for safe and rapid evacuation. In this [...] Read more.
High-rise teaching buildings are complex public buildings that combine the evacuation risks of school buildings and high-rise buildings. In this regard, studying fire product transport patterns and personnel evacuation characteristics of high-rise school buildings is crucial for safe and rapid evacuation. In this paper, we applied Pyrosim2018 software to build a model of a teaching building and performed numerical fire simulation to analyze temperature, CO gas, and visibility to determine the available evacuation time ASET; meanwhile, we performed evacuation simulation by Pathfinder 2019 to determine the required evacuation time and analyze the congestion problem during evacuation. By improving the evacuation route, secondary simulations were conducted and compared with the previous results. The results show that visibility is the main factor affecting evacuation in of the event of a fire in this school building. Based on the visibility analysis, it is recommended that personnel evacuate from floors four and above within 709.2 S when the fire location is at a specific position on the third floor. While the original safety exits of the school building can avoid a large number of casualties, they cannot guarantee the safe evacuation of all people, and planning a reasonable evacuation route can obviously relieve the evacuation pressure in the high-rise corridor. Full article
Show Figures

Figure 1

Figure 1
<p>Model of the teaching building: (<b>a</b>) exterior view of the school building and (<b>b</b>) perspective view of the building.</p>
Full article ">Figure 2
<p>Structures of the first and second floors: (<b>a</b>) structure of the first floor and (<b>b</b>) structure of the second floor.</p>
Full article ">Figure 3
<p>Structure of the third floor (same structure from three to six floors).</p>
Full article ">Figure 4
<p>Location of the fire source and measurement point.</p>
Full article ">Figure 5
<p>Temperature distributions of four points with time: (<b>a</b>) temperature distribution of point A with time; (<b>b</b>) temperature distribution of point B with time; (<b>c</b>) temperature distribution of point C with time; and (<b>d</b>) temperature distribution of point D with time.</p>
Full article ">Figure 6
<p>CO concentration variation: (<b>a</b>) CO concentration variation of point A; (<b>b</b>) CO concentration variation of point B; (<b>c</b>) CO concentration variation of point C; and (<b>d</b>) CO concentration variation of point D.</p>
Full article ">Figure 7
<p>Changes in visibility: (<b>a</b>) visibility slice (20.4 s); (<b>b</b>) visibility slice (30.0 s); (<b>c</b>) visibility slice (100.8 s); and (<b>d</b>) visibility slice (709.2 s).</p>
Full article ">Figure 8
<p>Evacuation model of teaching building.</p>
Full article ">Figure 9
<p>Personnel distribution in the teaching building.</p>
Full article ">Figure 10
<p>Distribution of people at different evacuation simulation times (disordered): (<b>a</b>) 20.4 s; (<b>b</b>) 200.1 s; (<b>c</b>) 300 s; and (<b>d</b>) 619.5 s.</p>
Full article ">Figure 10 Cont.
<p>Distribution of people at different evacuation simulation times (disordered): (<b>a</b>) 20.4 s; (<b>b</b>) 200.1 s; (<b>c</b>) 300 s; and (<b>d</b>) 619.5 s.</p>
Full article ">Figure 11
<p>Relationship between evacuation time and the number of evacuees.</p>
Full article ">Figure 12
<p>Relationship between flow rates for selected doors and time in cases of disorderly evacuation.</p>
Full article ">Figure 13
<p>Roadmap for orderly evacuation of each floor: (<b>a</b>) first floor; (<b>b</b>) second floor; (<b>c</b>) third floor; (<b>d</b>) fourth floor; (<b>e</b>) fifth floor; and (<b>f</b>) sixth floor.</p>
Full article ">Figure 14
<p>Relationship between flow rates for selected doors and time in case of orderly evacuation.</p>
Full article ">
12 pages, 3586 KiB  
Article
Study on the Particle Surface Fractal Characteristics of Sulfide Ores
by Yan Cui, Jimeng Wang, Chuan Cheng, Bo You, Yong Liu and Ming Li
Appl. Sci. 2023, 13(16), 9199; https://doi.org/10.3390/app13169199 - 12 Aug 2023
Viewed by 1175
Abstract
The fractal dimension is widely used in many fields as a parameter to characterize the geometric complexity and geometric distribution relationship of research objects. To study the surface characteristics of sulfide ore particles, the fractal theory was applied to quantitatively characterize the surface [...] Read more.
The fractal dimension is widely used in many fields as a parameter to characterize the geometric complexity and geometric distribution relationship of research objects. To study the surface characteristics of sulfide ore particles, the fractal theory was applied to quantitatively characterize the surface fractal dimension Ds of sulfide ore microparticles in three particle size ranges, 60–100 mesh, 100–140 mesh and >200 mesh, based on the area–perimeter method. Using an optical microscope, grain projection images of the particles were obtained. The grain shape and characteristics of sulfide ore particles were studied by means of an image processing system. The results demonstrate that the grain shape of sulfide ore particles can be expressed by fractal dimension, and the particle surface fractal dimension ranges from 2.4392 to 2.5492. It was found that the fractal properties begin to decrease due to the increasing of the particle size. The larger the fractal dimension, the finer the particles are. The fractal dimension of sulfide ore particles can be used as an important indicator of their particle shape distribution characteristics, which can provide important information for further study of the relevant physical and chemical properties of sulfide ore particles and provide a new theoretical method and basis for the adhesion and removal of sulfide ore dust. With the quantitative description of the fractal distribution of sulfide ore particles, a new way to study the adhesive force between particles is offered for further research. Full article
Show Figures

Figure 1

Figure 1
<p>Typical mineralogical X-ray analysis of mineral dust.</p>
Full article ">Figure 2
<p>Mineralogical observation using optical microscope. (<b>a</b>) Brechified granular pyrite cemented by dissolution of sphalerite. (<b>b</b>) Euhedral pyrite particle distributed in vein quartz. (<b>c</b>) Fine chalcopyrite particles filling fractures of pyrite. (<b>d</b>) Pyrite attached with galena.</p>
Full article ">Figure 2 Cont.
<p>Mineralogical observation using optical microscope. (<b>a</b>) Brechified granular pyrite cemented by dissolution of sphalerite. (<b>b</b>) Euhedral pyrite particle distributed in vein quartz. (<b>c</b>) Fine chalcopyrite particles filling fractures of pyrite. (<b>d</b>) Pyrite attached with galena.</p>
Full article ">Figure 3
<p>Images of the sample. (<b>a</b>) Ground ore sample of 60~100 mesh. (<b>b</b>) Ground ore sample of 100~140 mesh. (<b>c</b>) Ground ore sample &gt; 200 mesh. (<b>d</b>) SEM photograph of the ore sample (&gt;200 mesh ore sample).</p>
Full article ">Figure 4
<p>Binary images of the sulfide ore particles. (<b>a</b>) Ore sample of 60~100 mesh. (<b>b</b>) Ore sample of 100~140 mesh. (<b>c</b>) Ore sample of more than 200 mesh.</p>
Full article ">Figure 5
<p><span class="html-italic">lgL-lgA</span> curves of three sulfide ore microparticles. (<b>a</b>) Fractal curve of 60–100 mesh sulfide ore microparticles. (<b>b</b>) Fractal curve of 100–140 mesh sulfide ore microparticles. (<b>c</b>) Fractal curve of microparticles of sulfide ore larger than 200 mesh.</p>
Full article ">Figure 5 Cont.
<p><span class="html-italic">lgL-lgA</span> curves of three sulfide ore microparticles. (<b>a</b>) Fractal curve of 60–100 mesh sulfide ore microparticles. (<b>b</b>) Fractal curve of 100–140 mesh sulfide ore microparticles. (<b>c</b>) Fractal curve of microparticles of sulfide ore larger than 200 mesh.</p>
Full article ">Figure 6
<p>Curve of the relationship between particle size and fractal dimension.</p>
Full article ">
23 pages, 7743 KiB  
Article
Investigation on the Stress and Deformation Evolution Laws of Shield Tunnelling through a Mining Tunnel Structure
by Entong Du, Lei Zhou and Ruizhen Fei
Appl. Sci. 2023, 13(14), 8489; https://doi.org/10.3390/app13148489 - 22 Jul 2023
Cited by 2 | Viewed by 1262
Abstract
In the construction of a shield crossing an existing mined tunnel without load, it is imperative to develop corresponding design standards that reflect actual engineering force characteristics to ensure the successful completion of the tunnel construction. This study uses the MIDAS-GTS NX 2022 [...] Read more.
In the construction of a shield crossing an existing mined tunnel without load, it is imperative to develop corresponding design standards that reflect actual engineering force characteristics to ensure the successful completion of the tunnel construction. This study uses the MIDAS-GTS NX 2022 finite element software to facilitate the creation of a numerical model of a shield structure for an air-push-over mine tunnel project in Changsha, China while investigating the stress field’s evolution during shield construction and calculating the maximum positive and negative bending moments and maximum axial forces for different structures and other force states under various construction conditions. This study’s findings informed the design and construction optimisation of a shield tunnelling empty-push method. The outcomes of this numerical simulation led to several key findings: (1) The soil density exerted a significantly greater impact on the internal forces of the initial support structure than both the tunnel depth and soil Poisson’s ratio. Additionally, a sudden shift in internal forces occurred within the 300–350 mm range when the lining thickness was altered. (2) Factors such as the tunnel depth, soil density, soil Poisson’s ratio μ, and lining thickness similarly influenced the internal forces of the segment and the initial support. Notably, the backfill layer thickness significantly affected the segment’s maximum axial force, causing an abrupt change of approximately 300 mm. (3) It is essential to control the guide rail’s thickness under the shield machine equipment’s weight constraint to prevent it from becoming overly large. Full article
Show Figures

Figure 1

Figure 1
<p>The engineering geological distribution map and plan view of the undermining section.</p>
Full article ">Figure 2
<p>Cross-sectional view of the mining method tunnel.</p>
Full article ">Figure 3
<p>Finite element calculation models. (<b>a</b>) Finite element calculation models of each structure; (<b>b</b>) boundary conditions of finite element calculation models.</p>
Full article ">Figure 4
<p>Displacement cloud map for the second construction stage. (<b>a</b>) the displacement values in the x, y and z directions after the initial support construction; (<b>b</b>) the displacement values in the x, y and z directions after the lower half of the gravel construction; (<b>c</b>) the displacement values in the x, y and z directions after the tunnel lining segment construction; (<b>d</b>) the displacement values in the x, y and z directions after the upper half of the gravel construction with a half symbol.</p>
Full article ">Figure 4 Cont.
<p>Displacement cloud map for the second construction stage. (<b>a</b>) the displacement values in the x, y and z directions after the initial support construction; (<b>b</b>) the displacement values in the x, y and z directions after the lower half of the gravel construction; (<b>c</b>) the displacement values in the x, y and z directions after the tunnel lining segment construction; (<b>d</b>) the displacement values in the x, y and z directions after the upper half of the gravel construction with a half symbol.</p>
Full article ">Figure 5
<p>Tunnel x, y and z direction displacement values after single tunnel completion. (<b>a</b>) x direction displacement value of the tunnel after the completion of the left and right tunnel construction; (<b>b</b>) y direction displacement value of the tunnel after the completion of the left and right tunnel construction; (<b>c</b>) z direction displacement value of the tunnel after the completion of the left and right tunnel construction.</p>
Full article ">Figure 6
<p>Initial support stress variation curve. (<b>a</b>) influence curve of tunnel burial depth on initial support stress; (<b>b</b>) influence curve of soil bulk density on initial support stress; (<b>c</b>) influence curve of soil Poisson’s ratio on initial support stress; and (<b>d</b>) influence curve of initial support thickness on initial support stress.</p>
Full article ">Figure 7
<p>Segment stress variation curve. (<b>a</b>) Influence curve of tunnel depth on segment stress; (<b>b</b>) influence curve of soil unit weight on segment stress; (<b>c</b>) influence curve of soil Poisson’s ratio on segment stress; (<b>d</b>) influence curve of lining thickness on segment stress; and (<b>e</b>) influence curve of backfill thickness on segment stress.</p>
Full article ">Figure 7 Cont.
<p>Segment stress variation curve. (<b>a</b>) Influence curve of tunnel depth on segment stress; (<b>b</b>) influence curve of soil unit weight on segment stress; (<b>c</b>) influence curve of soil Poisson’s ratio on segment stress; (<b>d</b>) influence curve of lining thickness on segment stress; and (<b>e</b>) influence curve of backfill thickness on segment stress.</p>
Full article ">Figure 8
<p>Guide platform stress variation curve. (<b>a</b>) Influence curve of shield body weight on guide platform stress; (<b>b</b>) influence curve of guide thickness on guide platform stress; and (<b>c</b>) influence curve of subgrade reaction coefficient on guide stress.</p>
Full article ">
17 pages, 8897 KiB  
Article
A DEM Study on Bearing Behavior of Floating Geosynthetic-Encased Stone Column in Deep Soft Clays
by Feng Liu, Panpan Guo, Xunjian Hu, Baojian Li, Haibo Hu and Xiaonan Gong
Appl. Sci. 2023, 13(11), 6838; https://doi.org/10.3390/app13116838 - 5 Jun 2023
Viewed by 1141
Abstract
The use of geosynthetic-encased stone columns has been proven to be an economical and effective method for soft soil foundation treatment. This method is widely used in civil engineering projects at home and abroad. When the geosynthetic-encased stone columns are applied to deep [...] Read more.
The use of geosynthetic-encased stone columns has been proven to be an economical and effective method for soft soil foundation treatment. This method is widely used in civil engineering projects at home and abroad. When the geosynthetic-encased stone columns are applied to deep soft clays, they are in a floating state. The load-bearing deformation mechanism of geosynthetic-encased stone columns has changed. The interaction between the aggregates, geogrid, and soil is worth studying, especially at the bottom of the column. In this paper, the discrete element method is used to simulate a floating geosynthetic-encased stone column with a 280 mm encasement depth in deep soft clays. The load-bearing deformation characteristics and mesoscopic mechanism of the floating geosynthetic-encased stone column are studied. The results show that there are large vertical and radial stresses in the top region. Moreover, the porosity and sliding fraction of aggregates in this region increase with settlement, and the coordination number decreases with settlement. The vertical and radial stresses of the soil near the column body are not affected much by the column body. When the encasement depth exceeds 280 mm, the bearing capacity of the FGESC does not increase much. The encasement depth controls the failure mode of the floating geosynthetic-encased stone column. As the encasement depth increases, the failure mode of the floating geosynthetic-encased stone column gradually transitions from swelling deformation to penetration failure. Full article
Show Figures

Figure 1

Figure 1
<p>Unit cell idealization: (<b>a</b>) Group of FGESCs. (<b>b</b>) Influence zone of FGESC. (<b>c</b>) Unit cell.</p>
Full article ">Figure 2
<p>A unit cell of an FGESC in soft clay: (<b>a</b>) Components and dimensions of the DEM model for the FGESC. (<b>b</b>) Sectional view of the DEM model for FGESC.</p>
Full article ">Figure 3
<p>Measurement sphere in the model.</p>
Full article ">Figure 4
<p>Schematic diagram of the laboratory test.</p>
Full article ">Figure 5
<p>The FGESC laboratory test.</p>
Full article ">Figure 6
<p>Load–settlement curves from DEM model and laboratory test.</p>
Full article ">Figure 7
<p>Vertical stresses of the FGESC and underlying soil.</p>
Full article ">Figure 8
<p>Radial stresses of the FGESC and underlying soil.</p>
Full article ">Figure 9
<p>Contact force of FGESC in soft clay: (<b>a</b>) When the settlement is 18 mm, the maximum contact force is 2075 KN. (<b>b</b>) When the settlement is 36 mm, the maximum contact force is 2098 KN.</p>
Full article ">Figure 10
<p>Porosity changes of the FGESC with the settlement.</p>
Full article ">Figure 11
<p>Coordination number changes of the FGESC with the settlement.</p>
Full article ">Figure 12
<p>Sliding fraction changes of the FGESC with the settlement.</p>
Full article ">Figure 13
<p>Vertical stresses of the soil around the column and the underlying stratum at various distances from the column center: (<b>a</b>) 65 mm and (<b>b</b>) 105 mm.</p>
Full article ">Figure 14
<p>Radial stresses of the soil around the column and the underlying stratum at various distances from the column center: (<b>a</b>) 65 mm and (<b>b</b>) 105 mm.</p>
Full article ">Figure 15
<p>Changes of column body with settlement: (<b>a</b>) 0 mm, (<b>b</b>) 18 mm, and (<b>c</b>) 36 mm.</p>
Full article ">Figure 16
<p>Changes of column bottom with settlement: (<b>a</b>) 0 mm, (<b>b</b>) 18 mm, and (<b>c</b>) 36 mm.</p>
Full article ">Figure 17
<p>Load-bearing capacity of FGESC with different encasement depths.</p>
Full article ">Figure 18
<p>Contact force of the FGESC with different encasement depths: (<b>a</b>) 100 mm, (<b>b</b>) 180 mm, (<b>c</b>) 280 mm, and (<b>d</b>) 360 mm.</p>
Full article ">Figure 19
<p>Changes of column body with different encasement depths: (<b>a</b>) 100 mm, (<b>b</b>) 180 mm, (<b>c</b>) 280 mm, and (<b>d</b>) 360 mm.</p>
Full article ">Figure 20
<p>Changes of column bottom with different encasement depths: (<b>a</b>) 100 mm, (<b>b</b>) 180 mm, (<b>c</b>) 280 mm, and (<b>d</b>) 360 mm.</p>
Full article ">
11 pages, 3092 KiB  
Article
A Mathematical Model for Predicting the Droplet Size of Micro-Fog Nozzle with Circular-Hole Rotating Core Based on Orthogonal Design
by Yan Cui, Chuan Cheng, Pengfei Wang, Yong Liu, Runqiu Li, Yong Zhang, Ming Li and Shilin Li
Appl. Sci. 2023, 13(11), 6670; https://doi.org/10.3390/app13116670 - 30 May 2023
Cited by 1 | Viewed by 1206
Abstract
The circular-hole rotating core fog nozzle has excellent atomization performance and has been widely used in the realm of spray dust. As part of this study, a mathematical model was developed for predicting the Sauter mean diameter (SMD) of nozzles of this type. [...] Read more.
The circular-hole rotating core fog nozzle has excellent atomization performance and has been widely used in the realm of spray dust. As part of this study, a mathematical model was developed for predicting the Sauter mean diameter (SMD) of nozzles of this type. The coaction between the SMD of the nozzle and the three influencing factors of axial distance, water supply pressure, and outlet diameter was investigated based on the customized spray’s experimental platform and orthogonal design method. According to the comparative analysis of the size range, the axial distance, outlet diameter and water supply pressure are three parameters that affect the SMD of the nozzle, and the degree of influence is axial distance > outlet diameter > water supply pressure. On this basis, a mathematical model was developed using the multiple regression method to predict the SMD of the nozzle. We analyzed the results and compared them to the SMD value predicted by the multiple regression mathematical model and the orthogonal experiment results. The change trend was the same, the values were essentially the same, and the average relative error was just 16.11%. Accordingly, the mathematical model presented in this paper may be used for the prediction and calculation of the droplet size for circular-hole rotating core micro-fog nozzles. Full article
Show Figures

Figure 1

Figure 1
<p>Experimental system.</p>
Full article ">Figure 2
<p>Experimental site: (<b>a</b>) Malvern particle size analyzer; (<b>b</b>) computer system; (<b>c</b>) control cabinet.</p>
Full article ">Figure 3
<p>The test used a circular-hole rotating core micro-fog nozzle and structure: (<b>a</b>) nozzle shape; (<b>b</b>) 0.7 mm nozzle structure diagram.</p>
Full article ">Figure 4
<p>Droplet size distribution under different water supply pressures and outlet diameters at a 70 cm axial distance of the circular-hole rotating core micro-fog nozzle.</p>
Full article ">Figure 5
<p>Comprehensive mean and range of three factors: (<b>a</b>) axial distance and SMD; (<b>b</b>) outlet diameter and SMD; (<b>c</b>) water supply pressure and SMD.</p>
Full article ">Figure 6
<p>Comparison between SMD experimental value and predicted value.</p>
Full article ">Figure 7
<p>Comparison of experimental and predicted values of the SMD in the literature.</p>
Full article ">
17 pages, 5306 KiB  
Article
Digital Rock Analysis on the Influence of Coarse Micro-Fractures on Petrophysical Properties in Tight Sandstone Reservoirs
by Lei Liu, Jun Yao, Hai Sun, Lei Zhang and Kai Zhang
Appl. Sci. 2023, 13(9), 5237; https://doi.org/10.3390/app13095237 - 22 Apr 2023
Cited by 3 | Viewed by 1576
Abstract
Tight sandstone reservoirs, as typical unconventional reservoirs, have attracted more and more attention worldwide. Compared to conventional reservoirs, the complex microscopic pore structures and micro-fractures of the tight reservoirs are developed, and fluid flow in the tight sandstone reservoir is very complicated. Therefore, [...] Read more.
Tight sandstone reservoirs, as typical unconventional reservoirs, have attracted more and more attention worldwide. Compared to conventional reservoirs, the complex microscopic pore structures and micro-fractures of the tight reservoirs are developed, and fluid flow in the tight sandstone reservoir is very complicated. Therefore, studying the influence of fractures on the rock topological structure and the flow characteristics between micro-fractures and the matrix is critical to the development of tight sandstone reservoirs. In light of the intricate nature of micro-fractures, digital rock analysis technology is utilized to address this issue instead of traditional experimental methods. Firstly, the selected tight rock is scanned by X-ray computed tomography (XCT), and then the natural tight digital rock is reconstructed by filtering and binary segmentation. Secondly, micro-fracture with different shapes is added to the digital rock. Then, a pore network model extracted by the maximum ball method is adopted to conduct the flow simulation. The study finds that the distribution of pore throat radius changes with increasing fracture aperture and length and that the permeability and capillary pressure curves are influenced by fracture aperture and length in the direction of connectivity. The impact of micro-fracture dip angle on pore throat structure is significant with changes in permeability and fluid flow in different directions. Overall, the study emphasizes the importance of fracture aperture and length in determining the properties and behavior of tight sandstone reservoirs and highlights the usefulness of digital rock analysis technology in providing insights into complex microstructures. Full article
Show Figures

Figure 1

Figure 1
<p>The sample of tight sandstone. (<b>a</b>) is the gray-scale image of the tight sample, (<b>b</b>) is the tight digital rock. The red color represents pore space and purple color indicates grain space.</p>
Full article ">Figure 2
<p>The result of REV analysis is based on porosity and permeability. (<b>a</b>) is for porosity and (<b>b</b>) is for permeability.</p>
Full article ">Figure 3
<p>The rough-walled surface with different surface fractal dimensions. (<b>a</b>) shows the random fracture surface for <span class="html-italic">f<sub>D</sub></span> = 0.5, (<b>b</b>) is the random fracture surface for <span class="html-italic">f<sub>D</sub></span> = 1.0, (<b>c</b>) represents the random fracture surface for <span class="html-italic">f<sub>D</sub></span> = 1.5, and (<b>d</b>) displays the random fracture surface for <span class="html-italic">f<sub>D</sub></span> = 1.8.</p>
Full article ">Figure 4
<p>The rough-walled surface with different numbers of waves. (<b>a</b>) shows the random fracture surface for <span class="html-italic">M</span> = 20, (<b>b</b>) is the random fracture surface for <span class="html-italic">M</span> = 40, (<b>c</b>) represents the random fracture surface for <span class="html-italic">M</span> = 60, and (<b>d</b>) displays the random fracture surface for <span class="html-italic">M</span> = 80.</p>
Full article ">Figure 5
<p>The digital rocks embedding an artificial fracture with a different aperture and pore networks extracted using the maximal balls method. (<b>a</b>) shows the digital rock and pore network with the micro-fracture whose aperture is 2 μm, (<b>b</b>) is the digital rock and pore network with the micro-fracture whose aperture is 10 μm, (<b>c</b>) represents the digital rock and pore network with the micro-fracture whose aperture is 30 μm, and (<b>d</b>) displays the digital rock and pore network with the micro-fracture whose aperture is 50 μm.</p>
Full article ">Figure 6
<p>The pore structure distribution of the embedding an artificial fracture with different aperture. (<b>a</b>) is the pore radius distribution, and (<b>b</b>) is the throat radius distribution.</p>
Full article ">Figure 7
<p>The contribution for permeability of embedding an artificial fracture with different apertures. The pore’s contribution to permeability is (<b>a</b>) while the throat’s contribution to permeability is (<b>b</b>).</p>
Full article ">Figure 8
<p>The capillary pressure curve of embedding an artificial fracture with a different aperture in different directions. (<b>a</b>) X direction, (<b>b</b>) Y direction, (<b>c</b>) Z direction.</p>
Full article ">Figure 9
<p>The digital rocks embedding an artificial fracture with a different length and pore networks extracted using the maximal balls method. (<b>a</b>) shows the digital rock and pore network with the micro-fracture whose length is 50 μm, (<b>b</b>) is the digital rock and pore network with the micro-fracture whose length is 200 μm, (<b>c</b>) represents the digital rock and pore network with the micro-fracture whose length is 300 μm, and (<b>d</b>) displays the digital rock and pore network with the micro-fracture whose length is 50 μm.</p>
Full article ">Figure 10
<p>The pore structure distribution of the embedding artificial fracture with different lengths. (<b>a</b>) is the pore radius distribution, and (<b>b</b>) is the throat radius distribution.</p>
Full article ">Figure 11
<p>The contribution for permeability of embedding an artificial fracture with different lengths. The pore’s contribution to permeability is (<b>a</b>), while the throat’s contribution to permeability is (<b>b</b>).</p>
Full article ">Figure 12
<p>The capillary pressure curve of the embedding is an artificial fracture with different lengths in different directions. (<b>a</b>) is for X direction, (<b>b</b>) is for Y direction, (<b>c</b>) is for Z direction.</p>
Full article ">Figure 13
<p>The digital rocks embedding an artificial fracture with a different dip angle and pore networks extracted using the maximal balls method. (<b>a</b>) shows the digital rock and pore network with the micro-fracture whose dip angle is 10°, (<b>b</b>) is the digital rock and pore network with the micro-fracture whose dip angle is 20°, (<b>c</b>) represents the digital rock and pore network with the micro-fracture whose dip angle is 30°, and (<b>d</b>) displays the digital rock and pore network with the micro-fracture whose dip angle is 40°.</p>
Full article ">Figure 14
<p>The pore structure distribution of the embedding an artificial fracture with different dip angles. (<b>a</b>) pore radius distribution and (<b>b</b>) throat radius distribution.</p>
Full article ">Figure 15
<p>The contribution for permeability of embedding an artificial fracture with different dip angles. The pore’s contribution to permeability is (<b>a</b>) while the throat’s contribution to permeability is (<b>b</b>).</p>
Full article ">Figure 16
<p>The capillary pressure curve of embedding an artificial fracture with different dip angles in different directions. (<b>a</b>) is for the X direction, (<b>b</b>) is for the Y direction, and (<b>c</b>) is for the Z direction.</p>
Full article ">
27 pages, 14410 KiB  
Article
A Theory of Slope Shear Scouring and the Failure Mechanism of PFC3D on a Gangue Slope
by Yun Tian, Yong Wu, Hao Wang, Hongtao Li, Lindong He and Hong Zhao
Appl. Sci. 2023, 13(8), 5066; https://doi.org/10.3390/app13085066 - 18 Apr 2023
Cited by 1 | Viewed by 1714
Abstract
In this paper, scouring shear failure theory is optimized based on the gangue slope near the thermal power field in Baiguo Town, Panzhou City, Guizhou Province. Based on the particle flow PFC (particle flow code) 3D fluid–solid coupling method, the scouring failure mechanism [...] Read more.
In this paper, scouring shear failure theory is optimized based on the gangue slope near the thermal power field in Baiguo Town, Panzhou City, Guizhou Province. Based on the particle flow PFC (particle flow code) 3D fluid–solid coupling method, the scouring failure mechanism of ditch no. 5 of the gangue slope is comprehensively analyzed from the perspectives of the failure mode, displacement, motion track, and stress–strain. We consider the scouring shear theory in respect of (c, φ); this theory is dominated by two types of scouring intensity factors and can effectively explain the internal mechanisms of gully formation. The rainfall scouring failure of gangue slopes can be divided into four stages: (1) integral splash erosion and local pitting at the bottom of the slope; (2) erosion diversion and pitting in the slope; (3) the tributary–slope crest extension schist erosion stage; and (4) integral gully erosion and the landslide stage. The failure process is not only characterized by discontinuous failure but also occurs in the order of bottom–middle–branch–top. A three-section stepped effect is observed during the process in which the gangue is scoured and destroyed, which fully verifies the intermittent characteristics of the scouring and destruction of gangue slopes. During the whole process, the maximum displacement is concentrated at the top of the slope, and its proportions are as follows: top of the slope > tributary > middle of the slope > foot of the slope. The peak displacement of the slope crest in the horizontal Y-direction accounts for 41.76%, and that in the Z-direction accounts for 45.84%. Scouring deposits can be divided into the arc erosion deposit mode and the sector erosion deposit mode. Mainstream gullies primarily control whether deposits are characterized as arc or straight erosion deposits. The later stage of the second phase of scouring is the incubation period of the tributary gully. The large accumulation makes the stress at the bottom of the slope increase sharply, and the fluctuation value is between 2 and 6.8 MPa. The generation of the branch notch is mainly determined by X-direction stress, and 8.6 MPa is the critical stress. In efforts to prevent and control rainfall and landslide, the slope foot area should be preferentially protected, and the soil mass in the slope should be reduced to prevent the maximum energy fluctuation caused by scouring, so as to prevent significant displacement damage of the slope top. Full article
Show Figures

Figure 1

Figure 1
<p>Principle of the washout assay.</p>
Full article ">Figure 2
<p>Top view of the site.</p>
Full article ">Figure 3
<p>Gully no. 5.</p>
Full article ">Figure 4
<p>Generation and evolution effects of clump 1. (<b>a</b>). Coal gangue real shot; (<b>b</b>). ratio = 0.5, distance = 100; (<b>c</b>). ratio = 0.5, distance = 110; (<b>d</b>). ratio = 0.5, distance = 130; (<b>e</b>). ratio = 0.3, distance = 100; (<b>f</b>). ratio = 0.3, distance = 120; (<b>g</b>). ratio = 0.3, distance = 145; (<b>h</b>). ratio = 0.5, distance = 160.</p>
Full article ">Figure 5
<p>Generation and evolution effects of clump 2. (<b>a</b>). Coal gangue real shot; (<b>b</b>). ratio = 0.5, distance = 100; (<b>c</b>). ratio = 0.5, distance = 110; (<b>d</b>). ratio = 0.5, distance = 130; (<b>e</b>). ratio = 0.3, distance = 100; (<b>f</b>). ratio = 0.3, distance = 120; (<b>g</b>). ratio = 0.3, distance = 145; (<b>h</b>). ratio = 0.5, distance = 160.</p>
Full article ">Figure 6
<p>Schematic diagram of the triaxial test.</p>
Full article ">Figure 7
<p>Stress–strain curves of the numerical triaxial tests of the gangue.</p>
Full article ">Figure 8
<p>Comparison between the attenuation value and attenuation coefficient of the coal gangue.</p>
Full article ">Figure 9
<p>PFC3D coal-waste slope model and monitoring arrangement.</p>
Full article ">Figure 10
<p>PFC3D fluid–solid coupling scouring scheme.</p>
Full article ">Figure 11
<p>Gully formation process. (A-Catchmentarea; B-Rainfallscouring area; C-Catchmentarea).</p>
Full article ">Figure 12
<p>Comparison of the gully simulated by the site and by the PFC. (<b>a</b>) comparison <a href="#applsci-13-05066-f001" class="html-fig">Figure 1</a>, (<b>b</b>) comparison <a href="#applsci-13-05066-f002" class="html-fig">Figure 2</a>.</p>
Full article ">Figure 13
<p>Comparison diagram of scouring depth curves.</p>
Full article ">Figure 14
<p>Comparison diagram of the final damage boundary.</p>
Full article ">Figure 15
<p>Displacement curves of monitoring points. (<b>a</b>) Y-direction horizontal displacement of the slope surface, (<b>b</b>) Y-direction horizontal displacement of the deep slope, (<b>c</b>) Z-direction horizontal displacement of the slope surface, and (<b>d</b>) Z-direction horizontal displacement of the deep slope.</p>
Full article ">Figure 15 Cont.
<p>Displacement curves of monitoring points. (<b>a</b>) Y-direction horizontal displacement of the slope surface, (<b>b</b>) Y-direction horizontal displacement of the deep slope, (<b>c</b>) Z-direction horizontal displacement of the slope surface, and (<b>d</b>) Z-direction horizontal displacement of the deep slope.</p>
Full article ">Figure 16
<p>Percentage of the peak displacement of the monitoring points. (<b>a</b>) Proportion of peak displacement in the Y-direction. (<b>b</b>) Proportion of peak displacement in the Z-direction.</p>
Full article ">Figure 17
<p>Movement trajectories of the monitoring particles.</p>
Full article ">Figure 18
<p>Gully distribution and accumulation mode. (<b>a</b>). Two gully directions; (<b>b</b>). Erosion trend-arc trend; (<b>c</b>). Erosion trend-alluvialfan trend.</p>
Full article ">Figure 19
<p>Real-time stress–strain curves. (<b>a</b>) stress, (<b>b</b>) strain.</p>
Full article ">Figure 20
<p>Peak stress and strain. (<b>a</b>) peak stress, (<b>b</b>) peak strain.</p>
Full article ">
20 pages, 5806 KiB  
Review
A Review of Mechanical Properties and Rockburst Investigation of Transversely Isotropic Rocks by Experimental Technique
by Xuefeng Si, Song Luo and Yong Luo
Materials 2023, 16(8), 3183; https://doi.org/10.3390/ma16083183 - 18 Apr 2023
Cited by 14 | Viewed by 2344
Abstract
Under complex geostress caused by long-term geological evolution, approximately parallel bedding structures are normally created in rocks due to sedimentation or metamorphism. This type of rock is known as transversely isotropic rock (TIR). Due to the existence of bedding planes, the mechanical properties [...] Read more.
Under complex geostress caused by long-term geological evolution, approximately parallel bedding structures are normally created in rocks due to sedimentation or metamorphism. This type of rock is known as transversely isotropic rock (TIR). Due to the existence of bedding planes, the mechanical properties of TIR are quite different from those of relatively homogeneous rocks. The purpose of this review is to discuss the research progress into the mechanical properties and failure characteristics of TIR and to explore the influence of the bedding structure on the rockburst characteristics of the surrounding rocks. First, the P-wave velocity characteristics of the TIR is summarized, followed by the mechanical properties (e.g., the uniaxial compressive strength, the triaxial compressive strength, and tensile strength) and the related failure characteristics of the TIR. The strength criteria of the TIR under triaxial compression are also summarized in this section. Second, the research progress of the rockburst tests on the TIR is reviewed. Finally, six prospects for the study of the transversely isotropic rock are presented: (1) measuring the Brazilian tensile strength of the TIR; (2) establishing the strength criteria for the TIR; (3) revealing the influence mechanism of the mineral particles between the bedding planes on rock failure from the microscopic point of view; (4) investigating the mechanical properties of the TIR in complex environments; (5) experimentally investigating the rockburst of the TIR under the stress path of “the three-dimensional high stress + internal unloading + dynamic disturbance”; and (6) studying the influence of the bedding angle, thickness, and number on the rockburst proneness of the TIR. Finally, some conclusions are summarized. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of two definitions of the bedding angle: (<b>a</b>,<b>b</b>) definitions of the bending angle in uniaxial compression; and (<b>c</b>,<b>d</b>) definitions of the bending angle in tensile test.</p>
Full article ">Figure 2
<p>The relationship between the UCS and bedding angle of TIR: (<b>a</b>) phyllite [<a href="#B1-materials-16-03183" class="html-bibr">1</a>,<a href="#B46-materials-16-03183" class="html-bibr">46</a>,<a href="#B47-materials-16-03183" class="html-bibr">47</a>,<a href="#B48-materials-16-03183" class="html-bibr">48</a>,<a href="#B49-materials-16-03183" class="html-bibr">49</a>], (<b>b</b>) schist [<a href="#B50-materials-16-03183" class="html-bibr">50</a>,<a href="#B51-materials-16-03183" class="html-bibr">51</a>,<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B54-materials-16-03183" class="html-bibr">54</a>], (<b>c</b>) shale [<a href="#B35-materials-16-03183" class="html-bibr">35</a>,<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B55-materials-16-03183" class="html-bibr">55</a>,<a href="#B56-materials-16-03183" class="html-bibr">56</a>,<a href="#B57-materials-16-03183" class="html-bibr">57</a>,<a href="#B58-materials-16-03183" class="html-bibr">58</a>], (<b>d</b>) sandstone [<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B59-materials-16-03183" class="html-bibr">59</a>,<a href="#B60-materials-16-03183" class="html-bibr">60</a>,<a href="#B61-materials-16-03183" class="html-bibr">61</a>,<a href="#B62-materials-16-03183" class="html-bibr">62</a>], (<b>e</b>) slate [<a href="#B46-materials-16-03183" class="html-bibr">46</a>,<a href="#B63-materials-16-03183" class="html-bibr">63</a>,<a href="#B64-materials-16-03183" class="html-bibr">64</a>], (<b>f</b>) gneiss [<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B65-materials-16-03183" class="html-bibr">65</a>], limestone [<a href="#B53-materials-16-03183" class="html-bibr">53</a>], orthoquartzie [<a href="#B46-materials-16-03183" class="html-bibr">46</a>], travertine [<a href="#B49-materials-16-03183" class="html-bibr">49</a>], and siltstone [<a href="#B59-materials-16-03183" class="html-bibr">59</a>].</p>
Full article ">Figure 2 Cont.
<p>The relationship between the UCS and bedding angle of TIR: (<b>a</b>) phyllite [<a href="#B1-materials-16-03183" class="html-bibr">1</a>,<a href="#B46-materials-16-03183" class="html-bibr">46</a>,<a href="#B47-materials-16-03183" class="html-bibr">47</a>,<a href="#B48-materials-16-03183" class="html-bibr">48</a>,<a href="#B49-materials-16-03183" class="html-bibr">49</a>], (<b>b</b>) schist [<a href="#B50-materials-16-03183" class="html-bibr">50</a>,<a href="#B51-materials-16-03183" class="html-bibr">51</a>,<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B54-materials-16-03183" class="html-bibr">54</a>], (<b>c</b>) shale [<a href="#B35-materials-16-03183" class="html-bibr">35</a>,<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B55-materials-16-03183" class="html-bibr">55</a>,<a href="#B56-materials-16-03183" class="html-bibr">56</a>,<a href="#B57-materials-16-03183" class="html-bibr">57</a>,<a href="#B58-materials-16-03183" class="html-bibr">58</a>], (<b>d</b>) sandstone [<a href="#B53-materials-16-03183" class="html-bibr">53</a>,<a href="#B59-materials-16-03183" class="html-bibr">59</a>,<a href="#B60-materials-16-03183" class="html-bibr">60</a>,<a href="#B61-materials-16-03183" class="html-bibr">61</a>,<a href="#B62-materials-16-03183" class="html-bibr">62</a>], (<b>e</b>) slate [<a href="#B46-materials-16-03183" class="html-bibr">46</a>,<a href="#B63-materials-16-03183" class="html-bibr">63</a>,<a href="#B64-materials-16-03183" class="html-bibr">64</a>], (<b>f</b>) gneiss [<a href="#B52-materials-16-03183" class="html-bibr">52</a>,<a href="#B65-materials-16-03183" class="html-bibr">65</a>], limestone [<a href="#B53-materials-16-03183" class="html-bibr">53</a>], orthoquartzie [<a href="#B46-materials-16-03183" class="html-bibr">46</a>], travertine [<a href="#B49-materials-16-03183" class="html-bibr">49</a>], and siltstone [<a href="#B59-materials-16-03183" class="html-bibr">59</a>].</p>
Full article ">Figure 3
<p>Stress–strain curves of phyllite specimens: (<b>a</b>) <span class="html-italic">β</span> = 0°, (<b>b</b>) <span class="html-italic">β</span> = 15°, (<b>c</b>) <span class="html-italic">β</span> = 30°, (<b>d</b>) <span class="html-italic">β</span> = 45°, (<b>e</b>) <span class="html-italic">β</span> = 60°, (<b>f</b>) <span class="html-italic">β</span> = 75°, and (<b>g</b>) <span class="html-italic">β</span> = 90° [<a href="#B1-materials-16-03183" class="html-bibr">1</a>].</p>
Full article ">Figure 3 Cont.
<p>Stress–strain curves of phyllite specimens: (<b>a</b>) <span class="html-italic">β</span> = 0°, (<b>b</b>) <span class="html-italic">β</span> = 15°, (<b>c</b>) <span class="html-italic">β</span> = 30°, (<b>d</b>) <span class="html-italic">β</span> = 45°, (<b>e</b>) <span class="html-italic">β</span> = 60°, (<b>f</b>) <span class="html-italic">β</span> = 75°, and (<b>g</b>) <span class="html-italic">β</span> = 90° [<a href="#B1-materials-16-03183" class="html-bibr">1</a>].</p>
Full article ">Figure 4
<p>Failure modes of phyllite specimens with different bedding angles [<a href="#B1-materials-16-03183" class="html-bibr">1</a>]: (<b>a</b>) 0°, (<b>b</b>) 15°, (<b>c</b>) 0° and 45°, and (<b>d</b>) 60°, 75° and 90°.</p>
Full article ">Figure 5
<p>The tensile strength of TIR [<a href="#B72-materials-16-03183" class="html-bibr">72</a>] (<span class="html-italic">σ</span><sub>3</sub> is the confining pressure, <span class="html-italic">σ</span><sub>t(d)</sub> is the variation in axial strength, <span class="html-italic">β<sub>f</sub></span> is the associated orientation of the failure plane, <span class="html-italic">d</span> is the weakness plane, <span class="html-italic">T<sub>w</sub></span> is the critical value of normal stress across the weakness plane, and <span class="html-italic">T<sub>i</sub></span> is the tensile strength of intact rock material; the red line represents the failure plane of the specimen).</p>
Full article ">Figure 6
<p>Brazilian test for an anisotropic material [<a href="#B77-materials-16-03183" class="html-bibr">77</a>].</p>
Full article ">Figure 7
<p>Variations in BTS with <span class="html-italic">θ</span> for sandstone types (<b>a</b>) 1, (<b>b</b>) 2, and (<b>c</b>) 3; (<b>d</b>) variations in average BTS with <span class="html-italic">θ</span> [<a href="#B82-materials-16-03183" class="html-bibr">82</a>].</p>
Full article ">Figure 8
<p>Four variation trends: (<b>a</b>) trend 1, (<b>b</b>) trend 2, (<b>c</b>) trend 3, and (<b>d</b>) trend 4 [<a href="#B84-materials-16-03183" class="html-bibr">84</a>].</p>
Full article ">Figure 9
<p>(<b>a</b>) Variation in strength with orientation of planes [<a href="#B46-materials-16-03183" class="html-bibr">46</a>], and (<b>b</b>) nonlinear strength characteristic of phyllite [<a href="#B46-materials-16-03183" class="html-bibr">46</a>,<a href="#B85-materials-16-03183" class="html-bibr">85</a>].</p>
Full article ">Figure 10
<p>The <span class="html-italic">PES</span> and rockburst proneness of phyllite under different bedding angles [<a href="#B1-materials-16-03183" class="html-bibr">1</a>].</p>
Full article ">Figure 11
<p>(<b>a</b>) Stress distribution [<a href="#B123-materials-16-03183" class="html-bibr">123</a>] and (<b>b</b>) transition between shear and tensile failure modes [<a href="#B120-materials-16-03183" class="html-bibr">120</a>] of the specimen in the Brazilian disc split test.</p>
Full article ">Figure 12
<p>Final failure modes of the specimens with five bedding angles under quasi-static conditions (TM: tensile fracture across discontinuities; SM: sliding across discontinuities; SD: sliding along the bedding; TD: tensile failure along discontinuities) [<a href="#B119-materials-16-03183" class="html-bibr">119</a>].</p>
Full article ">
17 pages, 2685 KiB  
Article
Study on the Damage Model of Non-Persistent Jointed Rock Mass under the Coupling of Freeze–Thaw and Shear
by Daxing Lei, Haixiang Hu, Yifan Chen, Hang Lin, Chaomei Zhang, Guangli Wang, Zhigang Lu and Yaoping Zhang
Materials 2023, 16(8), 3041; https://doi.org/10.3390/ma16083041 - 12 Apr 2023
Cited by 1 | Viewed by 1366
Abstract
Considering that a jointed rock mass in a cold area is often affected by periodic freeze–thaw cycles and shear failure, definitions for the mesoscopic and macroscopic damage to a jointed rock mass under the coupling of freeze–thaw and shear are proposed, and the [...] Read more.
Considering that a jointed rock mass in a cold area is often affected by periodic freeze–thaw cycles and shear failure, definitions for the mesoscopic and macroscopic damage to a jointed rock mass under the coupling of freeze–thaw and shear are proposed, and the damage mechanism is verified according to experimental results. The results show that: (1) the jointed rock specimens increase macro-joints and meso-defects, the mechanical properties deteriorate significantly under freeze–thaw cycles, and the damage degree becomes more and more significant with the increases in freeze–thaw cycles and joint persistency. (2) When the number of freeze–thaw cycles is constant, the total damage variable value gradually increases with the increase in joint persistency. The damage variable difference in specimens with different persistency is distinct, which is gradually reduced in the later cycles, indicating a weakening influence of persistency on the total damage variable. (3) The shear resistance of non-persistent jointed rock mass in a cold area is determined by the coupling effect of meso-damage and frost heaving macro-damage. The coupling damage variable can accurately describe the damage variation law of jointed rock mass under freeze–thaw cycles and shear load. Full article
Show Figures

Figure 1

Figure 1
<p>Macroscopic damage and deterioration of jointed rock masses under freeze–thaw shear in northeast China.</p>
Full article ">Figure 2
<p>Schematic diagram showing the force analysis of rock shear zone [<a href="#B45-materials-16-03041" class="html-bibr">45</a>].</p>
Full article ">Figure 3
<p>Complete rock specimen shear damage model evolution curve for the (<b>a</b>) comparison between the theoretical and experimental stress–strain and (<b>b</b>) meso shear damage theory [<a href="#B45-materials-16-03041" class="html-bibr">45</a>,<a href="#B48-materials-16-03041" class="html-bibr">48</a>,<a href="#B49-materials-16-03041" class="html-bibr">49</a>].</p>
Full article ">Figure 4
<p>(<b>a</b>) Joint sample damaged by freeze-thaw and shear coupling, (<b>b</b>) joint sample with shear damage, (<b>c</b>) intact rock samples with freeze-thaw damage, (<b>d</b>) intact rock sample with shear damage. Calculation method for the equivalent strain of jointed rock specimens.</p>
Full article ">Figure 5
<p>Damage evolution curve of (<b>a</b>) a jointed rock with persistency and (<b>b</b>) an intact rock with freeze–thaw cycles.</p>
Full article ">Figure 6
<p>Joint distribution form of freeze–thaw specimens with (<b>a</b>) persistency = 20%, (<b>b</b>) persistency = 30%, and (<b>c</b>) persistency = 40%.</p>
Full article ">Figure 7
<p>Comparison between the calculation and experimental results for the total damage variables in freeze–thaw shear of (<b>a</b>) persistency = 20% joint specimens, (<b>b</b>) persistency = 30% joint specimens, and (<b>c</b>) persistency = 40% joint specimens.</p>
Full article ">
15 pages, 3632 KiB  
Article
Mechanical Characteristics of an Open-Buried Double-Arch Tunnel during Construction
by Yu-Liang Lin, Ya-Lin Guo, Guo-Lin Yang and Pei-Ran Zhang
Appl. Sci. 2023, 13(6), 3891; https://doi.org/10.3390/app13063891 - 18 Mar 2023
Cited by 1 | Viewed by 1820
Abstract
The open excavation and concealed construction method is widely adopted for the construction of bias double-arch tunnels. However, the mechanical behavior of the tunnel during the whole construction period by using the open excavation and concealed construction method is not well understood, and [...] Read more.
The open excavation and concealed construction method is widely adopted for the construction of bias double-arch tunnels. However, the mechanical behavior of the tunnel during the whole construction period by using the open excavation and concealed construction method is not well understood, and the basis for construction organization and optimization is lacking. Based on an open-buried double-arch tunnel on Xiajuan Road, Changsha City, China, on-site monitoring was carried out in terms of the deformation of the steel arch in the primary lining, the stress of reinforcement in the secondary lining, and the deformation of the surrounding rock during the construction process. The correlation between the vault settlement rate and the steel arch strain was analyzed. The results show that the maximum vault settlement and settling rate of the left and right caverns occur at different locations due to different supporting conditions. The peripheral displacement experiences a process of convergence inward and extension outward. The compressive steel stress in the secondary lining of the right cavern is greater than that in the left cavern, except for the points at the arch waist. The backfill above the left cavern reduces the loading on the lining of the right cavern, but it increases the loading on the left cavern. The bias effect of the open-buried double-arch tunnel is well controlled and balanced when the open excavation and concealed construction method is adopted. Full article
Show Figures

Figure 1

Figure 1
<p>Location and longitudinal and cross profiles of the double-arch tunnel on Xiajuan Road. (<b>a</b>) Front view of tunnel; (<b>b</b>) Longitudinal geological profile; (<b>c</b>) Project location map; (<b>d</b>) Monitoring section K2 + 097.</p>
Full article ">Figure 2
<p>Schematic diagram of the construction process of the open-buried double-arch and bias tunnel.</p>
Full article ">Figure 3
<p>Measurement point layout.</p>
Full article ">Figure 4
<p>Diagram of field components installation: (<b>a</b>) Strain gauge installation in primary lining; (<b>b</b>) the strain gauge and stress gauge installation in secondary lining.</p>
Full article ">Figure 5
<p>Strain distribution of the steel arch versus time. (<b>a</b>) Left cavern; (<b>b</b>) right cavern.</p>
Full article ">Figure 6
<p>Development of the settlement and sinking rate of the vault. (<b>a</b>) Vault settlement; (<b>b</b>) the sinking rate of vault settlement.</p>
Full article ">Figure 7
<p>Peripheral displacement and displacement rate versus time. (<b>a</b>) Peripheral displacement; (<b>b</b>) peripheral displacement rate.</p>
Full article ">Figure 8
<p>Correlation analysis between the strain and the sinking rate of the primary lining. (<b>a</b>) Left cavern; (<b>b</b>) right cavern.</p>
Full article ">Figure 9
<p>Steel stress of the secondary lining versus time. (<b>a</b>) Left cavern; (<b>b</b>) right cavern.</p>
Full article ">
22 pages, 10888 KiB  
Article
Study on Staged Damage Behaviors of Rock-like Materials with Different Brittleness Degrees Based on Multiple Parameters
by Tong Jiang, Li Wan, Wenxue Wang, Chao Xu, Chen Liu, Fanke Meng, Yuan Cui and Longfei Li
Materials 2023, 16(6), 2334; https://doi.org/10.3390/ma16062334 - 14 Mar 2023
Cited by 4 | Viewed by 1507
Abstract
Understanding the brittle fracture behavior of rock is crucial for engineering and Earth science. In this paper, based on acoustic emission (AE) and laser Doppler vibration (LDV) monitoring technology, the staged damage behaviors of rock-like materials with different brittleness degrees under uniaxial compression [...] Read more.
Understanding the brittle fracture behavior of rock is crucial for engineering and Earth science. In this paper, based on acoustic emission (AE) and laser Doppler vibration (LDV) monitoring technology, the staged damage behaviors of rock-like materials with different brittleness degrees under uniaxial compression are studied via multiple parameters. The results show that the brittleness degree determines the fracture mode. As the specimen’s brittleness degree increases, the tensile failure increases and shear failure decreases. AE activity is enhanced at the crack damage point. With an increasing specimen brittleness degree, different instability precursor information is shown during the unstable crack growth stage: the AE b value changes from the fluctuating to continuously decreasing state, and the natural frequency changes from the stable fluctuation to upward fluctuation state. The AE b value near the stress drop is the smallest, and it decreases with an increasing brittleness degree. The natural frequency reduction indicates the rock-like fracture. The natural frequency is a symbolic index that reflects staged damage characteristics and predicts the amount of energy released by brittle failure. These findings provide guidelines for rock stability monitoring and provide support for better responses to stability evaluations of rock slopes, rock collapses, and tunnel surrounding rock in engineering. Full article
Show Figures

Figure 1

Figure 1
<p>Photomicrographs of the tested specimen. Legends: Q stands for quartz, CM for clay mineral, Cc for calcite, F for feldspar.</p>
Full article ">Figure 2
<p>Stress–strain curve and failure mode of the argillaceous calcareous siltstone and the rock-like material.</p>
Full article ">Figure 3
<p>Specimen preparation process: (<b>A</b>) weighing; (<b>B</b>) dry material mixing; (<b>C</b>) water weighing; (<b>D</b>) gypsum retarder preparation; (<b>E</b>) wet material mixing; (<b>F</b>) mold preparation; (<b>G</b>) press molding with a jack; (<b>H</b>) grinding and standing; and (<b>I</b>) specimen maintenance.</p>
Full article ">Figure 4
<p>Testing site: 1—the AE system; 2—the AE sensor; 3—the LDV measurement point; and 4—the LDV.</p>
Full article ">Figure 5
<p>Crack volumetric strain model [<a href="#B21-materials-16-02334" class="html-bibr">21</a>].</p>
Full article ">Figure 6
<p>Crack volumetric strain curves, volumetric strain curves, and stress–strain curves of specimens with different ratios of aggregates to binders: (<b>a</b>) 1:1; (<b>b</b>) 4:1; and (<b>c</b>) 7:1.</p>
Full article ">Figure 7
<p>Relationship between the brittleness index (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>B</mi> </mrow> <mrow> <mi mathvariant="normal">i</mi> </mrow> </msub> </mrow> </semantics></math>) and the ratios of the aggregates to binders.</p>
Full article ">Figure 8
<p>Variation of the AE parameters of the specimens with different brittleness indexes (4.16, 3.36, and 2.25) during different failure stages: (<b>a</b>,<b>c</b>,<b>e</b>) the ring count rate and accumulative ringing count and (<b>b</b>,<b>d</b>,<b>f</b>) the energy rate and accumulative energy.</p>
Full article ">Figure 9
<p>Relationship between AE released at the failure of the specimen and brittleness index.</p>
Full article ">Figure 10
<p>Fracture mode classification criterion.</p>
Full article ">Figure 11
<p>Distribution of the AE RA-AF parameters for the specimen with a brittleness index of 4.16: (<b>a</b>) scatter diagram; and (<b>b</b>) density nephogram.</p>
Full article ">Figure 12
<p>Distribution of the AE RA-AF parameters for the specimen with a brittleness index of 3.36: (<b>a</b>) scatter diagram; and (<b>b</b>) density nephogram.</p>
Full article ">Figure 13
<p>Distribution of the AE RA-AF parameters for the specimen with a brittleness index of 2.25: (<b>a</b>) scatter diagram; and (<b>b</b>) density nephogram.</p>
Full article ">Figure 14
<p>Relationship between the stress, the <span class="html-italic">b</span> value, and the strain for brittleness indexes of (<b>a</b>) 4.16, (<b>b</b>) 3.36, and (<b>c</b>) 2.25.</p>
Full article ">Figure 15
<p>Relationship between the <span class="html-italic">b</span> value and the brittleness index.</p>
Full article ">Figure 16
<p>Acquisition of the natural frequency: (<b>a</b>) time-domain illustration and (<b>b</b>) frequency-domain illustration after a fast Fourier transform of the time-domain diagram.</p>
Full article ">Figure 17
<p>Axial stress, natural frequency, and strain curves for brittleness index of (<b>a</b>) 4.16, (<b>b</b>) 3.36, and (<b>c</b>) 2.25.</p>
Full article ">Figure 18
<p>Law of natural frequency during the stable crack growth stage: (<b>a</b>) linear fitting of frequency and (<b>b</b>) linear fitting of the rise slope of the frequency and brittleness index.</p>
Full article ">Figure 19
<p>Relationship between the natural frequency decline slope at the stress drop and the brittleness index.</p>
Full article ">Figure 20
<p>Variation analysis of the natural frequency: (<b>a</b>) natural frequency curves of specimens with different brittleness indexes and (<b>b</b>) relationship between the average natural frequency during different stages and the brittleness index.</p>
Full article ">Figure 21
<p>Analysis of the average natural frequency increment and energy: (<b>a</b>) area formed by the natural frequency curve and the strain at peak strength of specimens with different brittleness indexes; and (<b>b</b>) relationship between <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mo>Δ</mo> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> </mrow> <mo>¯</mo> </mover> </mrow> </semantics></math>, energy and the brittleness index.</p>
Full article ">Figure 22
<p>Relationship between the release of energy during failure and <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mo>Δ</mo> <msub> <mrow> <mi>f</mi> </mrow> <mrow> <mi>a</mi> </mrow> </msub> </mrow> <mo>¯</mo> </mover> </mrow> </semantics></math>.</p>
Full article ">
20 pages, 36520 KiB  
Article
An Innovative Method to Analyze the Hydraulic Fracture Reopening Pressure of Hot Dry Rock
by Deng-Deng Zhuang, Tu-Bing Yin, Zong-Xian Zhang, Adeyemi Aladejare, You Wu and Yang Qiao
Materials 2023, 16(3), 1118; https://doi.org/10.3390/ma16031118 - 28 Jan 2023
Viewed by 1710
Abstract
This paper focuses on a new test method and theoretical model for measuring and evaluating the reopening pressure during hot dry rock hydraulic fracturing. Firstly, rock blocks of four lithologies were collected from the hot dry rock strata. Hydraulic fracturing tests at high [...] Read more.
This paper focuses on a new test method and theoretical model for measuring and evaluating the reopening pressure during hot dry rock hydraulic fracturing. Firstly, rock blocks of four lithologies were collected from the hot dry rock strata. Hydraulic fracturing tests at high temperatures in real-time were conducted using drilled cubic specimens and drilled cubic specimens with a pre-crack. Breakdown pressure, reopening pressure, and fracture toughness were measured, respectively. In addition, Brazilian splitting tests at high temperatures in real-time were performed using Brazilian disc specimens to measure tensile strength. Secondly, an empirical equation for evaluating the reopening pressure during hot dry rock secondary fracturing was developed based on fracture mechanics and hydraulic fracturing theory. Third, the values calculated by the new equation, considering breakdown pressure, fracture toughness, and tensile strength, were compared to the values determined by the classical equation and to measurement results. It was found that the new equation predicted closer reopening pressure to the measurement results, regardless of the lithology of the hot dry rock. Moreover, with increasing temperature in the specimens, the error between the value calculated by the new equation and the measurement value remained low. In contrast, the difference between the classical equation predictions and the measurement results was widened. In addition, the reopening pressure was positively correlated with tensile strength and fracture toughness. Variations in lithology and temperature affected tensile strength and fracture toughness, which then changed the hot dry rock reopening pressure. Full article
Show Figures

Figure 1

Figure 1
<p>Location diagram of the rock specimens used in this study.</p>
Full article ">Figure 2
<p>Photos and matrix surfaces of Brazilian disc specimens of the lithologies G1, G2, G3, and S.</p>
Full article ">Figure 3
<p>Micrographs of G1, G2, G3, and S lithological specimens by a single-polarization microscope.</p>
Full article ">Figure 4
<p>X-ray diffraction (XRD) patterns of rock specimen: (<b>a</b>) G1 specimen; (<b>b</b>) G2 specimen; (<b>c</b>) G3 specimen; (<b>d</b>) S specimen.</p>
Full article ">Figure 5
<p>Specimen preparation: (<b>a</b>) HFS specimen for hydraulic fracturing tests; (<b>b</b>) SFS specimen for secondary fracturing tests; (<b>c</b>) BSS specimens for Brazilian splitting tests.</p>
Full article ">Figure 6
<p>Real-time high temperature true-triaxial hydraulic fracturing platform: (<b>a</b>) the heating system; (<b>b</b>) the true triaxial loading system; (<b>c</b>) the water injection and sealing system; (<b>d</b>) the computer monitoring system.</p>
Full article ">Figure 7
<p>Main hydraulic fracturing procedures: (<b>a</b>) HFS or SFS specimen was placed in the fracturing chamber; (<b>b</b>) specimen was heated in the furnace; (<b>c</b>) three directions confining stresses were applied; (<b>d</b>) specimen fractured by water injection.</p>
Full article ">Figure 8
<p>Brazilian splitting test procedures.</p>
Full article ">Figure 9
<p>Photograph of HFS specimens of G1, G2, G3, and S lithologies after fracturing.</p>
Full article ">Figure 10
<p>Photograph of SFS specimens of G1, G2, G3, and S lithologies after fracturing.</p>
Full article ">Figure 11
<p>Fracturing curves for HFS and SFS specimens of four lithologies at different temperatures.</p>
Full article ">Figure 12
<p>Variation of fracture toughness with specimen lithology and temperature.</p>
Full article ">Figure 13
<p>Variation of tensile strength with specimen lithology and temperature.</p>
Full article ">Figure 14
<p>Superposition of four kinds of fracture type.</p>
Full article ">Figure 15
<p>Variation of measured and calculated reopening pressure with temperature for all lithological samples.</p>
Full article ">Figure 16
<p>Variation of measured and calculated tensile strength with temperature for all lithological samples.</p>
Full article ">Figure 17
<p>Variation of measured reopening pressure with specimen lithology and temperature.</p>
Full article ">Figure 18
<p>Variation of measured reopening pressure with fracture toughness and tensile strength.</p>
Full article ">
11 pages, 5642 KiB  
Article
An Experimental Study of the Relation between Mode I Fracture Toughness, KIc, and Critical Energy Release Rate, GIc
by Yang Qiao, Zong-Xian Zhang and Sheng Zhang
Materials 2023, 16(3), 1056; https://doi.org/10.3390/ma16031056 - 25 Jan 2023
Cited by 6 | Viewed by 2649
Abstract
The construction of the relation between the critical energy release rate, GIc, and the mode I fracture toughness, KIc, is of great significance for understanding the fracture mechanism and facilitating its application in engineering. In this study, [...] Read more.
The construction of the relation between the critical energy release rate, GIc, and the mode I fracture toughness, KIc, is of great significance for understanding the fracture mechanism and facilitating its application in engineering. In this study, fracture experiments using NSCB and CCCD specimens were conducted. The effects of specimen sizes, loading rate and lithology on the relation between GIc and KIc were studied. GIc was calculated by integrating the load–displacement curve according to Irwin’s approach. Based on the measured KIc and GIc of the rock specimens, a relation between GIc and KIc was found to be different from the classical formula under linear elasticity. It was found that both specimen size and loading rate do not influence this relation. Full article
Show Figures

Figure 1

Figure 1
<p>Configuration of rock specimens and testing machine. (<b>a</b>) Top: notched semi-circular bending (NSCB) specimens; (<b>b</b>) bottom: center-cracked circular disk (CCCD) specimens.</p>
Full article ">Figure 2
<p>Load–displacement curve (the letters represent the group and the following number is the diameter of the specimen).</p>
Full article ">Figure 2 Cont.
<p>Load–displacement curve (the letters represent the group and the following number is the diameter of the specimen).</p>
Full article ">Figure 3
<p>Relation between <math display="inline"><semantics> <mrow> <msub> <mi>G</mi> <mrow> <mi>I</mi> <mi>c</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msubsup> <mi>K</mi> <mrow> <mi>I</mi> <mi>c</mi> </mrow> <mn>2</mn> </msubsup> <mo>/</mo> <mi>E</mi> </mrow> </semantics></math>.</p>
Full article ">Figure 4
<p>Load–displacement curve of limestone.</p>
Full article ">Figure 5
<p>(<b>a</b>) Regression equation and data for <span class="html-italic">Φ</span> = 150 mm. (<b>b</b>) Regression equation and data for <span class="html-italic">Φ</span> = 100 mm. (<b>c</b>) Regression equation and data for <span class="html-italic">Φ =</span> 75 mm. (<b>d</b>) Regression equation and data for <span class="html-italic">Φ</span> = 50 mm. (<b>e</b>) Regression equation and data for <span class="html-italic">Φ</span> = 30 mm.</p>
Full article ">Figure 5 Cont.
<p>(<b>a</b>) Regression equation and data for <span class="html-italic">Φ</span> = 150 mm. (<b>b</b>) Regression equation and data for <span class="html-italic">Φ</span> = 100 mm. (<b>c</b>) Regression equation and data for <span class="html-italic">Φ =</span> 75 mm. (<b>d</b>) Regression equation and data for <span class="html-italic">Φ</span> = 50 mm. (<b>e</b>) Regression equation and data for <span class="html-italic">Φ</span> = 30 mm.</p>
Full article ">Figure 6
<p>Regression equation and data of sandstone.</p>
Full article ">
17 pages, 20584 KiB  
Article
Energy Evolution and Damage Characteristics of Rock Materials under Different Cyclic Loading and Unloading Paths
by Bing Sun, Haowei Yang, Junwei Fan, Xiling Liu and Sheng Zeng
Buildings 2023, 13(1), 238; https://doi.org/10.3390/buildings13010238 - 14 Jan 2023
Cited by 4 | Viewed by 2254
Abstract
In order to study the deformation and failure characteristics of rocks under different cyclic loading and unloading paths, three stress path tests were conducted, and acoustic emission (AE) monitoring was conducted simultaneously. The mechanical characteristics and AE characteristics under different stress paths were [...] Read more.
In order to study the deformation and failure characteristics of rocks under different cyclic loading and unloading paths, three stress path tests were conducted, and acoustic emission (AE) monitoring was conducted simultaneously. The mechanical characteristics and AE characteristics under different stress paths were analyzed, and the influences of the different stress paths on the energy dissipation and deformation damage were investigated. The law of energy evolution considering viscoelasticity under different stress paths was obtained. The concept of ultimate damage energy and its calculation method was proposed. The results show that the “hardening effect” of sandstone and granite under the constant lower limit (CLLCL) is the most significant in maximizing the mechanical property. The CLLCL imparts a stronger elastic property to rocks than the variable lower limit (VLLCL) does, while the VLLCL causes more damage to rocks than the CLLCL. A significant linear relationship between the proportion of damage energy and the proportion of elastic energy was discovered. Based on this linear relationship, the ultimate damage energy can be calculated for sandstone and granite. The evolution of the damage variable based on damage energy was compatible with the real damage condition, which validates the ultimate damage energy calculation method. The research results lay a theoretical foundation for the design and construction of geotechnical engineering. Full article
Show Figures

Figure 1

Figure 1
<p>Rock specimens. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 2
<p>Schematic diagram of testing.</p>
Full article ">Figure 3
<p>The stress path of constant lower limit cyclic loading and unloading (CLLCL).</p>
Full article ">Figure 4
<p>The stress path of variable lower limit cyclic loading and unloading (VLLCL).</p>
Full article ">Figure 5
<p>Stress–strain curves under CLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 6
<p>Stress–strain curves under VLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 7
<p>The calculation method of modulus.</p>
Full article ">Figure 8
<p>The relationship between the elastic modulus and the number of cycles. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 9
<p>The AE energy evolution and location under UC. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 10
<p>The AE energy and location evolution under CLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 11
<p>The AE energy evolution and location under VLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 12
<p>Diagram of energy calculation.</p>
Full article ">Figure 13
<p>Rock energy evolution under CLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 14
<p>Rock energy evolution under VLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 15
<p>The evolution of rock energy proportion under CLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 16
<p>The evolution of rock energy proportion under VLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 17
<p>Fitting between the proportion of damage energy and proportion of elastic energy under CLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 18
<p>Fitting between the proportion of damage energy and proportion of elastic energy under VLLCL. (<b>a</b>) Sandstone; (<b>b</b>) granite.</p>
Full article ">Figure 19
<p>The damage evolution under different stress paths.</p>
Full article ">
23 pages, 6820 KiB  
Article
Apparent Deterioration Law and Shear Failure Mode of Rock–Mortar Interface Based on Topography-Sensing Technology
by Linglin Xie, Wenyu Tang, Hang Lin, Fan Lei, Yifan Chen, Yixian Wang and Yanlin Zhao
Materials 2023, 16(2), 763; https://doi.org/10.3390/ma16020763 - 12 Jan 2023
Viewed by 1556
Abstract
As an advanced spatial technology, topography-sensing technology is comprehensive, macroscopic, and intuitive. It shows unique advantages for rock structure interpretation and has important guiding significance for the research of the shear performances of rock–mortar interface under cyclic load in rock mass engineering. In [...] Read more.
As an advanced spatial technology, topography-sensing technology is comprehensive, macroscopic, and intuitive. It shows unique advantages for rock structure interpretation and has important guiding significance for the research of the shear performances of rock–mortar interface under cyclic load in rock mass engineering. In this paper, cyclic shearing tests combined with the shear surface topography-sensing technology are employed to investigate the evolution characteristics of the interface morphology and the strength deterioration of the rock–mortar interface. Primarily, mortar and three types of rocks are used to prepare different rock–mortar interfaces, which are then applied to cyclic shear loading under two constant normal stresses. Subsequently, the shear strength degradation and dilatancy characteristics of rock–mortar interfaces with varying shear times are discussed. In addition, on the basis of the non-contact three-dimensional topography-sensing technology, the apparent three-dimensional point–cloud coordinate information of rock–mortar interface before and after each shear loading is obtained, and the apparent three-dimensional topography parameters of rock–mortar interface are calculated, according to which the influences of normal stress and lithology on the topography of interface subjected to cyclic shearing loading are analyzed. Full article
Show Figures

Figure 1

Figure 1
<p>Landslide in engineering.</p>
Full article ">Figure 2
<p>Interface between rock-socketed pile and bedrock in high-speed railway.</p>
Full article ">Figure 3
<p>The components of interface topography-sensing system.</p>
Full article ">Figure 4
<p>The calibration of topography-sensing system.</p>
Full article ">Figure 5
<p>ZW100 multifunctional rock direct shear instrument.</p>
Full article ">Figure 6
<p>Rock–mortar interface preparation flow.</p>
Full article ">Figure 7
<p>The shear stress vs shear displacement curves of sample CD-1 in each shearing.</p>
Full article ">Figure 8
<p>Normalized relationship between shear strength and shear times. (<b>a</b>) Normal stress = 4 MPa; (<b>b</b>) Normal stress = 2 MPa.</p>
Full article ">Figure 9
<p>The relationship between normal displacement and shear displacement.</p>
Full article ">Figure 10
<p>The relationship between shear displacement, dilatancy angle, and shear stress. (<b>a</b>) First shearing; (<b>b</b>) Second shearing; (<b>c</b>) Third shearing.</p>
Full article ">Figure 11
<p>Relationship between shear times and peak dilatancy angle <span class="html-italic">d<sub>n</sub></span>.</p>
Full article ">Figure 12
<p>The three-dimensional scanning of CD-3 interface for each shearing. (<b>a</b>) Before shearing; (<b>a</b>) Before shearing; (<b>c</b>) Second shearing; (<b>d</b>) Third shearing.</p>
Full article ">Figure 13
<p>Failure surfaces of AD-1 and AD-2 after the first shearing.</p>
Full article ">Figure 14
<p>Failure surfaces of CD-3 after the first shearing.</p>
Full article ">Figure 15
<p>Relation between slope root mean square and shear strength.</p>
Full article ">Figure 16
<p>Contour map of CD-3 in cyclic shearing. (<b>a</b>) Before test; (<b>b</b>) First shearing; (<b>c</b>) Second shearing; (<b>d</b>) Third shearing.</p>
Full article ">Figure 17
<p>Abbott–Firestone curve of CD-3 in cyclic shearing. (<b>a</b>) Before test; (<b>b</b>) First shearing; (<b>c</b>) Second shearing; (<b>d</b>) Third shearing.</p>
Full article ">
16 pages, 9068 KiB  
Article
Study on Mechanical Properties of Ring Sandstone Specimen under Temperature and Water Coupling Dynamic Compression
by Qi Ping, Qi Gao and Shiwei Wu
Minerals 2023, 13(1), 119; https://doi.org/10.3390/min13010119 - 12 Jan 2023
Cited by 2 | Viewed by 2016
Abstract
The excavation of hard rock roadways in coal mines is often in the environment of underground water and high ground temperature, and it is easy to be affected by the dynamic load, which leads to roadway destruction and increases the difficulty of roadway [...] Read more.
The excavation of hard rock roadways in coal mines is often in the environment of underground water and high ground temperature, and it is easy to be affected by the dynamic load, which leads to roadway destruction and increases the difficulty of roadway support. The ring sandstone specimens with different inner diameters (0~25 mm) were treated with temperature and water coupled, and the dynamic compression test was produced by the Hopkinson pressure rod device (SHPB). The experimental results indicate that the coupling effect of temperature and water reduces the dynamic performance of sandstone specimens. XRD test results showed that the composition of sandstone specimens did not change before and after warm water coupling, and no new substances were found. Dynamic properties of ring sandstone specimens with different inner diameters weaken with the increase in inner diameters. With the increasing inner diameter of ring sandstone specimens, the energy dissipation per unit volume increases the dynamic compressive strength decreases, and the degree of breakage increases. Fracture morphology, average strain rate, and dynamic peak strain of ring sandstone specimens increase with inner diameter. Full article
Show Figures

Figure 1

Figure 1
<p>Processed annular sandstone specimen.</p>
Full article ">Figure 2
<p>Water bath box.</p>
Full article ">Figure 3
<p>Mass growth rate changes with annular diameter change.</p>
Full article ">Figure 4
<p>Volume growth rate changes with annular diameter change.</p>
Full article ">Figure 5
<p>The density reduction rate varies with annular diameter change.</p>
Full article ">Figure 6
<p>XRD pattern of sandstone specimen.</p>
Full article ">Figure 7
<p>SHPB test device.</p>
Full article ">Figure 8
<p>Dynamic stress-strain curve of sandstone specimen.</p>
Full article ">Figure 9
<p>The relationship between dynamic compressive strength and annular diameter change.</p>
Full article ">Figure 10
<p>Diagram of the dynamic peak strain and annular diameter change.</p>
Full article ">Figure 11
<p>Diagram of average strain rate and annular diameter change.</p>
Full article ">Figure 12
<p>Relationship between dynamic elastic modulus and annular diameter change.</p>
Full article ">Figure 13
<p>SEM test photos of sandstone specimens.</p>
Full article ">Figure 14
<p>Fracture morphology of specimens with temperature and water coupling.</p>
Full article ">Figure 15
<p>Fracture morphology of specimens without temperature and water coupling.</p>
Full article ">Figure 16
<p>Energy proportion diagram.</p>
Full article ">Figure 17
<p>Energy dissipation per unit volume diagram.</p>
Full article ">
18 pages, 4066 KiB  
Article
Fracture Closure Empirical Model and Theoretical Damage Model of Rock under Compression
by Yifan Chen, Hang Lin, Shijie Xie, Rihong Cao, Shuwei Sun, Wenhua Zha, Yixian Wang, Yanlin Zhao and Huihua Hu
Materials 2023, 16(2), 589; https://doi.org/10.3390/ma16020589 - 7 Jan 2023
Cited by 7 | Viewed by 1806
Abstract
The rock or rock mass in engineering often contains joints, fractures, voids, and other defects, which are the root cause of local or overall failure. In response to most of the current constitutive models that fail to simulate the nonlinear fracture compaction deformation [...] Read more.
The rock or rock mass in engineering often contains joints, fractures, voids, and other defects, which are the root cause of local or overall failure. In response to most of the current constitutive models that fail to simulate the nonlinear fracture compaction deformation in the whole process of rock failure, especially brittle rocks, a piecewise constitutive model was proposed to represent the global constitutive relation of rocks in this study, which was composed of the fracture compaction empirical model and the damage statistical constitutive model. The fracture empirical compaction model was determined by fitting the expressions of fracture closure curves of various rocks, while the rock damage evolution equation was derived underpinned by the fracture growth. According to the effective stress concept and strain equivalence hypothesis, the rock damage constitutive model was deduced. The model parameters of the fracture compaction empirical model and damage statistical constitutive model were all calculated by the geometrical characteristics of the global axial stress–strain curve to guarantee that the models are continuous and smooth at the curve intersection, which is also simple and ready to program. Finally, the uniaxial compression test data and the triaxial compression test data of different rocks in previous studies were employed to validate the models, and the determination coefficient was used to measure the accuracy. The results showed great consistency between the model curves and test data, especially in the pre-peak stage. Full article
Show Figures

Figure 1

Figure 1
<p>Common rock engineering.</p>
Full article ">Figure 2
<p>The highway geological landslide.</p>
Full article ">Figure 3
<p>The typical rock failure process.</p>
Full article ">Figure 4
<p>The deformation characteristics of fracture closure curve.</p>
Full article ">Figure 5
<p>The variation law of <span class="html-italic">k</span>. (<b>a</b>) Eberhardt et al. [<a href="#B49-materials-16-00589" class="html-bibr">49</a>]; (<b>b</b>) Gao et al. [<a href="#B52-materials-16-00589" class="html-bibr">52</a>]; (<b>c</b>) Chang et al. [<a href="#B53-materials-16-00589" class="html-bibr">53</a>]; (<b>d</b>) Chang et al. [<a href="#B53-materials-16-00589" class="html-bibr">53</a>].</p>
Full article ">Figure 6
<p>The strain equivalence hypothesis diagram.</p>
Full article ">Figure 7
<p>Stress–strain curve for the new coordinate system.</p>
Full article ">Figure 8
<p>The comparison between the uniaxial test data and the model curve of sandstone.</p>
Full article ">Figure 9
<p>The comparison between uniaxial test data and model curves of various rocks. (<b>a</b>) Beishan Granite; (<b>b</b>) 130 m LdB Granite; (<b>c</b>) Hwangdeung Granite; (<b>d</b>) Yeosan Marble.</p>
Full article ">Figure 10
<p>The comparison between partial triaxial test data and model curves of Jinping Marble. (<b>a</b>) Confining stress = 5 MPa; (<b>b</b>) confining stress = 10 MPa; (<b>c</b>) confining stress = 30 MPa.</p>
Full article ">Figure 11
<p>The comparison between partial triaxial test data and model curves of fine sandstone. (<b>a</b>) Confining stress = 1 MPa; (<b>b</b>) confining stress = 2 MPa; (<b>c</b>) confining stress = 3 MPa.</p>
Full article ">Figure 12
<p>The comparison between partial triaxial test data and model curves of coarse sandstone. (<b>a</b>) Confining stress = 1 MPa; (<b>b</b>) confining stress = 2 MPa; (<b>c</b>) confining stress = 3 MPa.</p>
Full article ">
20 pages, 4681 KiB  
Review
Research Status and Prospects for the Utilization of Lead–Zinc Tailings as Building Materials
by Rui Li, Ziyi Yin and Hang Lin
Buildings 2023, 13(1), 150; https://doi.org/10.3390/buildings13010150 - 6 Jan 2023
Cited by 15 | Viewed by 3176
Abstract
Lead–zinc tailings are the typical solid wastes in mines with high yield and low utilization rates in some countries at present. They are mainly stockpiled in tailings reservoirs, occupying massive land resources and threatening the health of the environment. One of the advantages [...] Read more.
Lead–zinc tailings are the typical solid wastes in mines with high yield and low utilization rates in some countries at present. They are mainly stockpiled in tailings reservoirs, occupying massive land resources and threatening the health of the environment. One of the advantages of building material production in sustainability is the ability to utilize large amounts of industrial solid wastes, and the use of lead–zinc tailings in building materials is an effective way to meet the dual needs of environmental protection and economic development. This paper reviews the progress of utilizing lead–zinc tailings as building materials and mainly summarizes the status of lead–zinc tailings in cement, geopolymer, concrete, building brick, and foam ceramic. According to previous research, lead–zinc tailings contain large amounts of silica–alumina oxide, which can be used in the production of cement clinker. The addition of lead–zinc tailings to the sintered material can reduce the sintering temperature. The active components contained in lead–zinc tailings can be used in concrete instead of cement or in the preparation of geopolymers. Meanwhile, lead–zinc tailings can also be used as a fine aggregate. However, there are few studies on the durability of building materials with lead–zinc tailings. Additionally, most of the research results of building materials are in the laboratory stage, which are difficult to be promoted. In view of these problems, corresponding suggestions and prospects are given in the end in order to provide a reference for the research on the utilization of lead–zinc tailings. Full article
Show Figures

Figure 1

Figure 1
<p>Adverse effects of tailings reservoirs on environment and human society.</p>
Full article ">Figure 2
<p>Utilization ways of lead–zinc tailings.</p>
Full article ">Figure 3
<p>Solidification rate and leaching concentration of Zn<sup>2+</sup> (<b>a</b>), Pb<sup>2+</sup> (<b>b</b>), and Cd<sup>2+</sup> (<b>c</b>) in geopolymers with different tailings contents [<a href="#B85-buildings-13-00150" class="html-bibr">85</a>].</p>
Full article ">Figure 4
<p>Relationship between grinding time of lead–zinc tailings and compressive strength of cement mortar [<a href="#B95-buildings-13-00150" class="html-bibr">95</a>].</p>
Full article ">Figure 5
<p>Relationship between grinding time and particle size of lead–zinc tailings [<a href="#B95-buildings-13-00150" class="html-bibr">95</a>].</p>
Full article ">Figure 6
<p>SEM photos of lead–zinc tailings after heat treatment at different temperatures [<a href="#B101-buildings-13-00150" class="html-bibr">101</a>]: (<b>a</b>) raw state; (<b>b</b>) 800 °C; (<b>c</b>) 1000 °C; (<b>d</b>) 1200 °C.</p>
Full article ">Figure 7
<p>Autogenous shrinkage of UHPC with different contents of lead–zinc tailings [<a href="#B106-buildings-13-00150" class="html-bibr">106</a>].</p>
Full article ">Figure 8
<p>Effects of lead–zinc tailings content on the conductivity of UHPC [<a href="#B106-buildings-13-00150" class="html-bibr">106</a>].</p>
Full article ">Figure 9
<p>Compressive strength comparison of C25 concrete with different contents of lead–zinc tailings [<a href="#B108-buildings-13-00150" class="html-bibr">108</a>].</p>
Full article ">Figure 10
<p>Relationship between γ-ray absorption coefficient of concrete and different contents of lead–zinc tailings [<a href="#B111-buildings-13-00150" class="html-bibr">111</a>].</p>
Full article ">Figure 11
<p>SEM photos of ceramics with different contents of lead–zinc tailings [<a href="#B124-buildings-13-00150" class="html-bibr">124</a>]: (<b>a</b>) 6 wt.%; (<b>b</b>) 12 wt.%; (<b>c</b>) 18 wt.%; (<b>d</b>) 24 wt.%.</p>
Full article ">
14 pages, 6572 KiB  
Article
Mechanism and Application of Layered Grouting Reinforcement for Fractured Coal and Rock Roadway
by Ze Liao and Tao Feng
Appl. Sci. 2023, 13(2), 724; https://doi.org/10.3390/app13020724 - 4 Jan 2023
Cited by 6 | Viewed by 1583
Abstract
This paper takes the ZF3806 working face of Shuiliandong Coal Mine in Binxian County, Shaanxi Province as the engineering background. Aiming at the problems of the development of surrounding rock cracks and roof breakage encountered in the process of roadway excavation and support [...] Read more.
This paper takes the ZF3806 working face of Shuiliandong Coal Mine in Binxian County, Shaanxi Province as the engineering background. Aiming at the problems of the development of surrounding rock cracks and roof breakage encountered in the process of roadway excavation and support and based on the composite beam theory, the method of layered grouting reinforcement of roadways is proposed according to the deformation and failure of the roadway roof and the internal drilling conditions. At the same time, combined with the splitting grouting mechanism, the roadway is strengthened and supported by layered grouting of “shallow bolt grouting + deep cable grouting”. The “shallow” and “deep” form a complete and stable composite beam support structure. After grouting, the bending moments of “shallow” and “deep” support beams decrease by 20.78 × 106 N·m and 26.50 × 106 N·m, respectively. The support scheme is applied to the field test, and the grouting effect is analyzed and monitored. The research results show the layered grouting support scheme of “shallow bolt grouting + deep cable grouting” can significantly improve the structural integrity of the roadway roof. The displacement of the two sides is within the controllable range, and the support role of the bolt and cable is entirely played through grouting. The roof displacement of the roadway is reduced by 65% on average, and the bolt failure and steel belt fracture are significantly reduced, which effectively controls the deformation and damage of the roadway and reduces the maintenance cost of the roadway while ensuring safe mining. The study’s findings could be useful in treating broken surrounding rock in other coal mine roadways. Full article
Show Figures

Figure 1

Figure 1
<p>Occurrence conditions of the roof and the floor of the coal seam.</p>
Full article ">Figure 2
<p>Deformation and failure conditions of the roadways.</p>
Full article ">Figure 3
<p>Characteristics of rock core.</p>
Full article ">Figure 4
<p>Processing of standard specimens.</p>
Full article ">Figure 5
<p>Stress–strain curve and failure mode of rock uniaxial compression experiment.</p>
Full article ">Figure 5 Cont.
<p>Stress–strain curve and failure mode of rock uniaxial compression experiment.</p>
Full article ">Figure 6
<p>Distribution of roadway surrounding rock state.</p>
Full article ">Figure 7
<p>Grouting diagram.</p>
Full article ">Figure 8
<p>Layered grouting support structure.</p>
Full article ">Figure 9
<p>Simply supported beam model of roof.</p>
Full article ">Figure 10
<p>Roadway support scheme.</p>
Full article ">Figure 11
<p>Layout of monitoring points.</p>
Full article ">Figure 12
<p>Variation curve of distance between two sides of ZF3806 mining roadway.</p>
Full article ">Figure 13
<p>Distance variation curve of ZF3806 roof and floor of mining roadway.</p>
Full article ">Figure 14
<p>Effect of grouting support.</p>
Full article ">
15 pages, 5216 KiB  
Article
Study on Stress–Strain Relationship of Coir Fiber-Reinforced Red Clay Based on Duncan–Chang Model
by Xueliang Jiang, Jiahui Guo, Hui Yang, Shufeng Bao, Changping Wen and Jiayu Chen
Appl. Sci. 2023, 13(1), 556; https://doi.org/10.3390/app13010556 - 30 Dec 2022
Cited by 2 | Viewed by 2044
Abstract
Compared with other natural fibers, coir fiber has good strength characteristics and long-term anti-biodegradation ability. At present, most studies on randomly distributed coir fiber-reinforced soil have focused on cohesionless soil or granular soil. In this paper, the influence of randomly distributed coir fiber [...] Read more.
Compared with other natural fibers, coir fiber has good strength characteristics and long-term anti-biodegradation ability. At present, most studies on randomly distributed coir fiber-reinforced soil have focused on cohesionless soil or granular soil. In this paper, the influence of randomly distributed coir fiber on the deviatoric stress and shear strength index of red clay with different fiber content was assessed by a consolidated undrained (CU) triaxial compression test. Since the hyperbolic variational character of the stress–strain relation of the samples conformed to the hyperbolic hypothesis of the Duncan–Chang model of nonlinear elastic model, the Duncan–Chang model was used to fit it, and the influences of fiber content and confining pressure on the parameters of the Duncan–Chang model were studied. The fiber content was determined by testing to be 0%, 0.2%, 0.25%, 0.3%, 0.35% and 0.4% of the dry soil mass. It has been found that coir fiber distributed in a random radial manner can significantly increase the deviatoric stress of red clay, and thus can be effectively used in the case of soil and fiber mixing. The cohesion of the red clay first increases and then decreases with the increase in fiber content, with an optimum content of 0.3%. The internal friction angle changes little with increasing fiber content. Full article
Show Figures

Figure 1

Figure 1
<p>Particle gradation curve of red clay.</p>
Full article ">Figure 2
<p>Coir fiber incorporated in soil.</p>
Full article ">Figure 3
<p>Sample preparation.</p>
Full article ">Figure 4
<p>Sample under loading.</p>
Full article ">Figure 5
<p>Relation curve between principal stress difference and axial strain. (<b>a</b>) 0% coir fiber; (<b>b</b>) 0.2% coir fiber; (<b>c</b>) 0.25% coir fiber; (<b>d</b>) 0.3% coir fiber; (<b>e</b>) 0.35% coir fiber; (<b>f</b>) 0.4% coir fiber.</p>
Full article ">Figure 5 Cont.
<p>Relation curve between principal stress difference and axial strain. (<b>a</b>) 0% coir fiber; (<b>b</b>) 0.2% coir fiber; (<b>c</b>) 0.25% coir fiber; (<b>d</b>) 0.3% coir fiber; (<b>e</b>) 0.35% coir fiber; (<b>f</b>) 0.4% coir fiber.</p>
Full article ">Figure 6
<p>Relation curve between pore water pressure and axial strain at 300 kPa.</p>
Full article ">Figure 7
<p>Mohr–Coulomb strength envelope of soil samples. (<b>a</b>) 0% coir fiber; (<b>b</b>) 0.2% coir fiber; (<b>c</b>) 0.25% coir fiber; (<b>d</b>) 0.3% coir fiber; (<b>e</b>) 0.35% coir fiber; (<b>f</b>) 0.4% coir fiber.</p>
Full article ">Figure 7 Cont.
<p>Mohr–Coulomb strength envelope of soil samples. (<b>a</b>) 0% coir fiber; (<b>b</b>) 0.2% coir fiber; (<b>c</b>) 0.25% coir fiber; (<b>d</b>) 0.3% coir fiber; (<b>e</b>) 0.35% coir fiber; (<b>f</b>) 0.4% coir fiber.</p>
Full article ">Figure 8
<p>Variation in shear strength index with fiber content. (<b>a</b>) influence of fiber content on cohesion; (<b>b</b>) influence of fiber content on internal friction angle.</p>
Full article ">Figure 9
<p>The failure mode of specimen under triaxial test.</p>
Full article ">Figure 10
<p><math display="inline"><semantics> <mrow> <msub> <mi>ε</mi> <mn>1</mn> </msub> <mo>/</mo> <mo>(</mo> <msub> <mi>σ</mi> <mn>1</mn> </msub> <mo>–</mo> <msub> <mi>σ</mi> <mn>3</mn> </msub> <mo>)</mo> <mo>~</mo> <msub> <mi>ε</mi> <mn>1</mn> </msub> </mrow> </semantics></math> curve of sample. (<b>a</b>) 0% coir fiber; (<b>b</b>) 0.2% coir fiber; (<b>c</b>) 0.25% coir fiber; (<b>d</b>) 0.3% coir fiber; (<b>e</b>) 0.35% coir fiber; (<b>f</b>) 0.4% coir fiber.</p>
Full article ">Figure 11
<p>Relationship curve between initial tangent modulus and confining pressure of sample.</p>
Full article ">
16 pages, 7121 KiB  
Article
Analysis of Influencing Factors of Cementitious Material Properties of Lead–Zinc Tailings Based on Orthogonal Tests
by Ziyi Yin, Rui Li, Hang Lin, Yifan Chen, Yixian Wang and Yanlin Zhao
Materials 2023, 16(1), 361; https://doi.org/10.3390/ma16010361 - 30 Dec 2022
Cited by 7 | Viewed by 1838
Abstract
At present, the treatment of tailings is mostly carried out in the form of stacking in tailings ponds, resulting in a huge waste of mineral resources and a major threat to the environment and ecology. Using tailings instead of a part of the [...] Read more.
At present, the treatment of tailings is mostly carried out in the form of stacking in tailings ponds, resulting in a huge waste of mineral resources and a major threat to the environment and ecology. Using tailings instead of a part of the cement to make cementitious materials is an effective way to reduce the accumulation of tailings. In this paper, lead–zinc tailings-based cementitious materials were prepared by using lead–zinc tailings, fly ash, and ordinary Portland cement, and the effects of four factors on the mechanical properties of lead–zinc tailings, as well as fly ash content, cement content, and water–binder ratio were studied by orthogonal experiments. The corresponding relationship between the factors and the properties of cementitious materials was determined, and the optimization and prediction of the raw material ratio of lead–zinc tailings-based cementitious materials were realized. The test showed the ratio of raw materials to be at the lowest price ratio. Synchronously the ratio that meets the minimum strength requirements was predicted. When the proportion of fly ash:lead and zinc tailings:cement = 30:40:30 and the water–binder ratio was 0.4, the predicted compressive strength of the prepared cementitious material achieved 22.281 MPa, which meets the strength requirements, while the total content of lead–zinc tailings and fly ash was the highest at this time. Full article
Show Figures

Figure 1

Figure 1
<p>Particle size distribution curve of Pb–Zn tailings.</p>
Full article ">Figure 2
<p>XRD patterns of lead–zinc tailings samples.</p>
Full article ">Figure 3
<p>Test Design.</p>
Full article ">Figure 4
<p>Test procedures.</p>
Full article ">Figure 5
<p>Uniaxial compressive strength test of 3 days, 7 days, and 28 days test block curing.</p>
Full article ">Figure 6
<p>The change diagram of compressive strength at 3 days, 7 days, and 28 days curing of each factor.</p>
Full article ">Figure 7
<p>Comparison of predicted and actual values of compressive strength for different curing days.</p>
Full article ">Figure 7 Cont.
<p>Comparison of predicted and actual values of compressive strength for different curing days.</p>
Full article ">Figure 8
<p>Effect of AB on compressive strength.</p>
Full article ">Figure 9
<p>Effect of BC on compressive strength.</p>
Full article ">
16 pages, 9673 KiB  
Article
Experimental Study on the Deformation and Mechanical Properties of Bamboo Forest Slopes
by Hui Yang, Zhengyi Cao, Xueliang Jiang and Yixian Wang
Appl. Sci. 2023, 13(1), 470; https://doi.org/10.3390/app13010470 - 29 Dec 2022
Cited by 1 | Viewed by 1455
Abstract
In this paper, model tests on a plain soil slope and a bamboo-rooted slope under slope top loading were carried out to analyze the slope surface displacement, the change in earth pressure, and the failure mode of the slope. Furthermore, the influence of [...] Read more.
In this paper, model tests on a plain soil slope and a bamboo-rooted slope under slope top loading were carried out to analyze the slope surface displacement, the change in earth pressure, and the failure mode of the slope. Furthermore, the influence of rainfall on the deformation and mechanical properties of bamboo-rooted slope sliding was studied. The results show that: (1) the failure mode of the plain soil slope was block sliding failure, while the failure mode of the bamboo-rooted slope was progressive backward failure. (2) Under the slope top load, the slope displacement shows the rule that the top of the slope was large and the foot of the slope was small. The presence of bamboo rhizomes had a negligible effect on the slope displacement, but it significantly contributed to the sliding area’s increase. (3) Compared with the plain soil slope, the earth pressure in the area of the foot of the slope under the same level of the load was elevated more obviously by the bamboo-rooted slope, which indicates that bamboo rhizomes could play a specific role in reinforcing the slope. Still, the scope of its influence was limited and mainly concentrated in the shallow soil. (4) There was a significant increase in the displacement of the bamboo-rooted slope under rainfall conditions, and the magnitude of the upward slope earth pressure was small in the process of step-by-step loading. The test results may have important guiding significance for the in-depth study of the instability law and disaster prevention in bamboo forest areas. Full article
Show Figures

Figure 1

Figure 1
<p>Jinpen Mountain bamboo forest.</p>
Full article ">Figure 2
<p>Morphology of the bamboo rhizomes.</p>
Full article ">Figure 3
<p>Test G1–G3 sensor arrangement.</p>
Full article ">Figure 4
<p>Schematic diagram of bamboo rhizomes’ embedment.</p>
Full article ">Figure 5
<p>Rainfall simulation system.</p>
Full article ">Figure 6
<p>Slope failure after loading in each group of tests. (<b>a</b>) Test G1 plain soil slope. (<b>b</b>) Test G2 bamboo-rooted slope. (<b>c</b>) Test G3 rainfall bamboo-rooted slope.</p>
Full article ">Figure 7
<p>Variation of horizontal displacement in the slope with a slope top load. (<b>a</b>) Test G1 plain soil slope. (<b>b</b>) Test G2 bamboo-rooted slope. (<b>c</b>) Test G3 rainfall bamboo-rooted slope.</p>
Full article ">Figure 8
<p>Displacement of representative measurement points in each group of tests. (<b>a</b>) Measurement point D4. (<b>b</b>) Measurement point D3.</p>
Full article ">Figure 9
<p>Variation of horizontal earth pressure at measured points along the slope with the slope top load (<b>a</b>) Test G1 plain soil slope. (<b>b</b>) Test G2 bamboo-rooted slope. (<b>c</b>) Test G3 rainfall bamboo-rooted slope.</p>
Full article ">Figure 10
<p>Earth pressure of representative measurement points in each group of tests. (<b>a</b>) Measurement point S2. (<b>b</b>) Measurement point S4.</p>
Full article ">Figure 11
<p>Variation of horizontal earth pressure at measured points along the bottom of the slope with the slope top load (<b>a</b>) Test G1 plain soil slope. (<b>b</b>) Test G2 bamboo-rooted slope. (<b>c</b>) Test G3 rainfall bamboo-rooted slope.</p>
Full article ">Figure 12
<p>Earth pressure at representative measurement points in each group of tests. (<b>a</b>) Measurement point S6. (<b>b</b>) Measurement point S7.</p>
Full article ">Figure 13
<p>Distribution of water content measuring points.</p>
Full article ">
16 pages, 3217 KiB  
Article
Study on Application of Comprehensive Geophysical Prospecting Method in Urban Geological Survey—Taking Concealed Bedrock Detection as an Example in Dingcheng District, Changde City, Hunan Province, China
by Yu-Long Lu, Chuang-Hua Cao, Yao-Qi Liu and Yang Liu
Appl. Sci. 2023, 13(1), 417; https://doi.org/10.3390/app13010417 - 28 Dec 2022
Cited by 2 | Viewed by 1980
Abstract
In order to ascertain the concealed bedrock and its spatial distribution in an urban low-resistance coverage area of a typical lacustrine basin in Hunan Province, a multi-method comprehensive experimental study was carried out in Dingcheng District, Changde City where there are multiple sets [...] Read more.
In order to ascertain the concealed bedrock and its spatial distribution in an urban low-resistance coverage area of a typical lacustrine basin in Hunan Province, a multi-method comprehensive experimental study was carried out in Dingcheng District, Changde City where there are multiple sets of strata and fault structures. In this study, the wide-area electromagnetic method and microtremor survey were utilized on the basis of traditional methods, including the high-density resistivity method and controlled-source audio-frequency magnetotelluric method, to infer the concealed Cambrian limestone, fault structure, and vertical distribution of strata and the results were verified by drilling. The results indicate that the wide-area electromagnetic method is effective to explore the bedrock and concealed structure in urban geological survey. The microtremor method has an obvious effect on the detection of the Cretaceous and Quaternary silty strata within 100 m. The study may provide references for similar projects in this area. Full article
Show Figures

Figure 1

Figure 1
<p>Location map of geological and geophysical test sections in the study area (revised from 1:50,000 Chang-de regional geological map).</p>
Full article ">Figure 2
<p>Geological interpretation of G4 test profile in the study area (<b>a</b>) High-density electrical processing results; (<b>b</b>) Controllable-source audio-magnetotelluric processing results; (<b>c</b>) Wide-area electromagnetic processing results; (<b>d</b>) Geological profile of G4.</p>
Full article ">Figure 3
<p>Lithographic layering results of sk09 natural source surface wave microtremor detection of dispersive wave velocity.</p>
Full article ">Figure 4
<p>Lithographic layering results of sk10 natural source surface wave microtremor detection of dispersive wave velocity.</p>
Full article ">Figure 5
<p>sk9 drilling core cataloguing results.</p>
Full article ">Figure 6
<p>sk10 drilling core cataloguing results.</p>
Full article ">
21 pages, 8212 KiB  
Article
A Constitutive Model of Time-Dependent Deformation Behavior for Sandstone
by Chongfeng Chen
Materials 2023, 16(1), 135; https://doi.org/10.3390/ma16010135 - 23 Dec 2022
Cited by 1 | Viewed by 1478
Abstract
Considering sandstone’s heterogeneity in the mesoscale and homogeneity in the macroscale, it is very difficult to describe its time-dependent behavior under stress. The mesoscale heterogeneity can affect the initiation and propagation of cracks. Clusters of cracks have a strong influence on the formation [...] Read more.
Considering sandstone’s heterogeneity in the mesoscale and homogeneity in the macroscale, it is very difficult to describe its time-dependent behavior under stress. The mesoscale heterogeneity can affect the initiation and propagation of cracks. Clusters of cracks have a strong influence on the formation of macroscale fractures. In order to investigate the influence of crack evolution on the formation of fractures during creep deformation, a time-dependent damage model is introduced in this paper. First, the instantaneous elastoplastic damage model of sandstone was built based on the elastoplastic theory of rock and the micro-heterogeneous characteristics of sandstone. A viscoelastic plastic creep damage model was established by combining the Nishihara model and the elastoplastic damage constitutive model. The proposed models have been validated by the results of corresponding analytical solutions. To help back up the model, some conventional constant strain rate tests and multi-step creep tests were carried out to analyze the time-dependent behavior of sandstone. The results show that the proposed damage model can not only reflect the time-dependent viscoelastic deformation characteristics of sandstone, but also provide a good fit to the viscoelastic plastic deformation characteristics of sandstone’s creep behavior. The damage model can also reproduce the propagation process of mesoscopic cracks in sandstone upon the damage and failure of micro-units. This research can provide an effective tool for studying the propagation of microscopic cracks in sandstone. Full article
Show Figures

Figure 1

Figure 1
<p>Heterogeneous model of sandstone in the mesoscale. (<b>A</b>) Optical microscope image at a 100 μm scale [<a href="#B45-materials-16-00135" class="html-bibr">45</a>]. (<b>B</b>) Heterogeneous distribution of strength elements in the model.</p>
Full article ">Figure 2
<p>Elastic-plastic damage constitutive rule for an element under uniaxial compression and tension.</p>
Full article ">Figure 3
<p>Numerical model of analytical solution with a borehole in the center of the stress field.</p>
Full article ">Figure 4
<p>Fitted yield and fracture surfaces from experimental data. (<b>A</b>) Axial differential stress vs. axial strain curves under different confining pressures. (<b>B</b>) Effective deviatoric stress vs. mean effective stress for the yield surface and the failure surface.</p>
Full article ">Figure 5
<p>Comparison between numerical simulation results at different degrees of homogeneity and the analytical solutions. (<b>A</b>) Stress curves of radial stress vs. distance to the center of the borehole. (<b>B</b>) Stress curves of circumferential stress vs. distance to the center of the borehole.</p>
Full article ">Figure 6
<p>Cloud map of plastic strain around the borehole calculated from the damage model. (<b>A</b>) Plastic deformation zone around the borehole. (<b>B</b>) Enlarged view.</p>
Full article ">Figure 7
<p>Schematic diagram of the traditional Nishihara model.</p>
Full article ">Figure 8
<p>Schematic diagram of the improved Nishihara model.</p>
Full article ">Figure 9
<p>Mechanical model of circular stress field with a center borehole.</p>
Full article ">Figure 10
<p>Comparison of displacement and circumferential stress distribution between the analytical solution and the proposed damage model at different homogeneities.</p>
Full article ">Figure 11
<p>Stress–strain curves of Neijiang sandstone obtained from numerical simulation and laboratory tests. Lateral strain, axial strain and volumetric strain are obtained from the numerical simulation.</p>
Full article ">Figure 12
<p>Strength failure snapshots extracted from the simulation result of the damage model. (<b>A</b>) An undamaged model. (<b>B</b>) Some cracks appear in the specimen. (<b>C</b>) Some cracks appear to accumulate and coalesce. (<b>D</b>) Main fracture surface is generated and some new cracks appear around the main fracture.</p>
Full article ">Figure 13
<p>Failure mode of Neijiang sandstone in uniaxial compression strength tests. (<b>A</b>) The shear failure angle is about 25 degrees. There are some small cracks around the main fracture. (<b>B</b>) A main shear fracture on another side opposite to (<b>A</b>).</p>
Full article ">Figure 14
<p>Comparison of axial and transverse strain vs. time curves in numerical simulation and in laboratory tests.</p>
Full article ">Figure 15
<p>Contour diagram of strength failure of graded incremental loading creep test.</p>
Full article ">Figure 16
<p>Failure mode of Neijiang sandstone in multi-step creep test. (<b>A</b>) The failure mode focuses on the shear failure, and a small crack (highlighted by the yellow circle) occurs near the main fracture similar to that in the failure mode in the UCS tests. (<b>B</b>) A main shear fracture on another side opposite to (<b>A</b>).</p>
Full article ">Figure 17
<p>Relationships between creep strain rate and applied stress in the multi-step creep tests in the laboratory and in numerical simulation.</p>
Full article ">
22 pages, 53326 KiB  
Article
Mechanical Properties and Failure Behavior of Dry and Water-Saturated Foliated Phyllite under Uniaxial Compression
by Guanping Wen, Jianhua Hu, Yabin Wu, Zong-Xian Zhang, Xiao Xu and Rui Xiang
Materials 2022, 15(24), 8962; https://doi.org/10.3390/ma15248962 - 15 Dec 2022
Cited by 2 | Viewed by 1667
Abstract
Phyllite is widely distributed in nature, and it deserves to be studied considering rock engineering applications. In this study, uniaxial compression tests were conducted on foliated phyllite with different foliation angles under dry and water-saturated conditions. The impacts of water content and foliation [...] Read more.
Phyllite is widely distributed in nature, and it deserves to be studied considering rock engineering applications. In this study, uniaxial compression tests were conducted on foliated phyllite with different foliation angles under dry and water-saturated conditions. The impacts of water content and foliation angle on the stress–strain curves and basic mechanical properties of the Phyllite were analyzed. The experimental results indicate that the peak stress and peak strain decrease first and then increase with increasing foliation angle as a U-shape or V-shape, and the phyllite specimens are weakened significantly by the presence of water. Moreover, an approach with acoustic emission, digital image correlation, and scanning electron microscopic is employed to observe and analyze the macroscopic and mesoscopic failure process. The results show that tensile microcracks dominate during the progressive failure of phyllite, and their initiation, propagation, and coalescence are the main reasons for the failure of the phyllite specimens. The water acts on biotite and clay minerals that are main components of phyllite, and it contributes to the initiation, propagation, and coalescence of numerous microcracks. Finally, four failure modes are classified as followed: (a) for the specimens with small foliation angles α = 0° or 30° (Saturated), both shear sliding and tensile-split across the foliation planes; (b) for the specimens with low to medium foliation angles α = 30° (Dry) or 45°(Saturated), shear sliding dominates the foliation planes; (c) for the specimens with medium to high foliation angles α = 45° (Dry) or 60°, shear sliding dominates the foliation planes; (d) for the specimens with high foliation angles α = 90°, tensile-split dominates the foliation planes. Full article
Show Figures

Figure 1

Figure 1
<p>X-ray diffraction (XRD) and Standard Electronic Modules (SEM) analysis.</p>
Full article ">Figure 2
<p>Schematic diagram of the loading system, the DIC system, and the AE system.</p>
Full article ">Figure 3
<p>Axial stress-strain curves of layered phyllite with different bedding angles α. (<b>a</b>) Dry groups; (<b>b</b>) Water-saturated groups.</p>
Full article ">Figure 4
<p>Comparison of mechanical properties of foliated phyllite from dry condition and water-saturated condition: (<b>a</b>) Uniaxial compression strength, <span class="html-italic">σ<sub>c</sub></span>; (<b>b</b>) Peak axial strain, <span class="html-italic">ε<sub>c</sub></span>; (<b>c</b>) Elastic modulus, <span class="html-italic">E</span>.</p>
Full article ">Figure 5
<p>An entire crack evolution process of a typical foliated phyllite subjected to uniaxial compressive loading (S-W-90°): (<b>a</b>) Geometrical parameters and loading diagram of the specimen; (<b>b</b>) Axial stress–strain curves of a typical specimen; (<b>c</b>) The maximum principal strain fields under different loads stage.</p>
Full article ">Figure 6
<p>Crack evolution process of dry phyllite with 0° foliation angle (S-D-0°).</p>
Full article ">Figure 7
<p>Crack evolution process of water-saturated phyllite with 45° foliation angle (S-W-45°).</p>
Full article ">Figure 8
<p>Crack evolution process of water-saturated phyllite with 60° foliation angle (S-W-60°).</p>
Full article ">Figure 9
<p>Crack evolution process of dry phyllite with 90° foliation angle (S-D-90°).</p>
Full article ">Figure 10
<p>Classification of tensile and shear cracks based on AE parameter analysis: (<b>a</b>) Graphical representations of AE characteristic parameters; (<b>b</b>) Comparison between typical waveform of tensile event and shear event; (<b>c</b>) Crack classification methods in AE parameter analysis.</p>
Full article ">Figure 11
<p>Comparison of AF-RA distribution of foliated phyllite with different foliation angles under dry and water-saturated conditions: (<b>a</b>) S-D-0°; (<b>b</b>) S-W-0°; (<b>c</b>) S-D-30°; (<b>d</b>) S-W-30°; (<b>e</b>) S-D-45°; (<b>f</b>) S-W-45°; (<b>g</b>) S-D-60°; (<b>h</b>) S-W-60°; (<b>i</b>) S-D-90°; (<b>j</b>) S-W-90°.</p>
Full article ">Figure 12
<p>Comparison of the proportions of shear and tensile cracks for foliation phyllite with different foliation angles.</p>
Full article ">Figure 13
<p>Comparison of failure mechanisms between foliated phyllite with different: (<b>a</b>) Shear sliding-tensile splitting across foliation planes (Mode I); (<b>b</b>) Shear sliding across foliation planes (Mode II); (<b>c</b>) Shear sliding along foliation planes (Mode III); (<b>d</b>) Tensile splitting along foliation planes (Mode IV).</p>
Full article ">Figure 14
<p>Failure mechanism analysis of foliated phyllite under uniaxial compression.</p>
Full article ">Figure 15
<p>SEM photos of the fracture surfaces for phyllite subjected to shear failure in uniaxial compression: (<b>a</b>) S-D-0; (<b>b</b>) S-W-45; (<b>c</b>) S-D-60; (<b>d</b>) S-W-60.</p>
Full article ">Figure 16
<p>SEM photos of the fracture surfaces for phyllite subjected to tensile failure in uniaxial compression: (<b>a</b>) S-D-0; (<b>b</b>) S-D-90.</p>
Full article ">Figure 17
<p>Diagram of the influence of water on phyllite microstructure.</p>
Full article ">Figure 18
<p>Uniaxial compressive strength of anisotropic rock versus foliation or bedding angle.</p>
Full article ">
17 pages, 4908 KiB  
Article
A Unified Nonlinear Elastic Model for Rock Material
by Chong Chen, Shenghong Chen, Yihu Zhang, Hang Lin and Yixian Wang
Appl. Sci. 2022, 12(24), 12725; https://doi.org/10.3390/app122412725 - 12 Dec 2022
Viewed by 1892
Abstract
Under conditions of low or medium stress, rocks that are in the compression state exhibit perceivable nonlinear elastic characteristics. After a comprehensive review of the existing nonlinear elastic models of rocks and joints, we proposed a new unified nonlinear elastic model. This new [...] Read more.
Under conditions of low or medium stress, rocks that are in the compression state exhibit perceivable nonlinear elastic characteristics. After a comprehensive review of the existing nonlinear elastic models of rocks and joints, we proposed a new unified nonlinear elastic model. This new model contains two parameters with clear definitions, namely, the initial elastic modulus Eni and the modulus change rate m. This model covers a variety of existing models, including the simple exponential model, BB model and two-part Hooke’s model, etc. Based on the RMT experimental system, a large number of uniaxial compression tests for dolomite, granite, limestone and sandstone were performed, and their nonlinear deformation stress‒strain curves were obtained and fit with the unified nonlinear elastic model. The results show that the rocks have obvious nonlinear elastic characteristics in their initial compression stage, and that the unified nonlinear elastic model is able to describe these phenomena rather well. In addition, an empirical formula for predicting the uniaxial compressive strength of the rock was constructed, corresponding to the unified nonlinear elastic model. Full article
Show Figures

Figure 1

Figure 1
<p>The stress‒strain curve of a uniaxial compression test adapted from Corkum. Adapted from [<a href="#B21-applsci-12-12725" class="html-bibr">21</a>].</p>
Full article ">Figure 2
<p>Linear and nonlinear elastic deformation of rock adapted from Liu. Adapted from [<a href="#B30-applsci-12-12725" class="html-bibr">30</a>].</p>
Full article ">Figure 3
<p>Linear and nonlinear elastic curves (<b>a</b>-Linear elastic; <b>b</b>-Nonlinear elastic).</p>
Full article ">Figure 4
<p>Stress‒strain curves for different <span class="html-italic">E<sub>ni</sub></span> values (<span class="html-italic">m</span> = 1.0).</p>
Full article ">Figure 5
<p>Stress‒strain curves for different <span class="html-italic">m</span> values (<span class="html-italic">E<sub>ni</sub></span> = 10 MPa).</p>
Full article ">Figure 6
<p>Fitting results of different strain ranges.</p>
Full article ">Figure 7
<p>Approximating to a single stress‒strain curve.</p>
Full article ">Figure 8
<p>Rock mechanics test system (RMT).</p>
Full article ">Figure 9
<p>Different rock specimens.</p>
Full article ">Figure 10
<p>Typical stress‒strain curves.</p>
Full article ">Figure 11
<p>The R<sup>2</sup> values with different <span class="html-italic">m</span> values for different rock types. (<b>a</b>—Dolomite; <b>b</b>—Granite; <b>c</b>—Limestone; <b>d</b>—Sandstone).</p>
Full article ">Figure 12
<p>The <span class="html-italic">E<sub>ni</sub></span> values with different <span class="html-italic">m</span> values for different rock types. (<b>a</b>—Dolomite; <b>b</b>—Granite; <b>c</b>—Limestone; <b>d</b>—Sandstone).</p>
Full article ">Figure 13
<p>Correlations between <span class="html-italic">UCS</span> and <span class="html-italic">E<sub>ni</sub></span> for different rock types. (<b>a</b>—Dolomite; <b>b</b>—Granite; <b>c</b>—Limestone; <b>d</b>—Sandstone).</p>
Full article ">Figure 14
<p>Comprehensive relationship between <span class="html-italic">UCS</span> and <span class="html-italic">E<sub>ni</sub></span> for all the rock types.</p>
Full article ">
22 pages, 17944 KiB  
Article
Numerical and Experimental Study on a Novel Filling Support Method for Mining of Closely Spaced Multilayer Orebody
by Xiuwen Chi, Zhuojun Zhang, Lifeng Li, Qizhou Wang, Zongying Wang, Haoran Dong and Yu Xie
Minerals 2022, 12(12), 1523; https://doi.org/10.3390/min12121523 - 28 Nov 2022
Cited by 2 | Viewed by 1331
Abstract
Mining of closely spaced multilayer orebodies brings the problems of significant disturbance between adjacent mining layers and drastic structural changes in surrounding rock, which brings the need for a more effective stope support method. Previous research has made sound analysis on filling or [...] Read more.
Mining of closely spaced multilayer orebodies brings the problems of significant disturbance between adjacent mining layers and drastic structural changes in surrounding rock, which brings the need for a more effective stope support method. Previous research has made sound analysis on filling or bolt support, but neither of them can solely provide ideal support effects. Thus, a novel bolt-filling support method is proposed by utilizing the synergistic effect of rock bolts (cable bolts) and filling. Numerical simulation and similarity experiments were conducted in this research to analyze the support effect of this method for multilayer ore mining. For numerical simulation, the distinct-element modelling framework PFC2D (Particle Flow Code in 2 Dimensions) was applied for four support scenarios based on the calibration of the microscopic parameters of particles in vanadium shale ores. The numerical simulation results show that the number of fractures decreases from 1311 without support through 652 with 95% filling support to 410 with bolt-filling support, which is resulted from the redistribution of the force chains due to support change. On the other hand, a 300 cm ×180 cm × 40 cm similarity model with a geometry similarity constant of 100 was established based on the 4# rock layer profile of Mount Shangheng. Two parts of similarity experiments were conducted to investigate the strains around the stopes in multi-layer ore mining for three support scenarios. The experiment results prove that the highest strain is in the center of the roof on the upper goaf, and the roof-bolt filling support induces smaller strains than zero support and conventional filling support. Finally, an effective bolt-filling support system has been developed and validated, which can improve the safety and the stability of the roofs and interlayers during the mining process of closely spaced multilayer orebody by reducing the overall load and fractures in surrounding rock. Full article
Show Figures

Figure 1

Figure 1
<p>Demonstration of the bolt-filling support system. (<b>a</b>) Schematic diagram of bolt-filling support; (<b>b</b>) Longitudinal section of drill hole arrangement for closely spaced multilayer orebodies; (<b>c</b>) Cross-sectional view of drill hole arrangement for closely spaced multilayer orebodies; (<b>d</b>) Longitudinal section of bolt-filling support system for closely spaced multilayer orebodies; (<b>e</b>) Top view of cable bolt network. 1—Surrounding rock, 2—Roof hole, 3—Goaf, 4—Floor hole, 5—Rock bolt, 6—Cable bolt, 7—Pre-loop, 8—Cable bolt network, 9—Backfill, 10—Ore body, 11—Ore pile.</p>
Full article ">Figure 1 Cont.
<p>Demonstration of the bolt-filling support system. (<b>a</b>) Schematic diagram of bolt-filling support; (<b>b</b>) Longitudinal section of drill hole arrangement for closely spaced multilayer orebodies; (<b>c</b>) Cross-sectional view of drill hole arrangement for closely spaced multilayer orebodies; (<b>d</b>) Longitudinal section of bolt-filling support system for closely spaced multilayer orebodies; (<b>e</b>) Top view of cable bolt network. 1—Surrounding rock, 2—Roof hole, 3—Goaf, 4—Floor hole, 5—Rock bolt, 6—Cable bolt, 7—Pre-loop, 8—Cable bolt network, 9—Backfill, 10—Ore body, 11—Ore pile.</p>
Full article ">Figure 2
<p>Correlation between Poisson’s ratio and stiffness ratio and friction coefficient. (<b>a</b>) Relationship between stiffness ratio <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="normal">k</mi> <mi mathvariant="normal">n</mi> </msub> <mo>/</mo> <msub> <mi mathvariant="normal">k</mi> <mi mathvariant="normal">s</mi> </msub> </mrow> </semantics></math> and Poisson’s ratio <math display="inline"><semantics> <mi mathvariant="sans-serif">ν</mi> </semantics></math>; (<b>b</b>) Relationship between friction coefficient μ and Poisson’s ratio <math display="inline"><semantics> <mi mathvariant="sans-serif">ν</mi> </semantics></math>.</p>
Full article ">Figure 3
<p>Correlation between elastic modulus and effective modulus of contact, friction coefficient, and stiffness ratio. (<b>a</b>) Relationship between effective modulus of contact <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="normal">E</mi> <mi mathvariant="normal">c</mi> </msub> </mrow> </semantics></math> elastic modulus <math display="inline"><semantics> <mi mathvariant="normal">E</mi> </semantics></math>; (<b>b</b>) Relationship between square of friction coefficient <math display="inline"><semantics> <mrow> <msup> <mi mathvariant="sans-serif">μ</mi> <mn>2</mn> </msup> </mrow> </semantics></math> and elastic modulus <math display="inline"><semantics> <mi mathvariant="normal">E</mi> </semantics></math>; (<b>c</b>) Relationship between logarithm of stiffness ratio <math display="inline"><semantics> <mrow> <msub> <mrow> <mrow> <mi>ln</mi> <mo>(</mo> <mi mathvariant="normal">k</mi> </mrow> </mrow> <mi mathvariant="normal">n</mi> </msub> <mo>/</mo> <msub> <mi mathvariant="normal">k</mi> <mi mathvariant="normal">s</mi> </msub> <mo>)</mo> </mrow> </semantics></math> and elastic modulus <math display="inline"><semantics> <mi mathvariant="normal">E</mi> </semantics></math>.</p>
Full article ">Figure 4
<p>Correlation between uniaxial compressive strength and the tensile strength, cohesion of bonds, and friction coefficient. (<b>a</b>) Relationship between tensile strength <math display="inline"><semantics> <mrow> <msub> <mrow> <mrow> <mtext> </mtext> <mi mathvariant="sans-serif">σ</mi> </mrow> </mrow> <mi mathvariant="normal">n</mi> </msub> </mrow> </semantics></math> and uniaxial compressive strength <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">c</mi> </msub> </mrow> </semantics></math>; (<b>b</b>) Relationship between cohesion of bonds c and uniaxial compressive strength <math display="inline"><semantics> <mrow> <mo> </mo> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">c</mi> </msub> </mrow> </semantics></math>; (<b>c</b>) Relationship between friction coefficient μ and uniaxial compressive strength <math display="inline"><semantics> <mrow> <mo> </mo> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">c</mi> </msub> </mrow> </semantics></math>.</p>
Full article ">Figure 5
<p>Variation curve of rock’s tensile strength with cohesion and tensile strength of bonds. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">t</mi> </msub> </mrow> </semantics></math> − c; (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">t</mi> </msub> </mrow> </semantics></math> − <math display="inline"><semantics> <mrow> <msub> <mi mathvariant="sans-serif">σ</mi> <mi mathvariant="normal">n</mi> </msub> </mrow> </semantics></math>.</p>
Full article ">Figure 6
<p>Uniaxial compressive experiment of surrounding rock and ore. (<b>a</b>) Uniaxial compression experiment of carbonaceous shale; (<b>b</b>) Uniaxial compression experiment of Vanadium-bearing shale.</p>
Full article ">Figure 7
<p>Stress–strain curve of surrounding rock and ore (1—Simulation curve, 2—Test curve). (<b>a</b>) Surrounding rock; (<b>b</b>) ore.</p>
Full article ">Figure 8
<p>PFC2D numerical simulation model of double-layer ore.</p>
Full article ">Figure 9
<p>Mechanics simulation of surrounding rock without support. (<b>a</b>) No support in the upper goaf; (<b>b</b>) Distribution of fractures when the upper goaf is not supported; (<b>c</b>) Distribution of the force chains when the upper goaf is not supported.</p>
Full article ">Figure 10
<p>Mechanics simulation of surrounding rock with the upper goaf 100% filled. (<b>a</b>) Filling support in the upper goaf (100%); (<b>b</b>) Distribution of fractures when the upper goaf is 100% filled; (<b>c</b>) Distribution of the force chains when the upper goaf is 100% filled.</p>
Full article ">Figure 11
<p>Mechanics simulation of surrounding rock with the upper goaf 95% filled. (<b>a</b>) Filling support in the upper goaf (95%); (<b>b</b>) Distribution of fractures when the upper goaf is 95% filled; (<b>c</b>) Distribution of the force chains when the upper goaf is 95% filled.</p>
Full article ">Figure 12
<p>Mechanics simulation of surrounding rock with bolt-fill support. (<b>a</b>) Bolt-filling support in the upper goaf; (<b>b</b>) Distribution of fractures with upper bolt-filling support; (<b>c</b>) Distribution of the force chains with upper bolt-filling support.</p>
Full article ">Figure 13
<p>River sand screening.</p>
Full article ">Figure 14
<p>Specimen of similar material model.</p>
Full article ">Figure 15
<p>Similarity model plan.</p>
Full article ">Figure 16
<p>Model building process. (<b>a</b>) Paste the model background image; (<b>b</b>) Mixing materials; (<b>c</b>) Filling materials in layer; (<b>d</b>) Finished model.</p>
Full article ">Figure 17
<p>Pre-experimental system test.</p>
Full article ">Figure 18
<p>Sensor Installation. (<b>a</b>) Fixing strain gages; (<b>b</b>) Connecting strain gages to monitoring system.</p>
Full article ">Figure 18 Cont.
<p>Sensor Installation. (<b>a</b>) Fixing strain gages; (<b>b</b>) Connecting strain gages to monitoring system.</p>
Full article ">Figure 19
<p>Layout of the stopes and monitoring points for the double-layer ore body mining experiment.</p>
Full article ">Figure 20
<p>Excavation process of experiment 1. (<b>a</b>) Excavation of E1; (<b>b</b>) Excavation of E2; (<b>c</b>) Excavation of F1; (<b>d</b>) Excavation of F2.</p>
Full article ">Figure 21
<p>Stope and monitoring point arrangement.</p>
Full article ">Figure 22
<p>Mining process of experiment 2. (<b>a</b>) Excavation of A1, A2, A3; (<b>b</b>) Excavation of B1, B2, B3 and support of A1, A2.</p>
Full article ">Figure 23
<p>Picture of bolt-filling support. (<b>a</b>) Similar experimental bolt-filling support diagram; (<b>b</b>) Rock bolt and cable bolt connection diagram.</p>
Full article ">Figure 24
<p>Strain-time curve of E1 stope roof.</p>
Full article ">Figure 25
<p>Strain-time curve of F1 stope roof (interlayer).</p>
Full article ">Figure 26
<p>Strain–time curve of the pillars.</p>
Full article ">Figure 27
<p>Strain–time curve of the roofs in experiment 2.</p>
Full article ">
24 pages, 7404 KiB  
Article
Experimental Investigation on Uniaxial Compressive Strength of Thin Building Sandstone
by Baofeng Huang, Yixian Xu and Guojun Zhang
Buildings 2022, 12(11), 1945; https://doi.org/10.3390/buildings12111945 - 10 Nov 2022
Cited by 2 | Viewed by 2795
Abstract
Thin sandstone is a widely used building material; however, its compressive behavior is not well understood. Four groups of cylinders were manufactured in a factory to investigate the uniaxial compressive behavior of red sandstone. Uniaxial compression tests were performed to determine the compressive [...] Read more.
Thin sandstone is a widely used building material; however, its compressive behavior is not well understood. Four groups of cylinders were manufactured in a factory to investigate the uniaxial compressive behavior of red sandstone. Uniaxial compression tests were performed to determine the compressive behavior and failure mode of the specimens. The geometry of the stress–strain diagram varied among the four groups. The critical strain generally increased with a decrease in the height of the cylinder, whereas the compressive strength exhibited an inverse trend. The experimental diagrams were normalized with the peak stress and corresponding critical strain to represent the stress–strain diagram of each group of cylinders. A formula consisting of two parabolas was employed for regression to obtain a representative mathematical expression of the diagram. The correlations between porosity, compressive strength, and elastic modulus were evaluated based on empirical expressions. Normalized strength was employed to evaluate the size effect on the diameter and length–diameter ratio (L/D) of the cylinder; the latter provided a better prediction of the experimental results than the former. A new expression in terms of L/D was proposed based on the regression analysis of the experimental results. This study is beneficial for the engineering application of sandstone as a construction material. Full article
Show Figures

Figure 1

Figure 1
<p>Red sandstone.</p>
Full article ">Figure 2
<p>Test specimens.</p>
Full article ">Figure 3
<p>Fatigue machine and cylinder.</p>
Full article ">Figure 4
<p>Failure patterns of sandstone. (<b>a</b>) Group A. (<b>b</b>) Vaneghi et al. [<a href="#B60-buildings-12-01945" class="html-bibr">60</a>]. (<b>c</b>) Li et al. [<a href="#B35-buildings-12-01945" class="html-bibr">35</a>]. (<b>d</b>) Wasantha et al. [<a href="#B62-buildings-12-01945" class="html-bibr">62</a>]. (<b>e</b>) Group B. (<b>f</b>) Group C. (<b>g</b>) Group D. (<b>h</b>) Cylindrical fracture of group B. (<b>i</b>) Cylindrical fracture of group C. (<b>j</b>) Cylindrical fracture of group D. (<b>k</b>) Fakhimi and Hemami [<a href="#B61-buildings-12-01945" class="html-bibr">61</a>].</p>
Full article ">Figure 5
<p>Stress–strain diagrams.</p>
Full article ">Figure 5 Cont.
<p>Stress–strain diagrams.</p>
Full article ">Figure 6
<p>Progressive failure of brittle material (adapted from [<a href="#B28-buildings-12-01945" class="html-bibr">28</a>]).</p>
Full article ">Figure 7
<p>Threshold stresses.</p>
Full article ">Figure 8
<p>Diagram regression.</p>
Full article ">Figure 8 Cont.
<p>Diagram regression.</p>
Full article ">Figure 9
<p>Compressive strength (note: σ denotes the standard deviation).</p>
Full article ">Figure 10
<p>Compressive strength predictions.</p>
Full article ">Figure 11
<p>Elastic moduli (note: <span class="html-italic">σ</span> denotes standard deviation).</p>
Full article ">Figure 12
<p>Elastic modulus and prediction.</p>
Full article ">Figure 13
<p>UCS and elastic modulus.</p>
Full article ">Figure 14
<p>Size effect on diameter.</p>
Full article ">Figure 15
<p>Normalized strength with theoretical expression.</p>
Full article ">Figure 16
<p>Normalized strength with empirical expressions.</p>
Full article ">
17 pages, 9161 KiB  
Article
The Freeze-Thaw Strength Evolution of Fiber-Reinforced Cement Mortar Based on NMR and Fractal Theory: Considering Porosity and Pore Distribution
by Chaoyang Zhang, Taoying Liu, Chong Jiang, Zhao Chen, Keping Zhou and Lujie Chen
Materials 2022, 15(20), 7316; https://doi.org/10.3390/ma15207316 - 19 Oct 2022
Cited by 8 | Viewed by 1644
Abstract
Predicting the strength evolution of fiber-reinforced cement mortar under freeze-thaw cycles plays an important role in engineering stability evaluation. In this study, the microscopic pore distribution characteristics of fiber-reinforced cement mortar were obtained by using nuclear magnetic resonance (NMR) technology. The change trend [...] Read more.
Predicting the strength evolution of fiber-reinforced cement mortar under freeze-thaw cycles plays an important role in engineering stability evaluation. In this study, the microscopic pore distribution characteristics of fiber-reinforced cement mortar were obtained by using nuclear magnetic resonance (NMR) technology. The change trend of T2 spectrum curve and porosity cumulative distribution curve showed that the freeze-thaw resistance of cement mortar increased first and then decreased with the fiber content. The optimal fiber content was approximately 0.5%. By conducting mechanical experiments, it is found that the uniaxial compressive strength (UCS) of the samples exhibited the ‘upward convex’ evolution trends with freeze-thaw cycles due to cement hydration, and based on fractal theory, the negative correlation between UCS and Dmin was established. Eventually, a freeze-thaw strength prediction model considering both porosity and pore distribution was proposed, which could accurately predict the strength deterioration law of cement-based materials under freeze-thaw conditions. Full article
Show Figures

Figure 1

Figure 1
<p>Experimental procedures and instruments.</p>
Full article ">Figure 2
<p>River sand particle gradation.</p>
Full article ">Figure 3
<p><span class="html-italic">T</span><sub>2</sub> spectrum and porosity cumulative distribution curve. (<b>a</b>) <span class="html-italic">T</span><sub>2</sub> spectrum curve, (<b>b</b>) Porosity cumulative distribution curve.</p>
Full article ">Figure 4
<p>Changes of pore distribution with freeze-thaw cycles. (<b>a</b>) A1, (<b>b</b>) A2, (<b>c</b>) A3, (<b>d</b>) A4.</p>
Full article ">Figure 4 Cont.
<p>Changes of pore distribution with freeze-thaw cycles. (<b>a</b>) A1, (<b>b</b>) A2, (<b>c</b>) A3, (<b>d</b>) A4.</p>
Full article ">Figure 5
<p><span class="html-italic">T</span><sub>2</sub> spectral distribution curves of cement mortars with different fiber contents after 100 freeze-thaw cycles.</p>
Full article ">Figure 6
<p>UCS of cement mortar under freeze-thaw cycles.</p>
Full article ">Figure 7
<p>Relationship between UCS and porosity. (<b>a</b>) Variation of UCS and porosity with freeze-thaw cycles, (<b>b</b>) Research results of Liu et al. [<a href="#B36-materials-15-07316" class="html-bibr">36</a>], (<b>c</b>) Fitting result of the deterioration model proposed by Gao et al. [<a href="#B35-materials-15-07316" class="html-bibr">35</a>].</p>
Full article ">Figure 8
<p>NMR fractal characteristics of samples in group A1.</p>
Full article ">Figure 8 Cont.
<p>NMR fractal characteristics of samples in group A1.</p>
Full article ">Figure 9
<p>Changes of <math display="inline"><semantics> <mrow> <msub> <mi>D</mi> <mrow> <mi>min</mi> </mrow> </msub> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <msub> <mi>D</mi> <mrow> <mi>max</mi> </mrow> </msub> </mrow> </semantics></math> under freeze-thaw cycles. (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mi>D</mi> <mrow> <mi>min</mi> </mrow> </msub> </mrow> </semantics></math> (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mi>D</mi> <mrow> <mi>max</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
Full article ">Figure 10
<p>The relationship between relative UCS and the change amount of the freeze-thaw factor.</p>
Full article ">Figure 11
<p>Variation of <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>W</mi> </mrow> </semantics></math> and <math display="inline"><semantics> <mrow> <mo>Δ</mo> <mi>P</mi> </mrow> </semantics></math> with freeze-thaw cycles.</p>
Full article ">Figure 12
<p>Prediction results of three models [<a href="#B29-materials-15-07316" class="html-bibr">29</a>,<a href="#B35-materials-15-07316" class="html-bibr">35</a>].</p>
Full article ">Figure 13
<p>Fitting results using data from Hu et al. [<a href="#B17-materials-15-07316" class="html-bibr">17</a>] and Gao et al. [<a href="#B35-materials-15-07316" class="html-bibr">35</a>].</p>
Full article ">
19 pages, 5844 KiB  
Article
Study on Deterioration Characteristics of Uniaxial Compression Performance and Microstructure Changes of Red-Bed Mudstone during Gaseous Water Sorption
by Hongbing Zhu, Zhenghao Fu, Fei Yu and Sai Li
Buildings 2022, 12(9), 1399; https://doi.org/10.3390/buildings12091399 - 6 Sep 2022
Cited by 2 | Viewed by 2059
Abstract
Previously conducted studies have established that gaseous water sorption of mudstone is widespread in nature. The deterioration of its uniaxial compression properties during gaseous water sorption can cause engineering problems. However, related studies were currently in the initial stage of this research direction. [...] Read more.
Previously conducted studies have established that gaseous water sorption of mudstone is widespread in nature. The deterioration of its uniaxial compression properties during gaseous water sorption can cause engineering problems. However, related studies were currently in the initial stage of this research direction. On the one hand, there were few studies on the deterioration characteristics of the uniaxial compression properties of mudstone in this process. The results might not be applicable to all projects. On the other hand, its microstructure changes in this process were unclear. Therefore, to obtain the deterioration characteristics of uniaxial compressive performance during gaseous water sorption for offering scientific reference to the geotechnical engineering of mudstone in the central Sichuan region of China, red-bed mudstone was used as a research material. A swelling test and uniaxial compression tests were carried out. To clarify microstructure changes for advancing the depth of research on the effects of gaseous water on mudstone, scanning electron microscopy (SEM) tests were performed. As a result of this study, formulas were first established that could correctly characterize the deterioration of uniaxial compressive strength (UCS) and elastic modulus when the moisture absorption rate increased. Secondly, the dependence was obtained, which was the relationship between both the UCS and elastic modulus and moisture absorption time. Finally, microstructure changes were revealed during gaseous water sorption. Full article
Show Figures

Figure 1

Figure 1
<p>Excavated natural mudstone.</p>
Full article ">Figure 2
<p>The processing of tests.</p>
Full article ">Figure 3
<p>Test device: (<b>a</b>) The swelling test; (<b>b</b>) The uniaxial compression test.</p>
Full article ">Figure 4
<p>Swelling rate curve with time.</p>
Full article ">Figure 5
<p>Stress-strain curve of the KY0-2 specimen.</p>
Full article ">Figure 6
<p>Stress-strain curves for specimens with different moisture absorption rates. note: The figure showed only the rising section of the stress-strain curve (the stage before the peak stress). The reasons for this were twofold. On the one hand, the decreasing section of the curve (the post-peak failure stage) had little influence on the purpose of the test. On the other hand, there were many curves in the graph. If all the descending sections of the curves were added, it would look like the information on the graph was cluttered and inconvenient to mark.</p>
Full article ">Figure 7
<p>UCS with different moisture absorption rates.</p>
Full article ">Figure 8
<p>Relationship between UCS and moisture absorption rate.</p>
Full article ">Figure 9
<p>Relationship between the elastic modulus and moisture absorption rate.</p>
Full article ">Figure 10
<p>Fitting curve of the relationship between UCS and time.</p>
Full article ">Figure 11
<p>Fitting curve of relationship between elastic modulus and time.</p>
Full article ">Figure 12
<p>Results of SEM before and after gaseous water sorption.</p>
Full article ">Figure 13
<p>The process of pores segmentation.</p>
Full article ">Figure 14
<p>The distribution of pores according to the size of the area. (<b>a</b>) The vertical coordinate was the percentage of number of pores (the sum of the number of pores in the corresponding area range divided by total number of pores); (<b>b</b>) The vertical coordinate was the percentage of pore area (sum of pore areas in the corresponding area range divided by total pore area).</p>
Full article ">
17 pages, 6349 KiB  
Article
The Transverse Bearing Characteristics of the Pile Foundation in a Calcareous Sand Area
by Haibo Hu, Lina Luo, Gang Lei, Jin Guo, Shaoheng He, Xunjian Hu, Panpan Guo and Xiaonan Gong
Materials 2022, 15(17), 6176; https://doi.org/10.3390/ma15176176 - 5 Sep 2022
Cited by 2 | Viewed by 1843
Abstract
Reviewing literature revealed that the studies on the bearing characteristics of pile foundations mainly focuses on clay, ordinary sand, loess, saline soil, and other areas. However, few studies on the bearing characteristics of the pile foundation in calcareous sand were conducted. Besides, existing [...] Read more.
Reviewing literature revealed that the studies on the bearing characteristics of pile foundations mainly focuses on clay, ordinary sand, loess, saline soil, and other areas. However, few studies on the bearing characteristics of the pile foundation in calcareous sand were conducted. Besides, existing traditional studies ignored the variation of soil compression modulus with depth, and the effect of void ratio on the transverse bearing characteristics of the pile foundation in a calcareous sand area were not well understood. In response of these problems, this study conducted a theoretical investigation on the transverse bearing characteristics of the pile foundation in a calcareous sand area. The transverse bearing characteristics of the pile foundation were derived based on the Pasternak foundation model and the Winkler foundation model, incorporating the heterogeneous distribution of compressive modulus with buried depth. The calculation results of the Pasternak foundation model are closer to the observed results than the Winkler foundation model. Therefore, the following research on the transverse bearing characteristics of the pile foundation in the calcareous sand area adopts the Pasternak foundation model. Then, the effects of the pile length, pile diameter, pile elastic modulus, horizontal load, bending moment, and void ratio on the transverse bearing characteristics of the pile foundation in a calcareous sand area were thoroughly analyzed. Furthermore, the difference between the transverse bearing characteristics of the pile foundation in a calcareous sand area and a quartz sand area was discussed. Results show that the horizontal displacement of the pile top in a calcareous sand area is greater than the quartz sand area under the same conditions. Full article
Show Figures

Figure 1

Figure 1
<p>Pasternak foundation model.</p>
Full article ">Figure 2
<p>Discrete analysis model of pile.</p>
Full article ">Figure 3
<p>Comparison of horizontal displacement of pile body.</p>
Full article ">Figure 4
<p>Correlation between compressive modulus and confining pressure.</p>
Full article ">Figure 5
<p>Horizontal displacement of pile body.</p>
Full article ">Figure 6
<p>Effect of pile length on horizontal displacement of pile body in calcareous sand area.</p>
Full article ">Figure 7
<p>Effect of pile diameter on horizontal displacement of pile body in calcareous sand area.</p>
Full article ">Figure 8
<p>Effect of elastic modulus of pile on horizontal displacement of pile in calcareous sand area.</p>
Full article ">Figure 9
<p>Effect of horizontal load on horizontal displacement of pile in calcareous sand area.</p>
Full article ">Figure 10
<p>Effect of bending moment on horizontal displacement of pile in calcareous sand area.</p>
Full article ">Figure 11
<p>Effect of void ratio on horizontal displacement of pile in calcareous sand area.</p>
Full article ">Figure 12
<p>Effect of pile length on horizontal displacement of pile body. (<b>a</b>) L; (<b>b</b>) 2L; (<b>c</b>) 3L.</p>
Full article ">Figure 13
<p>Effect of pile diameter on horizontal displacement of pile body. (<b>a</b>) D; (<b>b</b>) 2D; (<b>c</b>) 3D.</p>
Full article ">Figure 13 Cont.
<p>Effect of pile diameter on horizontal displacement of pile body. (<b>a</b>) D; (<b>b</b>) 2D; (<b>c</b>) 3D.</p>
Full article ">Figure 14
<p>Effect of elastic modulus of pile on horizontal displacement of pile. (<b>a</b>) E; (<b>b</b>) 2E; (<b>c</b>) 3E.</p>
Full article ">Figure 15
<p>Effect of horizontal load on horizontal displacement of pile. (<b>a</b>) H; (<b>b</b>) 2H; (<b>c</b>) 3H.</p>
Full article ">Figure 16
<p>Effect of bending moment on horizontal displacement of pile. (<b>a</b>) M; (<b>b</b>) 2M; (<b>c</b>) 3M.</p>
Full article ">Figure 17
<p>Effect of void ratio on horizontal displacement of pile. (<b>a</b>) e; (<b>b</b>) 1.1e; (<b>c</b>) 1.2e.</p>
Full article ">Figure 17 Cont.
<p>Effect of void ratio on horizontal displacement of pile. (<b>a</b>) e; (<b>b</b>) 1.1e; (<b>c</b>) 1.2e.</p>
Full article ">
15 pages, 2012 KiB  
Article
Microseismic Source Location Method and Application Based on NM-PSO Algorithm
by Ze Liao, Tao Feng, Weijian Yu, Dongge Cui and Genshui Wu
Appl. Sci. 2022, 12(17), 8796; https://doi.org/10.3390/app12178796 - 1 Sep 2022
Cited by 3 | Viewed by 1879
Abstract
Microseismic source location is the core of microseismic monitoring technology in coal mining; it is also the advantage of microseismic monitoring technology compared with other monitoring methods. The source location method directly determines the accuracy and stability of the source location results. Based [...] Read more.
Microseismic source location is the core of microseismic monitoring technology in coal mining; it is also the advantage of microseismic monitoring technology compared with other monitoring methods. The source location method directly determines the accuracy and stability of the source location results. Based on the problem of non-benign arrays of microseismic monitoring sensors in the coal mining process, a fast location method of microseismic source in coal mining based on the NM-PSO algorithm is proposed. The core idea of the NM-PSO algorithm is to use the particle swarm optimization (PSO) algorithm for global optimization, reduce the size of the solution space and provide the optimized initial value for the Nelder Mead simplex algorithm (NM), and then use the fast iteration characteristics of the NM algorithm to accelerate the convergence of the model. The NM-PSO algorithm is analyzed by an example and verified by the microseismic source location engineering. The NM-PSO algorithm has a significant improvement in the source location accuracy. The average location errors in all directions are (5.65 m, 5.01 m, and 7.21 m), all Within the acceptable range, and they showed good universality and stability. The proposed NM-PSO algorithm can provide a general fast seismic source localization method for different sensor array deployment methods, which significantly improves the stability and result in the accuracy of the seismic source localization algorithm and has good application value; this method can provide new ideas for research in microseismic localization in coal mining. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of microseismic positioning principle.</p>
Full article ">Figure 2
<p>Principle of TDOA source location.</p>
Full article ">Figure 3
<p>Flow chart of NM-PSO algorithm.</p>
Full article ">Figure 4
<p>Schematic diagram of sensor layout array.</p>
Full article ">Figure 5
<p>Comparison of positioning errors.</p>
Full article ">Figure 5 Cont.
<p>Comparison of positioning errors.</p>
Full article ">Figure 6
<p>Flow chart of microseismic monitoring.</p>
Full article ">
15 pages, 5960 KiB  
Article
Development of Damage Type Viscoelastic Ontological Model for Soft and Hard Materials under High-Strain-Rate Conditions
by Wei Liu, Xiangyun Xu and Chaomin Mu
Appl. Sci. 2022, 12(17), 8407; https://doi.org/10.3390/app12178407 - 23 Aug 2022
Cited by 5 | Viewed by 1690
Abstract
By improving the ZWT model, a principal structure model applicable to both soft and hard materials under dynamic loading conditions was obtained. Dynamic mechanical experiments were conducted using SHPB to obtain stress–strain curves for coal rock and foam concrete. The ZWT intrinsic model [...] Read more.
By improving the ZWT model, a principal structure model applicable to both soft and hard materials under dynamic loading conditions was obtained. Dynamic mechanical experiments were conducted using SHPB to obtain stress–strain curves for coal rock and foam concrete. The ZWT intrinsic model was simplified according to the dynamic impact characteristics of concrete, and the intrinsic model was established by introducing macroscopic damage quantity D and correction factor δ. The stress–strain curves of coal rock, foamed concrete, steel fiber concrete, granite, lightweight foamed concrete, and EPS concrete at different strain rates were used to validate the present constitutive model and prove the correctness of the model. Full article
Show Figures

Figure 1

Figure 1
<p>The “Zhu–Wang–Tang” constitutive model.</p>
Full article ">Figure 2
<p>The “Zhu–Wang–Tang” model simplified.</p>
Full article ">Figure 3
<p>Equivalent constitutive model.</p>
Full article ">Figure 4
<p>Drilling of raw coal test pieces.</p>
Full article ">Figure 5
<p>Raw coal test pieces.</p>
Full article ">Figure 6
<p>Foam concrete specimen.</p>
Full article ">Figure 7
<p>Diagram of the experimental setup.</p>
Full article ">Figure 8
<p>Power system.</p>
Full article ">Figure 9
<p>Semiconductor strain gauge.</p>
Full article ">Figure 10
<p>DHHP-20 ultra-dynamic strain gauge.</p>
Full article ">Figure 11
<p>Stress wave data analysis and processing software.</p>
Full article ">Figure 12
<p>Dynamic stress balance verification.</p>
Full article ">Figure 13
<p>Coal rock stress–strain curve.</p>
Full article ">Figure 14
<p>Stress–strain curve of foam concrete.</p>
Full article ">Figure 15
<p>Coal rock fitting curve.</p>
Full article ">Figure 16
<p>Foam concrete fitting curve.</p>
Full article ">Figure 17
<p>Curve fitting. (<b>a</b>) Steel fiber reinforced concrete; (<b>b</b>) Granite; (<b>c</b>) Lightweight foramed concrete; (<b>d</b>) EPS concrete.</p>
Full article ">
19 pages, 7330 KiB  
Article
Wavelet Energy Evolution Characteristics of Acoustic Emission Signal under True-Triaxial Loading during the Rockburst Test
by Chuanyu Hu, Fuding Mei and Wakeel Hussain
Appl. Sci. 2022, 12(15), 7786; https://doi.org/10.3390/app12157786 - 2 Aug 2022
Cited by 1 | Viewed by 1513
Abstract
The rockburst simulation test is conducted by utilizing a mineral-containing marble specimen. The loading condition is set to the three directions, each loading on five surfaces except for a single free surface. The whole test procedure is monitored in real time by using [...] Read more.
The rockburst simulation test is conducted by utilizing a mineral-containing marble specimen. The loading condition is set to the three directions, each loading on five surfaces except for a single free surface. The whole test procedure is monitored in real time by using a PCI-II acoustic emission monitoring system and a high-speed camera. According to the test outcomes, rockburst is a process in which energy is rapidly released from the free surface. Rock block and rock plate are buckled and ejected from the free surface and a severe rockburst process is accompanied by spray rock powder. An explosion sound can be heard during the process, which can be analyzed by signal processing techniques. The failure mode of the specimen is a splitting-shearing composite failure, and the free surface becomes a rockburst destruction surface. A V-type rockburst pit is formed in the ejection area. The effective acoustic emission signal of the whole test process is decomposed and reconstructed using five-layer wavelets to produce six frequency band sub-signals. In addition, the wavelet energy and its energy distribution coefficients are assessed for various frequency bands, and the proportion of each dominant frequency band within each period is computed. Finally, it was found that the dominant frequency band is 125~250 kHz, while the suboptimal frequency band is 250~500 kHz. The succeeding features are noticed to be used as predicted features for the rockburst disaster. Namely, acoustic emission signals arise in large numbers and the energy distribution coefficient of the dominant frequency band concentrates above 0.4. The proportion of dominant frequency band appears in continuous valley type and keeps below 80%, while the proportion of suboptimal frequency band appears in continuous peak type and keeps above 20%. Full article
Show Figures

Figure 1

Figure 1
<p>Test specimen.</p>
Full article ">Figure 2
<p>Test equipment.</p>
Full article ">Figure 3
<p>Test specimen loading way.</p>
Full article ">Figure 4
<p>Test loading path.</p>
Full article ">Figure 5
<p>Flow chart.</p>
Full article ">Figure 6
<p>Rockburst test phenomenon. (<b>a</b>) Before rockburst; (<b>b</b>) Small rock fragments ejecting; (<b>c</b>) Rock plate splitting and peeling; (<b>d</b>) Rock plate buckling ejection; (<b>e</b>) Rockburst violence occurring; (<b>f</b>) After rockburst.</p>
Full article ">Figure 6 Cont.
<p>Rockburst test phenomenon. (<b>a</b>) Before rockburst; (<b>b</b>) Small rock fragments ejecting; (<b>c</b>) Rock plate splitting and peeling; (<b>d</b>) Rock plate buckling ejection; (<b>e</b>) Rockburst violence occurring; (<b>f</b>) After rockburst.</p>
Full article ">Figure 7
<p>Results of the rockburst test.</p>
Full article ">Figure 8
<p>Removing zero processing to the original waveform. (<b>a</b>) Before processing; (<b>b</b>) After processing.</p>
Full article ">Figure 9
<p>Five-layer wavelet decomposition structure tree.</p>
Full article ">Figure 10
<p>The 3546th effective acoustic emission signal. (<b>a</b>) The original AE signal waveform; (<b>b</b>) AE signal reconstructed waveform of each frequency band.</p>
Full article ">Figure 10 Cont.
<p>The 3546th effective acoustic emission signal. (<b>a</b>) The original AE signal waveform; (<b>b</b>) AE signal reconstructed waveform of each frequency band.</p>
Full article ">Figure 11
<p>Acoustic emission full-time waveform.</p>
Full article ">Figure 12
<p>Evolution process of the energy distribution coefficients.</p>
Full article ">Figure 13
<p>Evolution process of the dominant frequency bands’ proportions.</p>
Full article ">Figure 14
<p>Characteristics of the AE wavelet energy evolution.</p>
Full article ">
21 pages, 4785 KiB  
Article
Numerical Analysis of Microcrack Propagation Characteristics and Influencing Factors of Serrated Structural Plane
by Xing Zhang, Hang Lin, Jianxin Qin, Rihong Cao, Shaowei Ma and Huihua Hu
Materials 2022, 15(15), 5287; https://doi.org/10.3390/ma15155287 - 31 Jul 2022
Cited by 5 | Viewed by 1611
Abstract
The serrated structural plane is the basic unit of structural plane morphology. However, the understanding of its internal stress distribution, failure mode and crack evolution law was not clear enough in previous studies. In this paper, the shear mechanical properties of the serrated [...] Read more.
The serrated structural plane is the basic unit of structural plane morphology. However, the understanding of its internal stress distribution, failure mode and crack evolution law was not clear enough in previous studies. In this paper, the shear mechanical properties of the serrated structural planes were studied by numerical simulation, and the crack evolution law of the serrated structural planes and the effects of four microscopic parameters on the shear properties were analyzed. The results show that: (1) the number of microcracks increases with the increase in normal stress; the crack expansion rate is slow before the shear stress reaches the peak. After the shear stress reaches the peak, the crack expansion rate continues to increase, and the microcracks keep sprouting and expanding, and the number of microcracks tends to stabilize when the shear stress reaches the residual shear strength. (2) The particle contact stiffness ratio kn/ks and parallel bond stiffness ratio kn/ks were negatively correlated with the shear strength; and the particle contact modulus E and parallel bond modulus E were positively correlated with the shear strength. As the particle contact modulus E and parallel bond modulus E increase, the peak shear displacement gradually decreases. The parallel bond stiffness ratio kn/ks has a negative correlation with the peak shear displacement. This study is expected to provide theoretical guidance for the microscopic parameter calibration and shear mechanical analysis of serrated structural planes. (3) Several XGBoost, WOA-XGBoost, and PSO-XGBoost algorithms are introduced to construct the quantitative prediction model, and the comparative analysis found that WOA-XGBoost has the best fitting effect and can be used for the prediction of shear strength. When using this model to calculate the weight shares of micro-parameters, it was found that kn/ks has the greatest influence on shear strength, followed by E; E and kn/ks had the least influence. Full article
Show Figures

Figure 1

Figure 1
<p>The distribution of one serrated structural plane of a slope.</p>
Full article ">Figure 2
<p>The numerical mode of PFC2D in a serrated structural plane (1–8 are the numbers of the walls respectively).</p>
Full article ">Figure 3
<p>Numerical simulation results and laboratory testing results [<a href="#B39-materials-15-05287" class="html-bibr">39</a>] with different normal stress of serrated structural plane. (<b>a</b>) Normal stress = 0.4 MPa. (<b>b</b>) Normal stress = 0.8 MPa. (<b>c</b>) Normal stress = 1.2 MPa. (<b>d</b>) Normal stress = 1.6 MPa. (<b>e</b>) Normal stress = 2.0 MPa.</p>
Full article ">Figure 4
<p>The relationship between the number of microcracks and shear displacement.</p>
Full article ">Figure 5
<p>Distribution of cracks expansion and contact force with different shearing displacement. (<b>a</b>) Shear displacement = 1 mm. (<b>b</b>) Shear displacement = 2 mm. (<b>c</b>) Shear displacement = 3 mm. (<b>d</b>) Shear displacement = 4 mm. (<b>e</b>) Shear displacement = 5 mm. (<b>f</b>) Shear displacement = 10 mm.</p>
Full article ">Figure 5 Cont.
<p>Distribution of cracks expansion and contact force with different shearing displacement. (<b>a</b>) Shear displacement = 1 mm. (<b>b</b>) Shear displacement = 2 mm. (<b>c</b>) Shear displacement = 3 mm. (<b>d</b>) Shear displacement = 4 mm. (<b>e</b>) Shear displacement = 5 mm. (<b>f</b>) Shear displacement = 10 mm.</p>
Full article ">Figure 5 Cont.
<p>Distribution of cracks expansion and contact force with different shearing displacement. (<b>a</b>) Shear displacement = 1 mm. (<b>b</b>) Shear displacement = 2 mm. (<b>c</b>) Shear displacement = 3 mm. (<b>d</b>) Shear displacement = 4 mm. (<b>e</b>) Shear displacement = 5 mm. (<b>f</b>) Shear displacement = 10 mm.</p>
Full article ">Figure 6
<p>The shear stress and number of cracks in the serrated structural plane. (a, b, c, d, e, and f correspond to the monitoring points where the shear displacements are 1 mm, 2 mm, 3 mm, 4 mm, 5 mm and 10 mm, respectively).</p>
Full article ">Figure 7
<p>Shear stress–shear displacement curves of corresponding different parallel bond stiffness ratios.</p>
Full article ">Figure 8
<p>The corresponding shear stress–shear displacement relationships of different particle contact stiffness ratios.</p>
Full article ">Figure 9
<p>The shear stress–shear displacement curve under different values of particle contact modulus.</p>
Full article ">Figure 10
<p>The corresponding shear stress–shear displacement curves with different parallel bond moduli.</p>
Full article ">Figure 11
<p>Effects of micro-parameters on shear strength.</p>
Full article ">Figure 12
<p>Relationships between micro-parameters and peak shear displacement.</p>
Full article ">Figure 13
<p>The comparison between the test data and predicted data being used by different models: (<b>a</b>) XGBoost, (<b>b</b>) WOA-XGBoost, (<b>c</b>) PSO-XGBoost.</p>
Full article ">Figure 13 Cont.
<p>The comparison between the test data and predicted data being used by different models: (<b>a</b>) XGBoost, (<b>b</b>) WOA-XGBoost, (<b>c</b>) PSO-XGBoost.</p>
Full article ">Figure 14
<p>Weight shares of different microscopic parameters for shear strength.</p>
Full article ">
22 pages, 10385 KiB  
Article
Deformation and Force Analysis of Wood-Piled Island Cofferdam Based on Equivalent Bending Stiffness Principle
by Shi Chen, Yixian Wang, Yonghai Li, Xian Li, Panpan Guo, Weichao Hou and Yan Liu
Buildings 2022, 12(8), 1104; https://doi.org/10.3390/buildings12081104 - 27 Jul 2022
Cited by 2 | Viewed by 2209
Abstract
This paper analyses the deformation and force behavior of a wood-piled island cofferdam based on the principle of equivalent bending stiffness. The horizontal deformation and bending moments in wood piles and the axial stress in tension bars on top of piles were both [...] Read more.
This paper analyses the deformation and force behavior of a wood-piled island cofferdam based on the principle of equivalent bending stiffness. The horizontal deformation and bending moments in wood piles and the axial stress in tension bars on top of piles were both analyzed by the finite difference (FD) method. Except for the analysis of the cofferdam construction process, the influence of the pile length, the dam width, the tension bar interval, and the pile interval, among the commonly adopted parameters, were detailly examined in numerical simulations. In addition, a reinforced wood-piled cofferdam model by steel pipe piles has been established to quantify the effect of reinforcement. It was found that the dewatering inside the cofferdam was detrimental to cofferdam stability. The pile deformation reached maxima (roughly 0.6% of the pile length) at solidifying stage after dewatering. The changing trend of the cofferdam structure force within a safe district was consistent with the displacement. The dam width had a vital effect on the stability of the cofferdam, especially on the horizontal deformation. The steel pipe pile reinforcement scheme performed better in further deformation control, providing a new idea for island-type cofferdams with rigorous structural deformation control. Full article
Show Figures

Figure 1

Figure 1
<p>Equivalence of cofferdam structure.</p>
Full article ">Figure 2
<p>Equivalent of wood piles.</p>
Full article ">Figure 3
<p>Equivalent of steel pipe piles.</p>
Full article ">Figure 4
<p>Equivalent of a combination of steel pipe piles and wood piles.</p>
Full article ">Figure 5
<p>Plan view of the project.</p>
Full article ">Figure 6
<p>Double row wood pile structure.</p>
Full article ">Figure 7
<p>Construction steps.</p>
Full article ">Figure 8
<p>Mesh of the numerical model.</p>
Full article ">Figure 9
<p>Horizontal displacement contours of piles at different stages (unit: m).</p>
Full article ">Figure 10
<p>Horizontal displacement curve of piles at different stages.</p>
Full article ">Figure 11
<p>Bending moment of piles at different stages.</p>
Full article ">Figure 12
<p>Pile horizontal displacement of different pile length conditions.</p>
Full article ">Figure 13
<p>Pile bending moment of different pile length conditions.</p>
Full article ">Figure 14
<p>Tension bar axial stress of different pile length conditions.</p>
Full article ">Figure 15
<p>Pile horizontal displacement of different dam width conditions.</p>
Full article ">Figure 16
<p>Pile bending moment of different dam width conditions.</p>
Full article ">Figure 17
<p>Tension bar axial stress of different dam width conditions.</p>
Full article ">Figure 18
<p>Pile horizontal displacement of different tension bar interval conditions.</p>
Full article ">Figure 19
<p>Pile bending moment of different tension bar interval conditions.</p>
Full article ">Figure 20
<p>Tension bar axial stress of its different interval conditions.</p>
Full article ">Figure 21
<p>Pile horizontal displacement of wood pile interval conditions.</p>
Full article ">Figure 22
<p>Pile bending moment of wood pile interval conditions.</p>
Full article ">Figure 23
<p>Tension bar axial stress of wood pile interval conditions.</p>
Full article ">Figure 24
<p>Steel pipe pile reinforced cofferdam structure.</p>
Full article ">Figure 25
<p>Horizontal displacement of reinforced piles.</p>
Full article ">Figure 26
<p>Comparison of the horizontal displacement between reinforced piles and double-row wood piles.</p>
Full article ">Figure 27
<p>Comparison of the internal force between reinforced piles and double-row wood piles.</p>
Full article ">
14 pages, 39785 KiB  
Article
Physical and Thermal Properties Analysis of Hematite for Thermal Heat Storage
by Andreia Santos, Fernando Almeida and Fernando Rocha
Materials 2022, 15(13), 4648; https://doi.org/10.3390/ma15134648 - 1 Jul 2022
Cited by 3 | Viewed by 2140
Abstract
Energy sustainability represents an important research topic for aiding decreasing energy dependence and slowing down climate changes. In this context, solutions using thermal energy storage through rock start to emerge, due to its natural benefits, when compared to more polluting alternatives. To understand [...] Read more.
Energy sustainability represents an important research topic for aiding decreasing energy dependence and slowing down climate changes. In this context, solutions using thermal energy storage through rock start to emerge, due to its natural benefits, when compared to more polluting alternatives. To understand whether a rock material can be considered a good thermal energy storage material for such solutions, it is necessary to evaluate the physical, chemical and thermal properties of such materials. Therefore, it becomes essential to understand how heat propagates in the rock and how voids influence the thermal properties. To achieve these goals, hematite ore from Moncorvo, Northeastern Portugal was used, in particular, to study the effect of grain size on thermal properties for three different sized lots. Chemical and physical changes between heated and unheated lots were detected using X-ray diffraction and particle size, as well as X-ray fluorescence analysis. Regarding thermal properties, a hot wire method approach was used with seven thermocouples. Additionally, a thermal inversion model to simulate the heat exchanges was also proposed, allowing changing the properties of the constituents, to fit the theoretical and experimental temperature curve. Furthermore, the model reveals how heat propagates inside the reservoir filled with hematite ore. Full article
Show Figures

Figure 1

Figure 1
<p>Location of the Cabeço da Mua hematite ore sampling area, Moncorvo. Images obtained from Google Maps.</p>
Full article ">Figure 2
<p>Longitudinal section (N−S) on Moncorvo’s synchlorium with overlapping interpretation of geophysical data. Adapted from [<a href="#B31-materials-15-04648" class="html-bibr">31</a>].</p>
Full article ">Figure 3
<p>Hematite ore sample extraction area, located on the slopes of Cabeço de Mua, Moncorvo: (<b>a</b>) sample collection site along a 100 m stretch; (<b>b</b>) hematite ore in situ.</p>
Full article ">Figure 4
<p>Different lots of hematite ore: (<b>a</b>) undersize—US; (<b>b</b>) total distribution—TD; (<b>c</b>) oversize—OS.</p>
Full article ">Figure 5
<p>Observation of the polished surface under the microscope with transmitted and reflected light, in parallel and crossed niches. A matrix of hematite (small-grained) is observed, containing quartz and muscovite. The amount of hematite is about twice that of quartz.</p>
Full article ">Figure 6
<p>Percentage curves of passes according to the opening of the sieves of all the samples.</p>
Full article ">Figure 7
<p>XRD powder diffraction analysis with identified peaks: (<b>a</b>) TQ sample not subjected to heating/cooling cycles; (<b>b</b>) TQ sample subjected to heating/cooling cycles.</p>
Full article ">Figure 8
<p>Reservoir overview: (<b>a</b>) experimental reservoir filled with the hematite ore; (<b>b</b>) theoretical model developed in Matlab with the inversion points; (<b>c</b>) temperature distribution in the reservoir over time.</p>
Full article ">Figure 9
<p>Theoretical and experimental curves for a heating and cooling cycle. The crosses represent the temperatures returned by the software and the line the actual temperatures: (<b>a</b>) temperature graph for lot TQ; (<b>b</b>) temperature graph for lot OS; (<b>c</b>) temperature graph for lot US.</p>
Full article ">
17 pages, 3523 KiB  
Article
Influence of Morphology Characteristics on Shear Mechanical Properties of Sawtooth Joints
by Huihua Hu, Xing Zhang, Jianxin Qin and Hang Lin
Buildings 2022, 12(7), 886; https://doi.org/10.3390/buildings12070886 - 22 Jun 2022
Cited by 3 | Viewed by 1908
Abstract
The interface problem exists widely in building. Joints are interfaces of rock mass structures. To further study the influence of morphological characteristics on the shear mechanical properties of sawtooth joints, this paper prepared rock-like materials based on the similarity principle and carried out [...] Read more.
The interface problem exists widely in building. Joints are interfaces of rock mass structures. To further study the influence of morphological characteristics on the shear mechanical properties of sawtooth joints, this paper prepared rock-like materials based on the similarity principle and carried out direct shear tests of sawtooth joints. The results showed that: (1) the peak shear displacement of joints first increases and then decreases with increasing normal stress, but the normal trend of stress during turning is different under different sawtooth angles. When the sawtooth angle of the joints is small, the decrease in shear stress between shear strength and residual shear strength is not obvious, and the rate of decrease is also small. (2) The shear strength of joints is positively correlated with normal stress. Using the Mohr–Coulomb criterion to analyze the shear strength of joints, it was found that the cohesion c and internal friction angle α of joints increased nonlinearly with increasing sawtooth angle, but their increasing trends were different. By introducing the function relation between cohesion, internal friction angle, and sawtooth angle into the classical shear strength equation, an empirical equation for the shear strength of joints was established in consideration of sawtooth angle. (3) There are two modes of shear failure for serrated joints: the “saw-toothed sliding gnawing failure mechanism” (SSG) and the “tensile fracture mechanism” (TFM). In the SSG, the shear failure mode of joints evolves in a slipping–gnawing–complete gnawing mechanism with increasing sawtooth angle and normal stress. The TFM mainly occurs at high sawtooth angles. This study provides a theoretical reference for the prediction and prevention of geological disasters. Full article
Show Figures

Figure 1

Figure 1
<p>Landslide and collapse caused by joints.</p>
Full article ">Figure 2
<p>Test specimens. (<b>a</b>) Lower test block of joints; (<b>b</b>) Prepared specimens.</p>
Full article ">Figure 3
<p>Shear stress–shear displacement curves of joints with different sawtooth angles: (<b>a</b>) Sawtooth angle of 0°; (<b>b</b>) Sawtooth angle of 10°; (<b>c</b>) Sawtooth angle of 20°; (<b>d</b>) Sawtooth angle of 30°; (<b>e</b>) Sawtooth angle of 45°.</p>
Full article ">Figure 3 Cont.
<p>Shear stress–shear displacement curves of joints with different sawtooth angles: (<b>a</b>) Sawtooth angle of 0°; (<b>b</b>) Sawtooth angle of 10°; (<b>c</b>) Sawtooth angle of 20°; (<b>d</b>) Sawtooth angle of 30°; (<b>e</b>) Sawtooth angle of 45°.</p>
Full article ">Figure 3 Cont.
<p>Shear stress–shear displacement curves of joints with different sawtooth angles: (<b>a</b>) Sawtooth angle of 0°; (<b>b</b>) Sawtooth angle of 10°; (<b>c</b>) Sawtooth angle of 20°; (<b>d</b>) Sawtooth angle of 30°; (<b>e</b>) Sawtooth angle of 45°.</p>
Full article ">Figure 4
<p>Shear strength under different normal stresses.</p>
Full article ">Figure 5
<p>Relationship between cohesion and sawtooth angle.</p>
Full article ">Figure 6
<p>Relationship between internal friction angle and sawtooth angle.</p>
Full article ">Figure 7
<p>Relationship between shear strength and sawtooth angle.</p>
Full article ">Figure 8
<p>Influence of sawtooth angle on the internal friction angle.</p>
Full article ">Figure 9
<p>Saw-toothed sliding gnawing failure mechanism of joints. (<b>a</b>) Slip failure at 10° sawtooth angle under 0.4 MPa normal stress; (<b>b</b>) Slip gnawing failure at 20° sawtooth angle under 1.2 MPa normal stress; (<b>c</b>) Complete gnawing failure at 45° sawtooth angle under 2.0 MPa normal stress.</p>
Full article ">Figure 10
<p>Shear mechanical model of the sawtooth joint.</p>
Full article ">Figure 11
<p>Tensile fracture mechanism. (<b>a</b>) Tensile crack of 45° sawtooth angle under 0.8 MPa normal stress. (<b>b</b>) Tensile crack of 30° sawtooth angle under 1.6 MPa normal stress.</p>
Full article ">Figure 12
<p>Stress diagram of sawtooth.</p>
Full article ">
18 pages, 5842 KiB  
Article
Numerical Simulation of Flood Intrusion Process under Malfunction of Flood Retaining Facilities in Complex Subway Stations
by Zhiyu Lin, Shengbin Hu, Tianzhong Zhou, Youxin Zhong, Ye Zhu, Lei Shi and Hang Lin
Buildings 2022, 12(6), 853; https://doi.org/10.3390/buildings12060853 - 19 Jun 2022
Cited by 14 | Viewed by 2976
Abstract
In recent years, heavy rain and waterlogging accidents in subway stations have occurred many times around the world. With the comprehensive development trend of underground space, the accidents caused by flood flow intruding complex subway stations and other underground complexes in extreme precipitation [...] Read more.
In recent years, heavy rain and waterlogging accidents in subway stations have occurred many times around the world. With the comprehensive development trend of underground space, the accidents caused by flood flow intruding complex subway stations and other underground complexes in extreme precipitation disasters will be lead to more serious casualties and property damage. Therefore, it is necessary to conduct numerical simulation of flood intrusion process under malfunction of flood retaining facilities in complex subway stations. In order to prevent floods from intruding subway stations and explore coping strategies, in this study, the simulation method was used to study the entire process of flood intrusion into complex subway stations when the flood retaining facilities fail in extreme rain and flood disasters that occur once-in-a-century. The three-dimensional numerical simulation model was constructed by taking a subway interchange station with a property development floor in Nanning as a prototype. Based on the Volume of Fluid (VOF) model method, the inundated area in the subway station during the process of flood intrusion from the beginning to the basic stability was simulated, and it was found that the property development floor has serious large-scale water accumulation under extreme rainfall conditions. Through the dynamic monitoring of the flood water level depth at important positions such as the entrances of the evacuation passages, and the analysis of the influence of the design structure and location distribution of different passages on the personnel evacuation plan, it was found that the deep water accumulation at the entrances of the narrow, long, and multi-run emergency safety passages are not conducive to the evacuation of personnel. Finally, the flow of flood water into the subway tunnel through the subway station was calculated. The research results provide certain reference and guidance for the safety design of subway stations under extreme rainfall climatic conditions. Full article
Show Figures

Figure 1

Figure 1
<p>The completed construction investment of subways in mainland China from 2011 to 2021.</p>
Full article ">Figure 2
<p>Location of the target study station.</p>
Full article ">Figure 3
<p>Plane design of the target study station.</p>
Full article ">Figure 4
<p>Schematic diagram of the floors of the target study station.</p>
Full article ">Figure 5
<p>Geometric model diagram. (<b>a</b>) Overall elevation of the geometric model, (<b>b</b>) floor plan of line 2, and (<b>c</b>) floor plan of line 5.</p>
Full article ">Figure 5 Cont.
<p>Geometric model diagram. (<b>a</b>) Overall elevation of the geometric model, (<b>b</b>) floor plan of line 2, and (<b>c</b>) floor plan of line 5.</p>
Full article ">Figure 6
<p>Meshing diagram of the target study station.</p>
Full article ">Figure 7
<p>Schematic diagram of the evacuation passages.</p>
Full article ">Figure 8
<p>Schematic diagram of boundary conditions.</p>
Full article ">Figure 9
<p>Flood inundated area of the subway station. (<b>a</b>) Contour of water volume fraction at 10 s, (<b>b</b>) contour of water volume fraction at 30 s, (<b>c</b>) contour of water volume fraction at 60 s, (<b>d</b>) contour of water volume fraction at 120 s, (<b>e</b>) contour of water volume fraction at 300 s, (<b>f</b>) contour of water volume fraction at 600 s.</p>
Full article ">Figure 9 Cont.
<p>Flood inundated area of the subway station. (<b>a</b>) Contour of water volume fraction at 10 s, (<b>b</b>) contour of water volume fraction at 30 s, (<b>c</b>) contour of water volume fraction at 60 s, (<b>d</b>) contour of water volume fraction at 120 s, (<b>e</b>) contour of water volume fraction at 300 s, (<b>f</b>) contour of water volume fraction at 600 s.</p>
Full article ">Figure 10
<p>Location map of monitoring points on the property development floor.</p>
Full article ">Figure 11
<p>Water depth at monitoring points on the property development floor as a function of time.</p>
Full article ">Figure 12
<p>Water depth growth rate at monitoring points on the property development floor as a function of time.</p>
Full article ">Figure 13
<p>Pedestrian moving velocity at the entrances of exit passages as a function of time.</p>
Full article ">Figure 14
<p>Water depth at the entrances of emergency safety passages as a function of time.</p>
Full article ">Figure 15
<p>Volume rendering of accumulated water in the Exit 4 passage.</p>
Full article ">Figure 16
<p>Flood inflow and outflow relationship diagram.</p>
Full article ">
27 pages, 8004 KiB  
Article
Mechanical Properties and Acoustic Emission Characteristics of Anchored Structure Plane with Different JRC under Direct Shear Test
by Su Li, Hang Lin, Jingjing Feng, Rihong Cao and Huihua Hu
Materials 2022, 15(12), 4169; https://doi.org/10.3390/ma15124169 - 12 Jun 2022
Cited by 11 | Viewed by 2179
Abstract
Rock mass, the heterogeneous natural material composed of rock and discontinuities, is an important part of engineering construction. Discontinuities affect the mechanical properties of natural rock mass and further threaten the stability of rock engineering. To study the failure characteristics of anchored structure [...] Read more.
Rock mass, the heterogeneous natural material composed of rock and discontinuities, is an important part of engineering construction. Discontinuities affect the mechanical properties of natural rock mass and further threaten the stability of rock engineering. To study the failure characteristics of anchored structure plane with different JRC, jointed specimens with four different JRC were fabricated by pouring cement mortar. Specimens were tested under four different normal loads to figure out how JRC and anchorage angle affect the mechanical properties of anchored structure plane. Besides, acoustic emission (AE) testing technology was adopted to explore the AE characteristics of anchored structural plane under shearing. The results showed that there exists a positive correlation between the peak shear strength and JRC. The undulation shape of structural plane led to an obvious downward trend in the strain softening stage of the structural plane with JRC of 6–8 and 18–20. When the anchorage angle ranged from 45° to 60°, the potentiation of bolt was the most significant. Based on the AE results, the larger the normal stress, the more likely the cumulative count curves were to enter the fast growth phase before the peak. The characteristics of b-value curves are mainly related to the topography of structural planes and whether the bolt is deformed. In the direct shear test, the cumulative proportion of shear cracks was more than 85%, which is much higher than that of tensile cracks. The variation of cumulative tensile cracks goes through three stages: slow growth, rapid growth, and slow growth. Compared with the unanchored structural plane, the variation range of real-time tensile cracks of the anchored structural plane is large, and sometimes the proportion of real-time tensile cracks may reach 80%. Full article
Show Figures

Figure 1

Figure 1
<p>Extraction process of JRC profile coordinates. (<b>a</b>) standard JRC profile with value of 12-14 (<b>b</b>) basic gray image (<b>c</b>) gray matrix and intensity matrix.</p>
Full article ">Figure 2
<p>The realization process of resin plates recorded with the information of JRC.</p>
Full article ">Figure 3
<p>Fabrication of specimens with different JRC.</p>
Full article ">Figure 4
<p>The diagrammatic sketch of specimens in this study.</p>
Full article ">Figure 5
<p>The arrangement of experimental devices. (<b>a</b>) AE monitoring system (<b>b</b>) Loading platform (<b>c</b>) Data acquisition system.</p>
Full article ">Figure 6
<p>Final failure modes: (<b>a</b>) cement mortar, (<b>b</b>) sandstone-1 (<b>c</b>) sandstone-2.</p>
Full article ">Figure 7
<p>Fitting curves of shear strength parameters of unanchored structural planes with different JRC.</p>
Full article ">Figure 8
<p>Shear stress-displacement curves of anchored structural planes under different normal stress: (<b>a</b>) σ = 2 MPa, (<b>b</b>) σ = 3 MPa, (<b>c</b>) σ = 4 MPa, (<b>d</b>) σ = 5 Mpa (specimen ID: DS-ab-α-σ, where DS represents direct shear experiment, ab represents the range of JRC, α means the anchorage angle, and σ means the normal stress).</p>
Full article ">Figure 9
<p>Shear stress-displacement curves of anchored structural planes with different JRC: (<b>a</b>) JRC = 0–2, (<b>b</b>) JRC = 6–8, (<b>c</b>) JRC = 12–14, (<b>d</b>) JRC = 18–20 (Specimen ID: DS-ab-α-σ, where DS represents direct shear experiment, ab represents the range of JRC, α means the anchorage angle, and σ means the normal stress).</p>
Full article ">Figure 10
<p>Relationship between shear strength and anchorage angle: (<b>a</b>) σ = 2 MPa, (<b>b</b>) σ = 3 MPa, (<b>c</b>) σ = 4 MPa, (<b>d</b>) σ = 5 Mpa.</p>
Full article ">Figure 11
<p>The variation trend of ring-down count and shear stress with time: (<b>a</b>) DS-02-30-2, (<b>b</b>) DS-02-60-5.</p>
Full article ">Figure 12
<p><span class="html-italic">b</span>-value curves of unanchored structural planes with different JRC under shearing: (<b>a</b>) DS-02-0-2, (<b>b</b>) DS-68-0-2, (<b>c</b>) DS-1214-0-2, (<b>d</b>) DS-1820-0-2, (<b>e</b>) DS-02-0-5, (<b>f</b>) DS-68-0-5, (<b>g</b>) DS-1214-0-5, and (<b>h</b>) DS-1820-0-5 (specimen ID: DS-ab-α-σ, where DS represents direct shear experiment, ab represents the range of JRC, α means the anchorage angle, and σ means the normal stress).</p>
Full article ">Figure 13
<p><span class="html-italic">b</span>-value curves of anchored structural planes with different JRC under shearing: (<b>a</b>) DS-02-60-2, (<b>b</b>) DS-68-60-2, (<b>c</b>) DS-1214-60-2, and (<b>d</b>) DS-1820-60-2 (specimen ID: DS-ab-α-σ, where DS represents direct shear experiment, ab represents the range of JRC, α means the anchorage angle, and σ means the normal stress).</p>
Full article ">Figure 14
<p><span class="html-italic">b</span>-value curves of anchored structural planes with different anchorage angles under shearing: (<b>a</b>) DS-02-30-2, (<b>b</b>) DS-02-45-2, (<b>c</b>) DS-02-60-2, and (<b>d</b>) DS-02-90-2 (specimen ID: DS-ab-α-σ, where DS represents direct shear experiment, ab represents the range of JRC, α means the anchorage angle, and σ means the normal stress).</p>
Full article ">Figure 15
<p>RA-AF distribution of unanchored structural planes. (<b>a</b>) DS-02-0-2 (<b>b</b>) DS-68-0-2 (<b>c</b>) DS-1214-0-2 (<b>d</b>) DS-1820-0-2 (<b>e</b>) DS-02-0-5 (<b>f</b>) DS-68-0-5 (<b>g</b>) DS-1214-0-5 (<b>h</b>) DS-1820-0-5.</p>
Full article ">Figure 16
<p>Variation trend of cumulative proportion of shear cracks and tensile cracks with time. ((<b>A</b>) (<b>a</b>) DS-02-0-2 (<b>b</b>) DS-68-0-2 (<b>c</b>) DS-1214-0-2 (<b>d</b>) DS-1820-0-2 (<b>e</b>) DS-02-0-5 (<b>f</b>) DS-68-0-5 (<b>g</b>) DS-1214-0-5 (<b>h</b>) DS-1820-0-5); ((<b>B</b>) (<b>a</b>) DS-02-30-2 (<b>b</b>) DS-68-30-2 (<b>c</b>) DS-1214-30-2 (<b>d</b>) DS-1820-30-2 (<b>e</b>) DS-02-30-5 (<b>f</b>) DS-68-30-5 (<b>g</b>) DS-1214-30-5 (<b>h</b>) DS-1820-30-5); ((<b>C</b>) (<b>a</b>) DS-02-90-2 (<b>b</b>) DS-68-90-2 (<b>c</b>) DS-1214-90-2 (<b>d</b>) DS-1820-90-2 (<b>e</b>) DS-02-90-5 (<b>f</b>) DS-68-90-5 (<b>g</b>) DS-1214-90-5 (<b>h</b>) DS-1820-90-5).</p>
Full article ">Figure 16 Cont.
<p>Variation trend of cumulative proportion of shear cracks and tensile cracks with time. ((<b>A</b>) (<b>a</b>) DS-02-0-2 (<b>b</b>) DS-68-0-2 (<b>c</b>) DS-1214-0-2 (<b>d</b>) DS-1820-0-2 (<b>e</b>) DS-02-0-5 (<b>f</b>) DS-68-0-5 (<b>g</b>) DS-1214-0-5 (<b>h</b>) DS-1820-0-5); ((<b>B</b>) (<b>a</b>) DS-02-30-2 (<b>b</b>) DS-68-30-2 (<b>c</b>) DS-1214-30-2 (<b>d</b>) DS-1820-30-2 (<b>e</b>) DS-02-30-5 (<b>f</b>) DS-68-30-5 (<b>g</b>) DS-1214-30-5 (<b>h</b>) DS-1820-30-5); ((<b>C</b>) (<b>a</b>) DS-02-90-2 (<b>b</b>) DS-68-90-2 (<b>c</b>) DS-1214-90-2 (<b>d</b>) DS-1820-90-2 (<b>e</b>) DS-02-90-5 (<b>f</b>) DS-68-90-5 (<b>g</b>) DS-1214-90-5 (<b>h</b>) DS-1820-90-5).</p>
Full article ">Figure 16 Cont.
<p>Variation trend of cumulative proportion of shear cracks and tensile cracks with time. ((<b>A</b>) (<b>a</b>) DS-02-0-2 (<b>b</b>) DS-68-0-2 (<b>c</b>) DS-1214-0-2 (<b>d</b>) DS-1820-0-2 (<b>e</b>) DS-02-0-5 (<b>f</b>) DS-68-0-5 (<b>g</b>) DS-1214-0-5 (<b>h</b>) DS-1820-0-5); ((<b>B</b>) (<b>a</b>) DS-02-30-2 (<b>b</b>) DS-68-30-2 (<b>c</b>) DS-1214-30-2 (<b>d</b>) DS-1820-30-2 (<b>e</b>) DS-02-30-5 (<b>f</b>) DS-68-30-5 (<b>g</b>) DS-1214-30-5 (<b>h</b>) DS-1820-30-5); ((<b>C</b>) (<b>a</b>) DS-02-90-2 (<b>b</b>) DS-68-90-2 (<b>c</b>) DS-1214-90-2 (<b>d</b>) DS-1820-90-2 (<b>e</b>) DS-02-90-5 (<b>f</b>) DS-68-90-5 (<b>g</b>) DS-1214-90-5 (<b>h</b>) DS-1820-90-5).</p>
Full article ">Figure 17
<p>Variation trend of real-time shear cracks’ proportion curves of unanchored structural planes. (<b>a</b>) Ds-02-0-2 (<b>b</b>) Ds-68-0-2 (<b>c</b>) Ds-1214-0-2 (<b>d</b>) Ds-1820-0-2 (<b>e</b>) Ds-02-0-5 (<b>f</b>) Ds-68-0-5 (<b>g</b>) Ds-1214-0-5 (<b>h</b>) Ds-1820-0-5.</p>
Full article ">Figure 18
<p>Variation trend of real-time shear cracks’ proportion of anchored structural planes with anchorage angle of 30°. (<b>a</b>) DS-02-30-2 (<b>b</b>) DS-68-30-2 (<b>c</b>) DS-1214-30-2 (<b>d</b>) DS-1820-30-2 (<b>e</b>) DS-02-30-5 (<b>f</b>) DS-68-30-5 (<b>g</b>) DS-1214-30-5 (<b>h</b>) DS-1820-30-5.</p>
Full article ">Figure 19
<p>Variation trend of real-time shear cracks’ proportion curves of anchored structural planes with anchorage angle of 90°. (<b>a</b>) DS-02-90-2 (<b>b</b>) DS-68-90-2 (<b>c</b>) DS-1214-90-2 (<b>d</b>) DS-1618-90-2 (<b>e</b>) DS-02-90-5 (<b>f</b>) DS-68-90-5 (<b>g</b>) DS-1214-90-5 (<b>h</b>) DS-1820-90-5.</p>
Full article ">
19 pages, 6031 KiB  
Article
Reliability Analysis of Serviceability Limit State for Braced Excavation Considering Multiple Failure Modes in Spatially Variable Soil
by Li Hong, Longlong Chen and Xiangyu Wang
Buildings 2022, 12(6), 722; https://doi.org/10.3390/buildings12060722 - 26 May 2022
Cited by 5 | Viewed by 2582
Abstract
High uncertainty is an inherent behavior of geotechnical materials. Nowadays, random field theory is an advanced method to quantify the effect of high uncertainty on geotechnical engineering. This study investigates the effect of spatial variable soil layers on deformations of deep excavation via [...] Read more.
High uncertainty is an inherent behavior of geotechnical materials. Nowadays, random field theory is an advanced method to quantify the effect of high uncertainty on geotechnical engineering. This study investigates the effect of spatial variable soil layers on deformations of deep excavation via the random finite element method. A procedure based on PLAXIS 2D software was developed to generate two-dimension random finite element models including multiple variables. Via the K-S test and S-W test, the excavation deformations basically followed lognormal distribution. With the growth of standard deviation of soil properties parameters, the distribution of excavation deformations becomes wider, and the failure probability increases. When the vertical scale of fluctuation ranges from 1 m to 25 m, the distribution of excavation deformations becomes wider. To analyze system reliability, this study proposed a fitted multiple lognormal distribution methods, which was a method with higher efficiency. The results indicated that system reliability was lower than single failure probability and sensitive to design level. The system failure probability will be over-evaluated or under-evaluated if the correlation between excavation responses is ignored. This study provided a novel method to quantify the effect of high uncertainty of soil layer on excavation responses and proposed an efficient method for system reliability analysis, which is meaningful for excavation reliability design. Full article
Show Figures

Figure 1

Figure 1
<p>Finite element model for deterministic analysis.</p>
Full article ">Figure 2
<p>Deformation curve of deterministic model: (<b>a</b>) ground settlement curve; (<b>b</b>) wall deflection curve.</p>
Full article ">Figure 3
<p>Flow chart of random finite element method.</p>
Full article ">Figure 4
<p>Random field realizations of <span class="html-italic">c<sub>u</sub></span> (<b>left</b>) and <span class="html-italic">φ</span> (<b>right</b>) (case 3).</p>
Full article ">Figure 5
<p>Convergence curve of wall deflection (case 1).</p>
Full article ">Figure 6
<p>Statistical distribution of excavation responses: (<b>a</b>) histogram of wall deflection in case 3; (<b>b</b>) Quantile-Quantile plot of wall deflection; (<b>c</b>) histogram of wall deflection with different <span class="html-italic">COVc<sub>u</sub></span>; (<b>d</b>) histogram of ground settlement with different <span class="html-italic">COVc<sub>u</sub></span>; (<b>e</b>) histogram of basal heave with different <span class="html-italic">COVc<sub>u</sub></span>.</p>
Full article ">Figure 6 Cont.
<p>Statistical distribution of excavation responses: (<b>a</b>) histogram of wall deflection in case 3; (<b>b</b>) Quantile-Quantile plot of wall deflection; (<b>c</b>) histogram of wall deflection with different <span class="html-italic">COVc<sub>u</sub></span>; (<b>d</b>) histogram of ground settlement with different <span class="html-italic">COVc<sub>u</sub></span>; (<b>e</b>) histogram of basal heave with different <span class="html-italic">COVc<sub>u</sub></span>.</p>
Full article ">Figure 7
<p>The effect of <span class="html-italic">COVc<sub>u</sub></span> and <span class="html-italic">COV</span><span class="html-italic">φ</span> on excavation responses: (<b>a</b>) Boxplot of wall deflection; (<b>b</b>) Boxplot of ground settlement; (<b>c</b>) Boxplot of basal heave.</p>
Full article ">Figure 8
<p>Effect of spatial variability on failure mode: (<b>a</b>) basal heave dominate; (<b>b</b>) wall deflection dominate.</p>
Full article ">Figure 9
<p>Effect of <span class="html-italic">δ<sub>y</sub></span> on distribution of excavation responses: (<b>a</b>) histogram of wall deflection with different <span class="html-italic">δ<sub>y</sub></span>; (<b>b</b>) histogram of ground settlement with different <span class="html-italic">δ<sub>y</sub></span>; (<b>c</b>) histogram of basal heave with different <span class="html-italic">δ<sub>y</sub></span>.</p>
Full article ">Figure 10
<p>Spearman correlation matrixes of responses (Case 3). Notes: <span class="html-italic">δ</span><span class="html-italic"><sub>d</sub></span>, <span class="html-italic">δ</span><span class="html-italic"><sub>s</sub></span>, <span class="html-italic">δ</span><span class="html-italic"><sub>b</sub></span> are the vector of wall deflection, ground settlement and basal heave, respectively. <span class="html-italic">M, V</span> are the vector of bending moment and shear force of diaphragm wall, respectively. <span class="html-italic">F<sub>Ni</sub></span> is the vector of axial force of strut in <span class="html-italic">i</span>th layer.</p>
Full article ">Figure 11
<p>Spatial variability effects on failure probability: (<b>a</b>) different thresholds of wall deflection; (<b>b</b>) different thresholds of basal heave.</p>
Full article ">Figure 12
<p>Effects of <math display="inline"><semantics> <mrow> <msub> <mi>δ</mi> <mi>y</mi> </msub> </mrow> </semantics></math> on failure probability at different thresholds of: (<b>a</b>) wall deflection; (<b>b</b>) basal heave.</p>
Full article ">
27 pages, 15807 KiB  
Article
Mechanical Characteristics and Acoustic Emission Characteristics of Mortar-Rock Binary Medium
by Wenyu Tang, Hang Lin, Yifan Chen, Jingjing Feng and Huihua Hu
Buildings 2022, 12(5), 665; https://doi.org/10.3390/buildings12050665 - 17 May 2022
Cited by 15 | Viewed by 2242
Abstract
The stability of the interface between mortar and rock is very important in engineering construction. In this paper, the all-digital acoustic emission (AE) system is used to detect the direct shear test of the mortar-rock binary medium interface with different sawtooth angles under [...] Read more.
The stability of the interface between mortar and rock is very important in engineering construction. In this paper, the all-digital acoustic emission (AE) system is used to detect the direct shear test of the mortar-rock binary medium interface with different sawtooth angles under different normal stress states. The stress-displacement information and AE signal during the whole shearing process are extracted. The coupling relationship between stress and AE characteristic parameters is discussed. The quantitative relationship between sawtooth angle and shear strength of binary medium is established, and three AE characteristic parameters that can be used to predict structural instability are proposed. The research shows that: With the increase of the normal stress and the sawtooth angle, the shear strength of the mortar-rock binary medium increases. The relationship of that is obtained by least squares fitting. The shear stress-displacement curve is divided into five stages according to the change of deformation law. Through the analysis of AE characteristic parameters, it is found that increasing the sawtooth angle makes the AE count and AE cumulative count increase. Based on the analysis of the characteristic parameters of RA-AF, the changes of shear cracks and tensile cracks within the whole shearing process were obtained, respectively. In the process of binary medium shearing, the AE peak frequency is in the range of 120–340 kHz. Three acoustic emission parameters that can predict the macroscopic damage of binary media are obtained: the AE b value, the ratio of shear crack signals, and the number of signals with a peak frequency of 220 Hz to 320 Hz. Full article
Show Figures

Figure 1

Figure 1
<p>Processing of rock surface.</p>
Full article ">Figure 2
<p>Specimen preparation before direct shear test. (<b>a</b>) Schematic diagram of specimens with different sawtooth angles. (<b>b</b>) Specimens after pouring.</p>
Full article ">Figure 3
<p>Shearing instrument, acoustic emission system.</p>
Full article ">Figure 4
<p>Schematic diagram of acoustic emission signal acquisition system.</p>
Full article ">Figure 5
<p>Relationship between shear stress and shear displacement of rock.</p>
Full article ">Figure 6
<p>Relationship between shear stress and shear displacement of mortar-rock binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 6 Cont.
<p>Relationship between shear stress and shear displacement of mortar-rock binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 7
<p>Stages of the shearing process.</p>
Full article ">Figure 8
<p>Relationship between normal stress and k value.</p>
Full article ">Figure 9
<p>The relationship between shear displacement and k/k’.</p>
Full article ">Figure 10
<p>Relationship between normal stress and shear strength of rock and binary medium.</p>
Full article ">Figure 11
<p>Relationship between cohesive force, internal friction angle and sawtooth angle.</p>
Full article ">Figure 12
<p>Relationship between normal stress and residual strength.</p>
Full article ">Figure 13
<p>Relationship between sawtooth angle and residual internal friction angle.</p>
Full article ">Figure 14
<p>Relationship between AE counts, AE cumulative counts and time. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 14 Cont.
<p>Relationship between AE counts, AE cumulative counts and time. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 15
<p>Relationship between AE b value and time in the whole shearing process. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 15 Cont.
<p>Relationship between AE b value and time in the whole shearing process. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 16
<p>Schematic diagram of crack distinction.</p>
Full article ">Figure 17
<p>Relation between the RA value and the average frequency in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 17 Cont.
<p>Relation between the RA value and the average frequency in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 17 Cont.
<p>Relation between the RA value and the average frequency in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 18
<p>Relation between the RA value and the time in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 18 Cont.
<p>Relation between the RA value and the time in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 18 Cont.
<p>Relation between the RA value and the time in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 19
<p>Relation between the crack ratio and the time in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 19 Cont.
<p>Relation between the crack ratio and the time in direct shear test of binary medium. (<b>a</b>) 8° (<b>b</b>) 30° (<b>c</b>) 45° (<b>d</b>) 55°.</p>
Full article ">Figure 20
<p>Relationship between AE signal peak frequency and time. (<b>a</b>) 30°, (<b>b</b>) 45°.</p>
Full article ">Figure 21
<p>AE signal peak frequency distribution.</p>
Full article ">Figure 22
<p>Relationship between peak frequency distribution of AE signal and time.</p>
Full article ">
15 pages, 8507 KiB  
Article
Numerical Analysis of Mechanical Characteristics of Constant-Resistance, Energy-Absorbing and Anti-Scour Bolts
by Zhi Tang, Hao Wu, Ying Liu, Yishan Pan, Jinguo Lv and Dezhi Chang
Materials 2022, 15(10), 3464; https://doi.org/10.3390/ma15103464 - 11 May 2022
Cited by 3 | Viewed by 1878
Abstract
In order to improve the impact resistance mechanical properties of bolt, the requirements of rock burst roadway support must be met. Based on the requirements that the anchor should have a reasonable deformation load threshold, high stroke efficiency, constant reaction force and stable [...] Read more.
In order to improve the impact resistance mechanical properties of bolt, the requirements of rock burst roadway support must be met. Based on the requirements that the anchor should have a reasonable deformation load threshold, high stroke efficiency, constant reaction force and stable repeatable deformation damage mode. A constant resistance anti-impact device was designed, and a new constant resistance energy-absorbing impact anchor rod was designed in combination with a conventional anchor rod, and the working principle of a constant resistance energy-absorbing impact anchor rod was given. ABAQUS finite element software was used to analyze the mechanical properties of bolt and the results showed that the constant resistance energy-absorbing anti-shock anchor has a stable and repeatable deformation damage mode under both static and impact loads, and the three indexes of the constant resistance energy-absorbing anti-shock anchor, such as yield distance, impact resistance time and energy absorption, are significantly better than those of the conventional anchor. The impact energy and impact velocity have less influence on the load-bearing capacity and stroke efficiency of the impact device. The impact velocity has less influence on the indices of the rod yield load, breaking load, absorbed energy and the yield distance of a conventional anchor and constant resistance energy-absorbing anti-stroke anchor, and the impact resistance time decreases non-linearly with the increase in the impact velocity. Full article
Show Figures

Figure 1

Figure 1
<p>Constant resistance anti-impact device. (<b>a</b>) Flared thin-walled round tube, (<b>b</b>) special-shaped nut, (<b>c</b>) constant resistance anti-impact device combination chart, (<b>d</b>) top view of constant resistance anti-impact device.</p>
Full article ">Figure 1 Cont.
<p>Constant resistance anti-impact device. (<b>a</b>) Flared thin-walled round tube, (<b>b</b>) special-shaped nut, (<b>c</b>) constant resistance anti-impact device combination chart, (<b>d</b>) top view of constant resistance anti-impact device.</p>
Full article ">Figure 2
<p>Anchor design drawings. (<b>a</b>) constant resistance energy-absorbing anti-scour anchor, (<b>b</b>) conventional anchors; 1: rod body; 2: tray; 3: anti-punch; 4: special-shaped nut.</p>
Full article ">Figure 3
<p>Deformation process of constant resistance energy-absorbing anti-scouring anchor rod by force, (<b>a</b>) initial stage (<b>b</b>) constant resistance deformation stage (<b>c</b>) yielding stage (<b>d</b>) strengthening and damage stage.</p>
Full article ">Figure 4
<p>Anchor rod deformation by static load. (<b>a</b>) conventional anchors, (<b>b</b>) constant resistance energy-absorbing anti-scour anchor, (<b>c</b>) deformation of constant resistance anti-impact device by force.</p>
Full article ">Figure 5
<p>Anchor force-displacement curve.</p>
Full article ">Figure 6
<p>Anchor energy–absorption–displacement curve.</p>
Full article ">Figure 7
<p>Deformation diagram of anchor rod subjected to impact load. (<b>a</b>) Conventional anchors, (<b>b</b>) constant resistance energy-absorbing anti-scour anchor.</p>
Full article ">Figure 8
<p>Anchor force–time curve: (<b>a</b>) impact energy 25 kJ; (<b>b</b>) impact energy 50 kJ; (<b>c</b>) impact energy 80 kJ.</p>
Full article ">Figure 9
<p>Anchor energy–absorption–displacement curve.</p>
Full article ">Figure 10
<p>Deformation of constant resistance energy-absorbing anti-scouring anchor rod by force. (<b>a</b>) Conventional anchor, (<b>b</b>) constant resistance energy-absorbing anti-scour anchor.</p>
Full article ">Figure 11
<p>Anchor force–time curve. (<b>a</b>) Conventional anchor, (<b>b</b>) constant resistance energy-absorbing anti-scour anchor.</p>
Full article ">Figure 12
<p>Anchor energy absorption–displacement curve.</p>
Full article ">Figure 13
<p>Anchor impact resistance time at different impact velocities.</p>
Full article ">Figure 14
<p>Anchor impact resistance time at different impact velocities.</p>
Full article ">Figure 15
<p>Test area of 11303 belt chute.</p>
Full article ">Figure 16
<p>Section of support in the test area of 11303 tape chute.</p>
Full article ">Figure 17
<p>Monitoring layout of 11303 belt chute test area.</p>
Full article ">Figure 18
<p>Specific monitoring scheme of 11303 belt chute monitoring area. (<b>a</b>) Surface displacement monitoring; (<b>b</b>) anchor force monitoring. (<b>c</b>) deep displacement monitoring.</p>
Full article ">
Back to TopTop