[go: up one dir, main page]

 
 
Sign in to use this feature.

Years

Between: -

Subjects

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Journals

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Article Types

Countries / Regions

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Search Results (2,098)

Search Parameters:
Keywords = crushing

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
19 pages, 3701 KiB  
Article
Integrated Techno-Environmental Analysis of Finely Ground Silica Sand in Sustainable Mortar Production
by Kamel Hebbache, Mourad Boutlikht, Abdellah Douadi, Cherif Belebchouche, Imed Benrebouh, Redha Hammouche, Laura Moretti, Adrian Chajec and Slawomir Czarnecki
Buildings 2024, 14(10), 3295; https://doi.org/10.3390/buildings14103295 (registering DOI) - 18 Oct 2024
Abstract
The environmental impacts of cement production are becoming more urgent concerns. This study examined the mechanical characteristics of cement when it is partially replaced with finely crushed sand. The experimental program consisted of three different levels of sand fineness of 459 m2 [...] Read more.
The environmental impacts of cement production are becoming more urgent concerns. This study examined the mechanical characteristics of cement when it is partially replaced with finely crushed sand. The experimental program consisted of three different levels of sand fineness of 459 m2/kg, 497 m2/kg, and 543 m2/kg, as well as four substitution ratios of 10%, 20%, 30%, and 40%. A total of thirteen combinations were formulated and then evaluated. The results demonstrated that increasing sand fineness from 459 m2/kg to 543 m2/kg substantially impacted the compressive strength (CS), increasing it by up to 30%, and increasing the substitution ratio from 10% to 40% reduced the mechanical strength by roughly 40%. An extensive techno-environmental evaluation showed that replacing cement with finely crushed sand is technically feasible and environmentally advantageous. This technique can decrease carbon dioxide (CO2) emissions by around 40%, emphasizing its ecological benefits and coinciding with worldwide initiatives to decrease the environmental impact of construction materials. In summary, this study demonstrates the advantages of improving the mechanical characteristics of cement while minimizing its ecological footprint. It suggests that finely crushed sand can be used as a sustainable alternative in cement manufacturing, promoting the use of more environmentally friendly construction methods. Full article
(This article belongs to the Section Building Materials, and Repair & Renovation)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Granulometric analysis of cement and crushed sand; (<b>b</b>) X-ray diffraction analysis of crushed sand [<a href="#B8-buildings-14-03295" class="html-bibr">8</a>].</p>
Full article ">Figure 2
<p>Chemical composition of cement: (<b>a</b>) cement substituted with 10% of sand powder (SP); (<b>b</b>) cement substituted with 20% of SP; (<b>c</b>) cement substituted with 30% of SP; and (<b>d</b>) cement substituted with 40% of SP.</p>
Full article ">Figure 3
<p>(<b>a</b>) Compressive strength and (<b>b</b>) bending strength at 7 and 28 days.</p>
Full article ">Figure 4
<p>Effect of crushed sand fineness on mechanical properties of mortar at 7 (<b>a</b>) and 28 (<b>b</b>) days.</p>
Full article ">Figure 5
<p>Effect of substitution ratio of cement on mechanical properties of mortar at 7 and 28 days (<b>a</b>) compressive strength at 7 days and (<b>b</b>) compressive strength at 28 days.</p>
Full article ">Figure 6
<p>Iso-response curve of mechanical performance (<b>a</b>) at 7 days and (<b>b</b>) 28 days.</p>
Full article ">Figure 7
<p>(<b>a</b>) Iso-response surfaces of the energy consumption for the production one ton of cement; (<b>b</b>) Iso-response curves of the energy consumption for the production one ton of cement.</p>
Full article ">Figure 8
<p>CO<sub>2</sub> emission in kilograms released to generate 1 kWh of electricity [<a href="#B53-buildings-14-03295" class="html-bibr">53</a>].</p>
Full article ">Figure 9
<p>Mechanical performance ratio (MPR) and effective carbon dioxide emission reduction (<b>a</b>) at 7 days and (<b>b</b>) 28 days.</p>
Full article ">
25 pages, 15207 KiB  
Article
Structure Design on Thermoplastic Composites Considering Forming Effects
by Wei Xie, Kai Song, Ju Yang, Fengyu Wang, Linjie Dong, Shengjie Jin, Guohua Zhu and Zhen Wang
Polymers 2024, 16(20), 2905; https://doi.org/10.3390/polym16202905 (registering DOI) - 15 Oct 2024
Viewed by 305
Abstract
Carbon fiber reinforced polypropylene (CF/PP) thermoplastics integrate the superior formability of fabrics with the recoverable characteristics of polypropylene, making them a pivotal solution for achieving lightweight designs in new energy vehicles. However, the prevailing methodologies for designing the structural performance of CF/PP vehicular [...] Read more.
Carbon fiber reinforced polypropylene (CF/PP) thermoplastics integrate the superior formability of fabrics with the recoverable characteristics of polypropylene, making them a pivotal solution for achieving lightweight designs in new energy vehicles. However, the prevailing methodologies for designing the structural performance of CF/PP vehicular components often omit the constraints imposed by the manufacturing process, thereby compromising product quality and reliability. This research presents a novel approach for developing a stamping–bending coupled finite element model (FEM) utilizing ABAQUS/Explicit. Initially, the hot stamping simulation is implemented, followed by the transmission of stamping information, including fiber yarn orientation and fiber yarn angle, to the follow-up step for updating the material properties of the cured specimen. Then, the structural performance analysis is conducted, accounting for the stamping effects. Furthermore, the parametric study reveals that the shape and length of the blank holding ring exerted minimal influence on the maximum fiber angle characteristic. However, it is noted that the energy absorption and crushing force efficiency metrics of the CF/PP specimens can be enhanced by increasing the length of the blank holding ring. Finally, a discrete optimization design is implemented to enhance the bending performance of the CF/PP specimen, accounting for the constraint of the maximum shear angle resulting from the stamping process. The optimized design resulted in a mass reduction of 14.3% and an improvement in specific energy absorption (SEA) by 17.5% compared to the baseline sample. Full article
Show Figures

Graphical abstract

Graphical abstract
Full article ">Figure 1
<p>Mechanical property parameter characterizations of CF/PP prepregs and the CF/PP laminates: (<b>a</b>) the bias-extension equipment for the CF/PP prepreg; (<b>b</b>) the normalized shear force–shear strain curve of single CF/PP prepreg; (<b>c</b>) the bias-extension equipment for the CF/PP laminate; (<b>d</b>) the true stress–true strain curves of CF/PP laminates; and (<b>e</b>) failure positions of three different CF/PP tensile samples.</p>
Full article ">Figure 2
<p>Manufacturing process of the hat-shaped CF/PP specimen: (<b>a</b>) the hot stamping machine and the molds; (<b>b</b>) the stamping molds and prepregs are pre-heated first, then the punch moves downwards and finishes the stamping step; the non-orthogonal cured specimen is taken out after cooling stage and trimmed to the final configuration for the further three-point bending test, the red line represents the weft yarn, and the blue line denotes the warp yarn, and the yellow arrow is the fiber direction.</p>
Full article ">Figure 3
<p>The three-point bending test fixtures and the typical bending responses of the CF/PP specimen: (<b>a</b>) three-point bending fixture descriptions; (<b>b</b>) force-/energy–displacement curves, deformation patterns and failure modes; and (<b>c</b>) typical historical photos of the CF/PP specimen.</p>
Full article ">Figure 4
<p>The establishment and workflow diagrams of the stamping–bending coupled model: (<b>a</b>) multi-step procedure of the stamping–bending coupled analysis in ABAQUS/Explicit, in which the orthogonal fabric configuration turned into a non-orthogonal configuration in the stamping step, and then the stamping information was transferred to the subsequent structural analysis step; (<b>b</b>) the VUMAT flowchart for the stamping–bending coupled finite element model, in which the trimming and mapping VUMAT served as a connecting link between the stamping VUMAT and bending VUMAT.</p>
Full article ">Figure 5
<p>The stamping–bending coupled finite element model of the hat-shaped CF/PP tube: (<b>a</b>) the stamping finite element model; (<b>b</b>) the molds removing and material trimming finite element model; and (<b>c</b>) the bending finite element model.</p>
Full article ">Figure 6
<p>Comparisons in forming and bending performances of the hat-shaped CF/PP specimen between the simulation and experiment results: (<b>a</b>) typical fiber angle variations; (<b>b</b>) force-/energy–displacement curves; (<b>c</b>) bending damage modes; and (<b>d</b>) bending deformation histories.</p>
Full article ">Figure 7
<p>The influences of the cross-sectional shape on the forming and bending characteristics of the CF/PP specimens: (<b>a</b>) the diagrams of stamping molds with three different cross-sectional shapes; (<b>b</b>) the fiber yarn shear angle distributions after the stamping process; (<b>c</b>) the bending force–displacement curves; and (<b>d</b>) the ultimate damage modes and plastic deformations.</p>
Full article ">Figure 8
<p>The influences of the blank holding ring shapes on the forming and bending characteristics of the CF/PP specimens: (<b>a</b>) the diagrams of stamping molds with three different blank holding ring shapes; (<b>b</b>) the fiber yarn shear angle distributions after the stamping process; (<b>c</b>) the bending force–displacement curves; and (<b>d</b>) the ultimate damage modes and plastic deformations.</p>
Full article ">Figure 9
<p>The influences of the blank holding ring lengths on the forming and bending characteristics of the CF/PP specimens: (<b>a</b>) the diagrams of stamping molds with three different blank holding ring lengths; (<b>b</b>) the fiber yarn shear angle distributions after the stamping process; (<b>c</b>) the bending force–displacement curves; and (<b>d</b>) the ultimate damage modes and plastic deformations.</p>
Full article ">Figure 10
<p>Comparisons in the forming and bending performance indicators of the CF/PP specimens: (<b>a</b>) the maximum fiber angle after the stamping process; (<b>b</b>) the peak force indicator; (<b>c</b>) the energy absorption indicator; and (<b>d</b>) the crushing force efficiency indicator.</p>
Full article ">Figure 11
<p>The multi-objective discrete optimization flowchart of CF/PP hat-shaped specimen accounting for the stamping process effects, in which the Taguchi approach was employed to deal with the discrete variables, and the gray relational analysis method was adopted to transform the constrained multi-objective problems into the unconstrained single-objective problems.</p>
Full article ">Figure 12
<p>Iteration history of gray relational degree.</p>
Full article ">
14 pages, 2471 KiB  
Article
Multi-Objective Optimal Control Method for the 6-DOF Robotic Crusher
by Guochen Duan, Lele Yao, Zhanyu Zhan, Tao Kang and Chaoyue Guo
Appl. Sci. 2024, 14(20), 9397; https://doi.org/10.3390/app14209397 - 15 Oct 2024
Viewed by 332
Abstract
In order to achieve the best crushing effect of the 6-DOF robotic crusher, a multi-objective optimal control method for the 6-DOF robotic crusher has been proposed. Taking the mass fraction of crushed products below 12 mm, total energy consumption, effective energy consumption, output, [...] Read more.
In order to achieve the best crushing effect of the 6-DOF robotic crusher, a multi-objective optimal control method for the 6-DOF robotic crusher has been proposed. Taking the mass fraction of crushed products below 12 mm, total energy consumption, effective energy consumption, output, and wear as the working indexes, and taking the suspension point, precession angle, and swing frequency of the mantle as the working conditions of the crusher, the working indexes under different working conditions are calculated. And, based on the above parameters, the optimization objective function of the 6-DOF robotic crusher is obtained. The weight determination method of fuzzy multiple attributes decision making (FMADM) is used to determine the equivalent wear and the optimization target weight. Compared with the original scheme, the output increases and the energy consumption decreases significantly. The results can be used as a reference for the control strategy of the 6-DOF robotic crusher. It can also be used as a reference for the design of a traditional cone crusher. Full article
(This article belongs to the Special Issue Mechanical Engineering Reliability Optimization Design)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Structure of cone crusher with traditional structure and 6-DOF robotic crusher. Structure of traditional cone crusher: (1) main shaft, (2) eccentric sleeve, (3) mantle, (4) concave. (<b>b</b>) Structure of traditional 6-DOF robotic crusher: (1) actuator, (2) mantle, (3) concave.</p>
Full article ">Figure 2
<p>Performance index calculation process.</p>
Full article ">Figure 3
<p>Coordinate transformation of suspension point.</p>
Full article ">Figure 4
<p>(<b>a</b>) Relative wear of the 2nd crushing layers, (<b>b</b>) Relative wear of the 5th crushing layers (<b>c</b>) Relative wear of the 9th crushing layers.</p>
Full article ">Figure 5
<p>Optimization target values under different conditions when moving cone swing frequency <span class="html-italic">f</span> = 5 Hz: (<b>a</b>) <span class="html-italic">M</span><sub>12,obj</sub>, (<b>b</b>) <span class="html-italic">η<sub>W</sub></span><sub>,obj</sub>, (<b>c</b>) <span class="html-italic">W</span><sub>sum,obj</sub>, (<b>d</b>) Δ<span class="html-italic">h</span><sub>e,obj,1</sub>, (<b>e</b>) Δ<span class="html-italic">h</span><sub>e,obj,2</sub>.</p>
Full article ">Figure 6
<p>Performance indicators of the original scheme and the optimized scheme: (<b>a</b>) mass fraction of crushed products below 12 mm <span class="html-italic">M</span><sub>12</sub> and treatment capacity <span class="html-italic">V</span><sub>sum</sub>, (<b>b</b>) total energy consumption <span class="html-italic">W</span><sub>sum</sub> and energy efficiency <span class="html-italic">η<sub>W</sub></span>, (<b>c</b>) equivalent wear Δ<span class="html-italic">h</span><sub>e</sub>.</p>
Full article ">Figure 7
<p>Wear of different crushing chamber depths hourly.</p>
Full article ">
18 pages, 1427 KiB  
Article
Ground Ivy (Glechoma hederacea L.) as an Innovative Additive for Enriching Wheat Bread: Study on Flour Fermentation Properties, Dough Rheological Properties and Bread Quality
by Karolina Pycia, Agata Maria Pawłowska, Zuzanna Posadzka and Joanna Kaszuba
Appl. Sci. 2024, 14(20), 9392; https://doi.org/10.3390/app14209392 - 15 Oct 2024
Viewed by 272
Abstract
The aim of the study was to assess the effect of water infusion of dried and crushed ground ivy (GH) on the fermentation properties of wheat flour (WF), farinographic properties of flour and dough (WD) and the quality of the obtained bread. In [...] Read more.
The aim of the study was to assess the effect of water infusion of dried and crushed ground ivy (GH) on the fermentation properties of wheat flour (WF), farinographic properties of flour and dough (WD) and the quality of the obtained bread. In the tested systems, tap water was replaced with water infusion with GH (m/v) at a concentration of 1% (A), 3% (B) and 5% (C). As part of the research methodology, the fermentation properties of flour and rheological properties of dough were assessed using a farinograph, and bread was obtained using a single-phase method using yeast and its quality was assessed. As part of this, the antioxidant potential and the profile and level of polyphenol content were determined. It was shown that replacing water with GH infusions shortened the total fermentation time of the dough and reduced the fermentation capacity of the dough. In the farinographic evaluation, an increase in flour water absorption (54.0–57.0%), dough development time (2.3–7.6 min), dough stability and softening were observed with an increase in the concentration of the added GH infusion. In turn, the volume of the loaf and the specific volume of the bread decreased with increasing the concentration of the GH infusion. The bread crumb darkened, and the elasticity and chewiness of the crumb decreased in relation to the control sample. In turn, the presence of GH infusion did not significantly affect the hardness of the crumb. As the concentration of the added GH infusion increased, an increase in the antioxidant potential of bread and the content of polyphenols and flavonoids was observed, and the UPLC-PDA-MS/MS analysis allowed the identification of 11 polyphenols in the bread. Full article
(This article belongs to the Section Food Science and Technology)
Show Figures

Figure 1

Figure 1
<p>Fermentographic graphs of tested doughs: <b>control</b>—control sample with water; <b>A</b>—dough with 1% infusion; <b>B</b>—dough with 3% infusion; <b>C</b>—dough with 5% infusion.</p>
Full article ">Figure 2
<p>Appearance of loaves and their cross-sections of tested breads with <span class="html-italic">G. hederacea</span> L. infusions: <b>control</b>—bread made of dough with water; <b>A</b>—bread made of dough with 1% infusion; <b>B</b>—bread made of dough with 3% infusion; <b>C</b>—bread made of dough with 5% infusion.</p>
Full article ">
27 pages, 20504 KiB  
Article
Three-Dimensional Numerical Simulation of High-Speed Shear Crushing of High-Density Fluid
by Xi Lin, Tao Lin, Gaojie Xu, Gangqiang Chen and Fei Xu
Processes 2024, 12(10), 2246; https://doi.org/10.3390/pr12102246 (registering DOI) - 15 Oct 2024
Viewed by 387
Abstract
Plasma atomization is a technology that can produce high sphericity, small particle diameters, and high-purity copper powder, which is of great significance for the development of metal additive manufacturing. At present, although plasma atomization can realize the industrial preparation of spherical copper powder, [...] Read more.
Plasma atomization is a technology that can produce high sphericity, small particle diameters, and high-purity copper powder, which is of great significance for the development of metal additive manufacturing. At present, although plasma atomization can realize the industrial preparation of spherical copper powder, there are still some problems, such as unclear understanding of the atomization process and a lack of theoretical support for powder quality control. This leads to the inability to predict the average particle diameter of powder in advance based on the actual atomization conditions and to optimize the process parameters, which seriously affects the further development of the plasma atomization process. We mainly studied the non-stationary simulation of a DC argon plasma torch. The purpose of this paper was to study the specific influence law of the average particle diameter of the powder in the process of plasma atomization by means of numerical simulation and experimental observation. The aim was to establish the mapping relationship between the atomization condition and the average particle diameter of the powder and realize the controllable preparation of the plasma atomized powder. At the same time, we used industrial-grade plasma atomization equipment to carry out pulverizing experiments to verify the plasma atomization theory and the powder average particle diameter control scheme proposed in this paper, thus proving the reliability of this study. Full article
(This article belongs to the Section Materials Processes)
Show Figures

Figure 1

Figure 1
<p>Overall structure diagram (including the computational domain) (<b>left</b>) and variable parameters involved in the model (<b>right</b>).</p>
Full article ">Figure 2
<p>Liquid tube–plasma torch model (<b>left</b>) and liquid tube–plasma torch model grid diagram (<b>right</b>).</p>
Full article ">Figure 3
<p>Liquid tube outlet (Zone A) and plasma torch outlet (Zone B) local encryption grid detail diagram.</p>
Full article ">Figure 4
<p>The particle size distribution curves of equivalent particle sizes in the experiment (red) and simulation (blue).</p>
Full article ">Figure 5
<p>(<b>a</b>–<b>c</b>) The morphology of the prepared Cu powder sample.</p>
Full article ">Figure 6
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle diameter distribution curve.</p>
Full article ">Figure 7
<p>(<b>a</b>,<b>d</b>), (<b>b</b>,<b>e</b>), (<b>c</b>,<b>f</b>) The velocity nephogram and velocity distribution vector diagram when <span class="html-italic">V</span><sub>1</sub> = 500 m/s (first row), 1000 m/s (second row), and 1500 m/s (third row), respectively.</p>
Full article ">Figure 8
<p>(<b>a</b>–<b>c</b>) For <span class="html-italic">V</span><sub>1</sub> = 500 m/s (first column), X-direction velocity on the Y-axis of the gradient cloud, and similarly for (<b>d</b>–<b>f</b>) <span class="html-italic">V</span><sub>1</sub> = 1000 m/s (second column) and (<b>g</b>–<b>i</b>) <span class="html-italic">V</span><sub>1</sub> = 1500 m/s (third column).</p>
Full article ">Figure 9
<p>(<b>a</b>–<b>c</b>) The gradient cloud diagram of the velocity in the X-direction on the Y-axis when <span class="html-italic">V</span><sub>1</sub> = 500 m/s (first row); similarly, (<b>d</b>–<b>f</b>) <span class="html-italic">V</span><sub>1</sub> = 1000 m/s (second row) and (<b>g</b>–<b>i</b>) <span class="html-italic">V</span><sub>1</sub> = 1500 m/s (third row).</p>
Full article ">Figure 10
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle diameter distribution curve.</p>
Full article ">Figure 11
<p>(<b>a</b>,<b>d</b>), (<b>b</b>,<b>e</b>), (<b>c</b>,<b>f</b>) The velocity nephogram and velocity distribution vector diagram when the outlet shape of the pipe was the 1 mm × 0.2 mm rectangle (first row), 1 mm × 0.4 mm rectangle (second row), and r = 0.36 mm circle (third row), respectively.</p>
Full article ">Figure 12
<p>(<b>a</b>–<b>c</b>) For the 1 mm × 0.2 mm rectangle (first column) X-direction velocity on the Y-axis of the gradient cloud; similarly, (<b>d</b>–<b>f</b>) for the 1 mm*0.4 mm rectangle (second column) and (<b>g</b>–<b>i</b>) for the r = 0.36 mm circle (third column).</p>
Full article ">Figure 13
<p>(<b>a</b>–<b>c</b>) The gradient cloud diagram of the velocity in the X-direction on the Y-axis for the 1 mm × 0.2 mm rectangle (first row); similarly, (<b>d</b>–<b>f</b>) for the 1 mm × 0.4 mm rectangle (second row) and (<b>g</b>–<b>i</b>) for r = 0.36 mm circle (third row).</p>
Full article ">Figure 14
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle size distribution curve.</p>
Full article ">Figure 15
<p>(<b>a</b>,<b>b</b>), (<b>c</b>,<b>d</b>) The velocity nephogram and velocity distribution vector diagram when the surface tension <span class="html-italic">σ</span> = 0.074 (first row) and <span class="html-italic">σ</span> = 0.74 (second row), respectively.</p>
Full article ">Figure 16
<p>(<b>a</b>–<b>c</b>) The gradient contours of the velocity in the X-direction of the surface tension <span class="html-italic">σ</span> = 0.074 (first column) on the Y-axis, and similarly (<b>d</b>–<b>f</b>) for <span class="html-italic">σ</span> = 0.74 (second column).</p>
Full article ">Figure 17
<p>(<b>a</b>–<b>c</b>) The gradient contours of the velocity in the X-direction of the surface tension <span class="html-italic">σ</span> = 0.074 (first row) on the Z-axis, and similarly (<b>d</b>–<b>f</b>) for <span class="html-italic">σ</span> = 0.74 (second row).</p>
Full article ">Figure 18
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle size distribution curve.</p>
Full article ">Figure 19
<p>(<b>a</b>,<b>b</b>), (<b>c</b>,<b>d</b>) The velocity nephogram and velocity distribution vector diagram when the collection tube length L = 0 mm (first row) and L = 40 mm (second row), respectively.</p>
Full article ">Figure 20
<p>(<b>a</b>–<b>c</b>) The gradient cloud images of the velocity in the X-direction on the Y-axis with the length of the collection tube <span class="html-italic">L</span> = 0 mm (first column), and (<b>d</b>–<b>f</b>) are the gradient cloud images of <span class="html-italic">L</span> = 40 mm (second column).</p>
Full article ">Figure 21
<p>(<b>a</b>–<b>c</b>) The gradient cloud images of the velocity on the Z-axis in the X-direction of the length of the collection tube <span class="html-italic">L</span> = 0 mm (first row), and (<b>d</b>–<b>f</b>) are the gradient cloud images of <span class="html-italic">L</span> = 40 mm (second row).</p>
Full article ">Figure 22
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle diameter distribution curve.</p>
Full article ">Figure 23
<p>(<b>a</b>,<b>b</b>), (<b>c</b>,<b>d</b>) The velocity nephogram and velocity distribution vector diagram when the right angle was used (first row) and when the chamfer was added to the outlet of the guide pipe (second row), respectively.</p>
Full article ">Figure 24
<p>(<b>a</b>–<b>c</b>) The gradient contours of the velocity in the X-direction for the outlet of the guide pipe at the right angle (first column) on the Y-axis, and similarly (<b>d</b>–<b>f</b>) for the chamfer (second column).</p>
Full article ">Figure 25
<p>(<b>a</b>–<b>c</b>) The gradient contours of the velocity in the X-direction for the outlet of the guide pipe at the right angle (first row) on the Z-axis, and similarly (<b>d</b>–<b>f</b>) for the chamfer (second row).</p>
Full article ">Figure 26
<p>(<b>a</b>) Spatial distribution of liquid particles. (<b>b</b>) Particle size distribution curve.</p>
Full article ">Figure 27
<p>(<b>a</b>,<b>d</b>), (<b>b</b>,<b>e</b>), (<b>c</b>,<b>f</b>) The velocity nephogram and velocity distribution vector diagram when <span class="html-italic">L</span><sub>1</sub> = 0 mm (first row), <span class="html-italic">L</span><sub>1</sub> = 1 mm (second row), and <span class="html-italic">L</span><sub>1</sub> = 2 mm (third row), respectively.</p>
Full article ">Figure 28
<p>(<b>a</b>–<b>c</b>) For <span class="html-italic">L</span><sub>1</sub> = 0 mm (first column), X-direction velocity on the Y-axis of the gradient cloud, and similarly for (<b>d</b>–<b>f</b>) <span class="html-italic">L</span><sub>1</sub> = 1 mm (second column) and (<b>g</b>–<b>i</b>) <span class="html-italic">L</span><sub>1</sub> = 2 mm (third column).</p>
Full article ">Figure 29
<p>(<b>a</b>–<b>c</b>) The gradient cloud diagram of the velocity in the X-direction on the Y-axis when <span class="html-italic">L</span><sub>1</sub> = 0 mm (first row); similarly, (<b>d</b>–<b>f</b>) <span class="html-italic">L</span><sub>1</sub> = 1 mm (second row) and (<b>g</b>–<b>i</b>) <span class="html-italic">L</span><sub>1</sub> = 2 mm (third row).</p>
Full article ">
17 pages, 3443 KiB  
Article
Carbon Sequestration by Preparing Recycled Cement, Recycled Aggregates, and Recycled Concrete from Construction and Demolition (C&D) Wastes
by Jing Luo, Rong Huang, Junjie Wang and Yi Zhang
Materials 2024, 17(20), 5020; https://doi.org/10.3390/ma17205020 - 14 Oct 2024
Viewed by 408
Abstract
As the world’s largest producer of construction waste, China’s recycling and related policies are of the biggest concern to the world. However, the effective disposal and reuse of this waste has become an important issue since currently China still has a very low [...] Read more.
As the world’s largest producer of construction waste, China’s recycling and related policies are of the biggest concern to the world. However, the effective disposal and reuse of this waste has become an important issue since currently China still has a very low recycling ratio compared to developed countries, and most of the waste concrete was only simply broken and used as low-grade recycled aggregates for subgrade cushion, cement stabilized crushed stone, and filler wall. In this paper, a concrete cycle model focusing on how to effectively recycle and utilize waste concrete is put forward to prepare high quality recycled concrete, especially through a series of technical means, such as effective separation, carbon sequestration, and reactivation. Producing high quality recycled concrete can not only replace traditional concrete but also effectively reduce the consumption and waste of raw materials. What’s more, the calculation results show a potential of significantly carbon sink; for every ton of recycled cement produced, the CO2 emission could be reduced by 0.35–0.77 tons compared to ordinary Portland cement, corresponding to a reduction of 47%–94%; and for every ton of recycled concrete produced, the CO2 emission could be reduced by 0.186 tons compared to normal concrete. A yearly CO2 sequestration of 1.4–3.08 gigatonnes could happen if the ordinary Portland cement could be replaced by the recycled cement around the world. Taking the currently accumulated construction and demolition (C&D) wastes globally, the production of recycled cement, recycled aggregates, and recycled concrete could induce a significant carbon sink in the world. Full article
Show Figures

Figure 1

Figure 1
<p>Comparison of reported compressive strengths of (<b>a</b>) recycled cement pastes and (<b>b</b>) ordinary cement pastes in different literature (RC—Recycled Cement, RBC—Recycled Blended Cement, RCP—Recycled Concrete Powder, OPC—Ordinary Porland Cement, BC—Blended Cement). (data from [<a href="#B33-materials-17-05020" class="html-bibr">33</a>,<a href="#B35-materials-17-05020" class="html-bibr">35</a>,<a href="#B36-materials-17-05020" class="html-bibr">36</a>,<a href="#B37-materials-17-05020" class="html-bibr">37</a>,<a href="#B38-materials-17-05020" class="html-bibr">38</a>,<a href="#B39-materials-17-05020" class="html-bibr">39</a>,<a href="#B40-materials-17-05020" class="html-bibr">40</a>,<a href="#B41-materials-17-05020" class="html-bibr">41</a>,<a href="#B42-materials-17-05020" class="html-bibr">42</a>,<a href="#B43-materials-17-05020" class="html-bibr">43</a>,<a href="#B44-materials-17-05020" class="html-bibr">44</a>,<a href="#B45-materials-17-05020" class="html-bibr">45</a>,<a href="#B46-materials-17-05020" class="html-bibr">46</a>,<a href="#B47-materials-17-05020" class="html-bibr">47</a>,<a href="#B48-materials-17-05020" class="html-bibr">48</a>,<a href="#B49-materials-17-05020" class="html-bibr">49</a>,<a href="#B50-materials-17-05020" class="html-bibr">50</a>]).</p>
Full article ">Figure 1 Cont.
<p>Comparison of reported compressive strengths of (<b>a</b>) recycled cement pastes and (<b>b</b>) ordinary cement pastes in different literature (RC—Recycled Cement, RBC—Recycled Blended Cement, RCP—Recycled Concrete Powder, OPC—Ordinary Porland Cement, BC—Blended Cement). (data from [<a href="#B33-materials-17-05020" class="html-bibr">33</a>,<a href="#B35-materials-17-05020" class="html-bibr">35</a>,<a href="#B36-materials-17-05020" class="html-bibr">36</a>,<a href="#B37-materials-17-05020" class="html-bibr">37</a>,<a href="#B38-materials-17-05020" class="html-bibr">38</a>,<a href="#B39-materials-17-05020" class="html-bibr">39</a>,<a href="#B40-materials-17-05020" class="html-bibr">40</a>,<a href="#B41-materials-17-05020" class="html-bibr">41</a>,<a href="#B42-materials-17-05020" class="html-bibr">42</a>,<a href="#B43-materials-17-05020" class="html-bibr">43</a>,<a href="#B44-materials-17-05020" class="html-bibr">44</a>,<a href="#B45-materials-17-05020" class="html-bibr">45</a>,<a href="#B46-materials-17-05020" class="html-bibr">46</a>,<a href="#B47-materials-17-05020" class="html-bibr">47</a>,<a href="#B48-materials-17-05020" class="html-bibr">48</a>,<a href="#B49-materials-17-05020" class="html-bibr">49</a>,<a href="#B50-materials-17-05020" class="html-bibr">50</a>]).</p>
Full article ">Figure 2
<p>Comparison of reported CO<sub>2</sub> emissions for producing per ton of recycled cement (RC) and ordinary Portland cement (OPC). (grey [<a href="#B40-materials-17-05020" class="html-bibr">40</a>], purple [<a href="#B46-materials-17-05020" class="html-bibr">46</a>], green [<a href="#B52-materials-17-05020" class="html-bibr">52</a>]) (data from [<a href="#B40-materials-17-05020" class="html-bibr">40</a>,<a href="#B46-materials-17-05020" class="html-bibr">46</a>,<a href="#B52-materials-17-05020" class="html-bibr">52</a>]).</p>
Full article ">Figure 3
<p>The weight of C&amp;D wastes in main countries worldwide (data source from [<a href="#B72-materials-17-05020" class="html-bibr">72</a>,<a href="#B73-materials-17-05020" class="html-bibr">73</a>,<a href="#B74-materials-17-05020" class="html-bibr">74</a>,<a href="#B75-materials-17-05020" class="html-bibr">75</a>,<a href="#B76-materials-17-05020" class="html-bibr">76</a>,<a href="#B77-materials-17-05020" class="html-bibr">77</a>,<a href="#B78-materials-17-05020" class="html-bibr">78</a>,<a href="#B79-materials-17-05020" class="html-bibr">79</a>,<a href="#B80-materials-17-05020" class="html-bibr">80</a>]).</p>
Full article ">Figure 4
<p>The trends of C&amp;D wastes in China (The numbers in 2023E to 2026E represent years, and the E stands for estimated. Data from [<a href="#B81-materials-17-05020" class="html-bibr">81</a>]).</p>
Full article ">Figure 5
<p>Comparison of recycling ratios of C&amp;D wastes in different countries at the year 2020 (data from [<a href="#B82-materials-17-05020" class="html-bibr">82</a>]).</p>
Full article ">Figure 6
<p>Remarkable development trend of the recycling ratios of C&amp;D wastes in China (data from [<a href="#B33-materials-17-05020" class="html-bibr">33</a>]).</p>
Full article ">Figure 7
<p>Production of recycled cement and recycled concrete with enhanced CO<sub>2</sub> sequestration in concrete cycle.</p>
Full article ">
15 pages, 338 KiB  
Article
What Are Sporty Sisters Talking About? A Textual Analysis of an All-Female Athlete Reality Show
by Yunjung Kim
Soc. Sci. 2024, 13(10), 543; https://doi.org/10.3390/socsci13100543 - 13 Oct 2024
Viewed by 470
Abstract
This study explores the representation of female athletes cast in a South Korean reality show titled Sporty Sisters (Korean title: Nonun Unni). Though there have been attempts to understand the media representation of female athletes from diverse media landscapes, the analysis of [...] Read more.
This study explores the representation of female athletes cast in a South Korean reality show titled Sporty Sisters (Korean title: Nonun Unni). Though there have been attempts to understand the media representation of female athletes from diverse media landscapes, the analysis of Asian female athletes is limited. Such interpretations have been discussed through geopolitical relations or nationalistic representations, which lack in-depth understanding and exploration of Asian athletes. Therefore, this paper expands the narrative by analyzing the first season (54 episodes) of Sporty Sisters. It is observed that professional athletes who transition to the entertainment industry are identified as “spor-tainers” and implicitly follow norms and rules applied to public figures. In this reality show, female athletes express their opinions on marriage, menstruation, pregnancy, and domestic roles while displaying characteristics of a girl crush, manifesting a variety of the female attributes of sportswomen. Despite the social expectations to fulfill their roles as sports celebrities and Korean women, Sporty Sisters is an outlet for female athletes to an extent to freely expose and describe their experiences as athletes and individuals. Full article
(This article belongs to the Special Issue Sport, Gender and Stereotypes)
28 pages, 9202 KiB  
Article
Effect of Coarse Aggregate Type on the Fracture Toughness of Ordinary Concrete
by Grzegorz Ludwik Golewski
Infrastructures 2024, 9(10), 185; https://doi.org/10.3390/infrastructures9100185 - 13 Oct 2024
Viewed by 349
Abstract
This research work aims to compare the strength and fracture mechanics properties of plain concretes, obtained from different coarse aggregates. During the study, mechanical parameters including compressive strength (fcm) and splitting tensile strength (fctm), as well as [...] Read more.
This research work aims to compare the strength and fracture mechanics properties of plain concretes, obtained from different coarse aggregates. During the study, mechanical parameters including compressive strength (fcm) and splitting tensile strength (fctm), as well as fracture parameters involving critical stress intensity factor (KIcS) and critical crack tip opening displacement (CTODc) were evaluated. The effect of the aggregates used on the brittleness of the concretes was also analyzed. For better understanding of the crack initiation and propagation in concretes with different coarse aggregates, a macroscopic failure surfaces examination of the tested beams is also presented. Crushed aggregates covered were basalt (BA), granite (GT), and limestone (LM), and natural peeble gravel aggregate (GL) were used in the concrete mixtures. Fracture toughness tests were performed on an MTS 810 testing machine. Due to the high strength of the rock material, the rough surface of the aggregate grains, and good bonding in the ITZ area between the aggregate and the paste, the concretes with crushed aggregates exhibited high fracture toughness. Both of the analyzed fracture mechanics parameters, i.e.,  KIcS and CTODc, increased significantly in the case of concretes which were manufactured with crushed aggregates. They amounted, in comparison to concrete based on gravel aggregate, to levels ranging from 20% for concrete with limestone aggregate to over 30% for concrete with a granite aggregate, and to as much as over 70% for concrete with basalt aggregate. On the other hand, the concrete with gravel aggregate showed the lowest fracture toughness because of the smooth surface of the aggregate grains and poor bonding between the aggregate and the cement paste. However, the fracture process in each series of concrete was quasi-plastic in the case of gravel concrete, semi-brittle in the case of limestone concrete, and clearly brittle in the case of the concretes based on granite and basalt aggregates. The results obtained help to explain how the coarse aggregate type affects the strength parameters and fracture toughness at bending. Full article
Show Figures

Figure 1

Figure 1
<p>The main factors determining the structure of the ITZ and the susceptibility of concrete to cracking.</p>
Full article ">Figure 2
<p>Appearance of coarse aggregate used in the studies: (<b>a</b>) basalt, (<b>b</b>) granite, (<b>c</b>) limestone, (<b>d</b>) gravel.</p>
Full article ">Figure 3
<p>Flowchart for testing the mechanical parameters of concretes.</p>
Full article ">Figure 4
<p>Flowchart for the evaluation of the fracture toughness of composites.</p>
Full article ">Figure 5
<p>Strength parameters of tested concretes: (<b>a</b>) compressive strength, (<b>b</b>) splitting tensile strength.</p>
Full article ">Figure 5 Cont.
<p>Strength parameters of tested concretes: (<b>a</b>) compressive strength, (<b>b</b>) splitting tensile strength.</p>
Full article ">Figure 6
<p>Relative changes in analyzed mechanical parameters of concretes based on different types of aggregates: (<b>a</b>) compressive strength, (<b>b</b>) splitting tensile strength.</p>
Full article ">Figure 7
<p>Brittleness index (<span class="html-italic">BI</span>) of tested concretes.</p>
Full article ">Figure 8
<p>The results of fracture mechanics parameters of the analyzed concretes with error bars: (<b>a</b>) <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mo> </mo> <mi>K</mi> </mrow> <mrow> <mi mathvariant="normal">I</mi> <mi mathvariant="normal">c</mi> </mrow> <mrow> <mi mathvariant="normal">S</mi> </mrow> </msubsup> </mrow> </semantics></math>, (<b>b</b>) <span class="html-italic">CTOD</span><sub>c</sub>.</p>
Full article ">Figure 9
<p>Relative changes in analyzed fracture mechanics parameters of concretes based on different type of aggregates: (<b>a</b>) <math display="inline"><semantics> <mrow> <msubsup> <mrow> <mo> </mo> <mi>K</mi> </mrow> <mrow> <mi mathvariant="normal">I</mi> <mi mathvariant="normal">c</mi> </mrow> <mrow> <mi mathvariant="normal">S</mi> </mrow> </msubsup> </mrow> </semantics></math>, (<b>b</b>) <span class="html-italic">CTOD</span><sub>c</sub>.</p>
Full article ">Figure 10
<p>Cross-section of analyzed concrete composites after fracture toughness test with indication of the details visible on the fracture surfaces: (<b>a</b>) C–GL, (<b>b</b>) C–LM, (<b>c</b>) C–GT, (<b>d</b>) C–BA; description in the text.</p>
Full article ">Figure 10 Cont.
<p>Cross-section of analyzed concrete composites after fracture toughness test with indication of the details visible on the fracture surfaces: (<b>a</b>) C–GL, (<b>b</b>) C–LM, (<b>c</b>) C–GT, (<b>d</b>) C–BA; description in the text.</p>
Full article ">
16 pages, 4576 KiB  
Article
A Method for the Coefficient Superposition Buckling Bearing Capacity of Thin-Walled Members
by Bing Xu, Lang Wang, Qin Liu, Rui Wang, Bing Kong and Bo Xu
Buildings 2024, 14(10), 3236; https://doi.org/10.3390/buildings14103236 - 12 Oct 2024
Viewed by 342
Abstract
Axial compression tests were conducted on short rhombic tubes of different cross-sectional shapes. The deformation modes of the rhombic short tubes were obtained. To induce a finite element model with deformation modes consistent with the actual working conditions, buckling modes are introduced into [...] Read more.
Axial compression tests were conducted on short rhombic tubes of different cross-sectional shapes. The deformation modes of the rhombic short tubes were obtained. To induce a finite element model with deformation modes consistent with the actual working conditions, buckling modes are introduced into the model as the initial imperfections of the structure. However, the buckling modes resulting from finite element buckling analyses often do not meet the needs of actual crushing modes. A coefficient superposition method of solution is proposed to derive modal characteristics consistent with the actual deformation modes by linear superposition of the buckling modes. Through the study of three aspects of theory, test, and simulation, and the comparison and verification of this method with the simulation results of related literature, the results show that the indexes derived from this method are closer to the actual circumstances and are more expandable, which provides a reference for the project. Full article
(This article belongs to the Section Building Structures)
Show Figures

Figure 1

Figure 1
<p>Specimens for axial compression test and parameter definition.</p>
Full article ">Figure 2
<p>Test instrument (CMT5305).</p>
Full article ">Figure 3
<p>(<b>A</b>) Flat specimen for tension test. (<b>B</b>) Dimensions of the flat specimen. (<b>C</b>) True stress–strain curve.</p>
Full article ">Figure 4
<p>Deformation modes, buckling modes (<b>left</b>), and force–displacement curves of all the specimens (<b>right</b>) under axial compression.</p>
Full article ">Figure 5
<p>(<b>A</b>) Finite element model. (<b>B</b>) Direction definition for the model. (<b>C</b>) Mesh subdivision for the model.</p>
Full article ">Figure 6
<p>All 1st-order buckling mode results: (<b>A</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>30</mn> <mo>°</mo> </mrow> </semantics></math> (<b>B</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo>°</mo> </mrow> </semantics></math>. (<b>C</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>60</mn> <mo>°</mo> </mrow> </semantics></math>. (<b>D</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>90</mn> <mo>°</mo> </mrow> </semantics></math>. (<b>E</b>) Comparison of buckling modes of side plates under different boundaries.</p>
Full article ">Figure 7
<p>Smooth amplitude curve of simulated loading.</p>
Full article ">Figure 8
<p>The positive and negative definitions of buckling shape coefficients <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="bold-italic">a</mi> </mrow> <mrow> <mi mathvariant="bold-italic">i</mi> <mi mathvariant="bold-italic">j</mi> </mrow> </msub> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi mathvariant="bold-italic">b</mi> </mrow> <mrow> <mi mathvariant="bold-italic">j</mi> </mrow> </msub> </mrow> </semantics></math>.</p>
Full article ">Figure 9
<p>Deformation modes of the finite model (<b>left</b>), experimental model (<b>middle</b>), and displacement–force curve (<b>right</b>) under compression after the introduction of specific defects: (<b>A</b>) <math display="inline"><semantics> <mrow> <mstyle mathvariant="bold"> <msub> <mrow> <mi mathvariant="bold-italic">θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>30</mn> <mo>°</mo> </mstyle> </mrow> </semantics></math>. (<b>B</b>) <math display="inline"><semantics> <mrow> <mstyle mathvariant="bold"> <msub> <mrow> <mi mathvariant="bold-italic">θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>45</mn> <mo>°</mo> </mstyle> </mrow> </semantics></math>. (<b>C</b>) <math display="inline"><semantics> <mrow> <mstyle mathvariant="bold"> <msub> <mrow> <mi mathvariant="bold-italic">θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>60</mn> <mo>°</mo> </mstyle> </mrow> </semantics></math>. (<b>D</b>) <math display="inline"><semantics> <mrow> <mstyle mathvariant="bold"> <msub> <mrow> <mi mathvariant="bold-italic">θ</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> <mo>=</mo> <mn>90</mn> <mo>°</mo> </mstyle> </mrow> </semantics></math>.</p>
Full article ">Figure 10
<p>The ratio of the initial peak crushing force between the simulated value and the experimental value under different numbers of sides.</p>
Full article ">Figure 11
<p>Comparison of two naming methods.</p>
Full article ">
13 pages, 4051 KiB  
Article
Performance Evaluation of Pebble Concrete for Pavement: A Study on the Sucre Highway Project
by Zhuqing Feng, Jue Lu, Simin Liu, Jingliang Xia, Jing Wang, Faguang Leng and Xinxin Ma
Materials 2024, 17(20), 4994; https://doi.org/10.3390/ma17204994 - 12 Oct 2024
Viewed by 268
Abstract
Bolivia has abundant pebbles, while the supply of crushed stone is limited and unstable. Thus, the resource utilization of local pebble as a coarse aggregate and the guarantee of concrete durability are the key scientific issues in the Sucre Highway Project. In this [...] Read more.
Bolivia has abundant pebbles, while the supply of crushed stone is limited and unstable. Thus, the resource utilization of local pebble as a coarse aggregate and the guarantee of concrete durability are the key scientific issues in the Sucre Highway Project. In this paper, a comparative analysis was conducted of the performance of crushed stone concrete and pebble concrete. Additionally, the impact of fly ash on the water permeability resistance of concrete was investigated. The results indicate that the apparent density, bulk density, and void ratio of pebbles are lower than those of crushed stone, and the aggregate gradation of pebbles is dispersed. The type of aggregate is the primary factor influencing the splitting tensile strength of concrete, with the main failure modes of pebble concrete being slurry cracking, aggregate crushing, and interface debonding. While aggregate and fly ash have a minor effect on compressive strength, they significantly impact flexural tensile strength; however, all concretes meet the requirements for extra-heavy, very heavy, and heavy traffic load levels. In terms of impermeability, fly ash effectively mitigates the negative impact of aggregate type on the impermeability of concrete. These findings support the application of pebble concrete in the highway project. Full article
(This article belongs to the Special Issue Sustainable Pavement Materials and Their Performance Evaluation)
Show Figures

Figure 1

Figure 1
<p>Project location diagram.</p>
Full article ">Figure 2
<p>Physical appearance of the coarse aggregates: (<b>a</b>) crushed stone; (<b>b</b>) Pebble A; (<b>c</b>) Pebble B.</p>
Full article ">Figure 3
<p>Grading curve for coarse aggregate.</p>
Full article ">Figure 4
<p>Split sections of the crushed stone concretes (CS1/CS2) and two kinds of pebble concrete (PA1/PA2 and PB1/PB2).</p>
Full article ">Figure 5
<p>Splitting tensile strength variations in the concrete.</p>
Full article ">Figure 6
<p>The splitting surface of concrete: (<b>a</b>) crushed stone concrete with slurry cracking; (<b>b</b>) pebble concrete with slurry cracking and aggregate fracture; (<b>c</b>) pebble concrete with interface debonding and large holes (The dotted yellow lines display the pores inside the concrete).</p>
Full article ">Figure 7
<p>Compressive strength variations in the concrete.</p>
Full article ">Figure 8
<p>Flexural tensile strength variations in the concrete.</p>
Full article ">
20 pages, 10032 KiB  
Article
Study on Crashworthiness of Shrink Tube Anti-Creep Device
by Fan Zou, Shuguang Yao, Xin Zheng, Minhan Xie and Lei Yang
Machines 2024, 12(10), 720; https://doi.org/10.3390/machines12100720 - 11 Oct 2024
Viewed by 284
Abstract
Based on the requirements of the narrow installation space of a train end, compact energy-absorbing travel, and huge energy suck, a shrink tube anti-creep device was designed. The crashworthiness of different structures was studied by means of a material test, a trolley test, [...] Read more.
Based on the requirements of the narrow installation space of a train end, compact energy-absorbing travel, and huge energy suck, a shrink tube anti-creep device was designed. The crashworthiness of different structures was studied by means of a material test, a trolley test, and numerical simulation. For every 1 mm increase in tube wall thickness, 1 mm increase in the axial length of the friction cone, and 0.01 increase in the friction coefficient, the mean crushing force (MCF) increased by 45.1 kN, 13.5 kN, and 30.5 kN, respectively. When the cone angle of the shrink tube increased from α = 5° to α = 25°, the increase in the MCF with different thicknesses was about 600%. The MCF was most affected by the cone angle, followed by the wall thickness, the friction coefficient, and the axial length of the friction cone. The change in the contact length of the friction cone of the shrink tube under different structural parameters was compared. The contact length decreased with the increase in tube wall thickness and increased with the increase in angle. The variation rule of MCF was obtained to provide a reference for the development of genealogical products. Full article
(This article belongs to the Section Machine Design and Theory)
Show Figures

Figure 1

Figure 1
<p>Geometry description of main structure: (<b>a</b>) general location, (<b>b</b>) main structure, (<b>c</b>) collision attitude display, (<b>d</b>) half-section view, and (<b>e</b>) dimensional detail view.</p>
Full article ">Figure 2
<p>Material properties: (<b>a</b>) test equipment, (<b>b</b>) the sample before test, (<b>c</b>) the sample after test, and (<b>d</b>) material specimen size.</p>
Full article ">Figure 3
<p>Stress–strain curve of 45 steel: (<b>a</b>) engineering curve; (<b>b</b>) true curve.</p>
Full article ">Figure 4
<p>Pre-collision test scenario.</p>
Full article ">Figure 5
<p>Collision model of trolley test.</p>
Full article ">Figure 6
<p>Comparison of deformation process under different energy absorption strokes. (<b>a</b>) Test condition; (<b>b</b>) simulation condition.</p>
Full article ">Figure 7
<p>Comparison of test and simulation conditions: (<b>a</b>) force and time curve, (<b>b</b>) displacement and time curve, (<b>c</b>) force and displacement curve, and (<b>d</b>) energy absorption and displacement curve.</p>
Full article ">Figure 8
<p>Vertical 40 mm height difference collision test: (<b>a</b>) test scene; (<b>b</b>) deformation sequence diagram and experimental and simulated force and displacement curves.</p>
Full article ">Figure 9
<p>Test system composition.</p>
Full article ">Figure 10
<p>Loading and unloading curves under different peak loads.</p>
Full article ">Figure 11
<p>Influence of wall thickness: (<b>a</b>) force and displacement curves at different thicknesses; (<b>b</b>) <span class="html-italic">MCF</span> changes at different thicknesses.</p>
Full article ">Figure 12
<p>Influence of wall thickness: (<b>a</b>) energy absorption and displacement curves at different thicknesses; (<b>b</b>) <span class="html-italic">SEA</span> changes at different thicknesses.</p>
Full article ">Figure 13
<p>Influence of friction coefficient: (<b>a</b>) force and displacement curves under different friction coefficients; (<b>b</b>) variation trend of <span class="html-italic">MCF</span> under different friction coefficients.</p>
Full article ">Figure 14
<p>Influence of friction coefficient: (<b>a</b>) energy absorption and displacement curves under different friction coefficients; (<b>b</b>) variation trend of <span class="html-italic">SEA</span> under different friction coefficients.</p>
Full article ">Figure 15
<p>Influence of axial length of friction cone: (<b>a</b>) force and displacement curves under different friction lengths; (<b>b</b>) <span class="html-italic">MCF</span> changes under different friction lengths.</p>
Full article ">Figure 16
<p>Influence of axial length of friction cone: (<b>a</b>) energy absorption and displacement curves under different friction lengths; (<b>b</b>) <span class="html-italic">SEA</span> changes under different friction lengths.</p>
Full article ">Figure 17
<p>Comparison of force and displacement curves of tubes with different cone angles: (<b>a</b>) cone angle of 25°; (<b>b</b>) cone angle of 30°.</p>
Full article ">Figure 18
<p>Comparison of deformation modes of tubes with different cone angles; the circles in the figure show different deformation modes. (<b>a</b>) Cone angle of 25°; (<b>b</b>) cone angle of 30°.</p>
Full article ">Figure 19
<p>The crashworthiness of the tube with different thicknesses varies with the cone angle: (<b>a</b>) the <span class="html-italic">SEA</span>; (<b>b</b>) the <span class="html-italic">MCF</span>.</p>
Full article ">Figure 20
<p>The crashworthiness of tubes with different cone angles varies with thickness: (<b>a</b>) the <span class="html-italic">SEA</span>; (<b>b</b>) the <span class="html-italic">MCF</span>.</p>
Full article ">Figure 21
<p>Crashworthiness of the shrink tube varies with the radius: (<b>a</b>) the <span class="html-italic">SEA</span>; (<b>b</b>) the <span class="html-italic">MCF</span>.</p>
Full article ">Figure 22
<p>Energy composition variation with the radius of the shrinkable tube.</p>
Full article ">Figure 23
<p>The change process of the contact length of the conical surface in the initial stage of collision: (<b>a</b>) 0 ms; (<b>b</b>) 1 ms; (<b>c</b>) 2 ms; (<b>d</b>) 3 ms; (<b>e</b>) 4 ms; (<b>f</b>) 5 ms; (<b>g</b>) 6 ms; (<b>h</b>) 7 ms; (<b>i</b>) local enlarged view of contact surface.</p>
Full article ">Figure 24
<p>The stable contact length of the tube with different cone angles varies with thickness.</p>
Full article ">Figure 25
<p>The change trend of internal energy ratio of different shrinkage tubes: (<b>a</b>) thickness change; (<b>b</b>) cone angle change.</p>
Full article ">
18 pages, 7020 KiB  
Article
Axial Impact Response of Carbon Fiber-Reinforced Polymer Structures in High-Speed Trains Based on Filament Winding Process
by Aiqin Tian, Kang Sun, Quanwei Che, Beichen Jiang, Xiangang Song, Lirong Guo, Dongdong Chen and Shoune Xiao
Materials 2024, 17(20), 4970; https://doi.org/10.3390/ma17204970 - 11 Oct 2024
Viewed by 379
Abstract
The continuous increase in the operating speed of rail vehicles demands higher requirements for passive safety protection and lightweight design. This paper focuses on an energy-absorbing component (circular tubes) at the end of a train. Thin-walled carbon fiber-reinforced polymer (CFRP) tubes were prepared [...] Read more.
The continuous increase in the operating speed of rail vehicles demands higher requirements for passive safety protection and lightweight design. This paper focuses on an energy-absorbing component (circular tubes) at the end of a train. Thin-walled carbon fiber-reinforced polymer (CFRP) tubes were prepared using the filament winding process. Through a combination of sled impact tests and finite element simulations, the effects of a chamfered trigger (Tube I) and embedded trigger (Tube II) on the impact response and crashworthiness of the structure were investigated. The results showed that both triggering methods led to the progressive end failure of the tubes. Tube I exhibited a mean crush force (MCF) of 891.89 kN and specific energy absorption (SEA) of 38.69 kJ/kg. In comparison, the MCF and SEA of Tube II decreased by 21.2% and 21.9%, respectively. The reason for this reduction is that the presence of the embedded trigger in Tube II restricts the expansion of the inner plies (plies 4 to 6), thereby affecting the overall energy absorption mechanism. Based on the validated finite element model, a modeling strategy study was conducted, including the failure parameters (DFAILT/DFAILC), the friction coefficient, and the interfacial strength. It was found that the prediction results are significantly influenced by modeling methods. Specifically, as the interfacial strength decreases, the tube wall is more prone to circumferential cracking or overall buckling under axial impact. Full article
Show Figures

Figure 1

Figure 1
<p>Preparation of composite material tubes.</p>
Full article ">Figure 2
<p>Dynamic impact test.</p>
Full article ">Figure 3
<p>Numerical model for axial crushing of CFRP tubes.</p>
Full article ">Figure 4
<p>Schematic of delamination failure mode.</p>
Full article ">Figure 5
<p>Axial crushing force–displacement curves from experiment and simulation: (<b>a</b>) Tube I; (<b>b</b>) Tube II.</p>
Full article ">Figure 6
<p>Crushing process of Tube I from experiment and simulation.</p>
Full article ">Figure 7
<p>Crushing process of Tube II from experiment and simulation.</p>
Full article ">Figure 8
<p>Cross-sectional view of tube wall during crushing: (<b>a</b>) Tube I; (<b>b</b>) Tube II.</p>
Full article ">Figure 9
<p>Damage distribution of composite material tubes.</p>
Full article ">Figure 10
<p>Comparison of experimental and simulated crushing responses of Tube I under different fiber failure parameters: (<b>a</b>) impact force–displacement curves; (<b>b</b>) energy absorption–displacement curves.</p>
Full article ">Figure 11
<p>Effects of failure parameters (DFAILT/DFAILC), friction coefficient, and interfacial strength on MCF and SEA.</p>
Full article ">Figure 12
<p>Crushing process of Tube I predicted using different failure parameters.</p>
Full article ">Figure 13
<p>Comparison of experimental and simulated crushing responses of Tube I under different friction coefficients: (<b>a</b>) impact force–displacement curves; (<b>b</b>) energy absorption–displacement curves.</p>
Full article ">Figure 14
<p>Simulated crushing process of Tube I under different friction coefficients.</p>
Full article ">Figure 15
<p>Comparison of experimental and simulated crushing responses of Tube I under different inter-ply failure stresses: (<b>a</b>) crushing force–displacement curves; (<b>b</b>) energy absorption–displacement curves.</p>
Full article ">Figure 16
<p>Simulated crushing process of Tube I under different inter-ply failure stresses.</p>
Full article ">
27 pages, 25873 KiB  
Article
Biomimetic Modular Honeycomb with Enhanced Crushing Strength and Flexible Customizability
by Lumin Shen, Yuanzhi Wu, Tuo Ye, Tianyu Gao, Shanmei Zheng, Zhihao Long, Xi Ren, Huangyou Zhang, Junwen Huang and Kai Liu
Materials 2024, 17(20), 4950; https://doi.org/10.3390/ma17204950 - 10 Oct 2024
Viewed by 493
Abstract
The integration of biomimetic principles into the sophisticated design of honeycomb structures has gained significant traction. Inspired by the natural reinforcement mechanisms observed in tree stems, this research introduces localized thickening to the conventional honeycombs, leading to the development of variable-density honeycomb blocks. [...] Read more.
The integration of biomimetic principles into the sophisticated design of honeycomb structures has gained significant traction. Inspired by the natural reinforcement mechanisms observed in tree stems, this research introduces localized thickening to the conventional honeycombs, leading to the development of variable-density honeycomb blocks. These blocks are strategically configured to form modular honeycombs. Initially, the methodology for calculating the relative density of the new design is meticulously detailed. Following this, a numerical model based on the plastic limit theorem, verified experimentally, is used to investigate the in-plane deformation models of modular honeycomb under the low- and high-velocity impact and to establish a theoretical framework for compressive strength. The results confirm that the theoretical predictions for crushing strength in the modular honeycomb align closely with numerical findings across both low- and high-velocity impacts. Further investigation into densification strain, energy absorption, and gradient strategy is conducted using both simulation and experimental approaches. The outcomes indicate that the innovative design outperforms conventional honeycombs by significantly enhancing the crushing strength under low-velocity impacts through the judicious arrangement of honeycomb blocks. Additionally, with a negligible difference in densification strains, the modular honeycomb demonstrates superior energy dissipation capabilities compared to its conventional counterparts. At a strain of 0.85, the modular honeycomb’s energy absorption capacity improves by 36.68% at 1 m/s and 25.47% at 10 m/s compared to the conventional honeycomb. By meticulously engineering the arrangement of sub-honeycombs, it is possible to develop a modular honeycomb that exhibits a multi-plateau stress response under uniaxial and biaxial compression. These advancements are particularly beneficial to the development of auto crash absorption systems, high-end product transportation packaging, and personalized protective gear. Full article
(This article belongs to the Section Biomaterials)
Show Figures

Figure 1

Figure 1
<p>The design inspiration and geometry of the modular honeycomb. (<b>a</b>) The phenomenon of variable density in tree trunks, (<b>b</b>) the design process of modular honeycomb, and (<b>c</b>) four distinct configurations of the various density honeycomb blocks, (<b>c1</b>) The honeycomb block with side length 3<span class="html-italic">l<sub>n</sub></span>/2, (<b>c2</b>) The honeycomb block with side length 5<span class="html-italic">l<sub>n</sub></span>/2, (<b>c3</b>) The honeycomb block with side length 7<span class="html-italic">l<sub>n</sub></span>/2, (<b>c4</b>) The honeycomb block with side length 9<span class="html-italic">l<sub>n</sub></span>/2.</p>
Full article ">Figure 2
<p>The 3 × 3 modular honeycomb structure (<b>a</b>), sub-honeycomb configuration (<b>b</b>) and geometric parameters (<b>c</b>), and matrix honeycomb configuration (<b>d</b>) and geometric parameters (<b>e</b>).</p>
Full article ">Figure 3
<p>A sub-honeycomb (<b>a</b>) and the typical repetitive unit of the honeycomb structure (<b>b</b>).</p>
Full article ">Figure 4
<p>Two different types of 3 × 3 modular honeycombs. (<b>a</b>) The modular honeycomb with randomly distributed honeycomb blocks, (<b>b</b>) The modular honeycomb neat honeycomb blocks.</p>
Full article ">Figure 5
<p>The numerical model of in-plane compression for the modular honeycomb. <span class="html-italic">y</span>-directional compression (<b>a</b>), <span class="html-italic">x</span>-directional compression (<b>b</b>), wall thickness of the sub-honeycomb and matrix honeycomb (<b>c</b>).</p>
Full article ">Figure 6
<p>The mesh convergence study of the numerical model.</p>
Full article ">Figure 7
<p>The verification of numerical methods through comparative experiment.</p>
Full article ">Figure 8
<p>The deformation mode of the modular honeycomb when subjected to <span class="html-italic">y</span>-direction compression at the velocity of 1 m/s. (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.12</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.24</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.36</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.48</mn> </mrow> </semantics></math>, (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.60</mn> </mrow> </semantics></math>, (<b>f</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.72</mn> </mrow> </semantics></math>.</p>
Full article ">Figure 9
<p>The deformation mode of the modular honeycomb when subjected to <span class="html-italic">x</span>-direction compression at the velocity of 1 m/s. (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.12</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.24</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.36</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.48</mn> </mrow> </semantics></math>, (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.60</mn> </mrow> </semantics></math>, (<b>f</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.72</mn> </mrow> </semantics></math>.</p>
Full article ">Figure 10
<p>Analysis of force distribution in sub-honeycomb under compression along the <span class="html-italic">y</span>-axis. (<b>a</b>) A part of the sub-honeycomb, (<b>b</b>) the basic unit, (<b>c</b>) the strut AD.</p>
Full article ">Figure 11
<p>Analysis of force distribution in sub-honeycomb under compression along the <span class="html-italic">x</span>-axis. (<b>a</b>) A part of the sub-honeycomb, (<b>b</b>) the basic unit, (<b>c</b>) the deformation of the basic unit.</p>
Full article ">Figure 12
<p>Stress–strain and energy absorption efficiency curves of the modular honeycomb under low-velocity impact: (<b>a</b>) <span class="html-italic">y</span>-direction; (<b>b</b>) <span class="html-italic">x</span>-direction.</p>
Full article ">Figure 13
<p>The deformation mode of the modular honeycomb when subjected to <span class="html-italic">y</span>-direction compression at the velocity of 100 m/s. (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.12</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.24</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.36</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.48</mn> </mrow> </semantics></math>, (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.60</mn> </mrow> </semantics></math>, (<b>f</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.72</mn> </mrow> </semantics></math>.</p>
Full article ">Figure 14
<p>The deformation mode of the modular honeycomb when subjected to <span class="html-italic">x</span>-direction compression at the velocity of 100 m/s. (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.12</mn> </mrow> </semantics></math>, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.24</mn> </mrow> </semantics></math>, (<b>c</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.36</mn> </mrow> </semantics></math>, (<b>d</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.48</mn> </mrow> </semantics></math>, (<b>e</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.60</mn> </mrow> </semantics></math>, (<b>f</b>) <math display="inline"><semantics> <mrow> <mi>ε</mi> <mo>=</mo> <mn>0.72</mn> </mrow> </semantics></math>.</p>
Full article ">Figure 15
<p>The stress–strain curves of the modular honeycomb and the conventional honeycomb under the impact velocity of 100 m/s, (<b>a</b>) <span class="html-italic">y</span>-direction, (<b>b</b>) <span class="html-italic">x</span>-direction.</p>
Full article ">Figure 16
<p>The plateau stresses for modular honeycombs and the conventional honeycomb under different impact velocities: (<b>a</b>) for impacts along the <span class="html-italic">y</span>-direction; (<b>b</b>) a comparative analysis along the <span class="html-italic">x</span>- and <span class="html-italic">y</span>-directions.</p>
Full article ">Figure 17
<p>The stress–strain and densification strain of each honeycomb under varying velocities. (<b>a</b>) <span class="html-italic">v</span> = 1 m/s, (<b>b</b>) <span class="html-italic">v</span> = 10 m/s, (<b>c</b>) <span class="html-italic">v</span> = 30 m/s, (<b>d</b>) <span class="html-italic">v</span> = 50 m/s.</p>
Full article ">Figure 18
<p>Energy absorption of various honeycombs with an equivalent density of 3.46% under different impact velocities. (<b>a</b>) <span class="html-italic">v</span> = 1 m/s, (<b>b</b>) <span class="html-italic">v</span> = 10 m/s, (<b>c</b>) <span class="html-italic">v</span> = 30 m/s, (<b>d</b>) <span class="html-italic">v</span> = 50 m/s.</p>
Full article ">Figure 19
<p>Customized response by intermixing two types of honeycombs with different cell walls. (<b>a</b>) Deformation process; and (<b>b</b>) stress versus strain curve.</p>
Full article ">Figure 20
<p>Design of a modular honeycomb with three-stage plateau stress: (<b>a</b>) geometric model, (<b>b</b>) stress–strain curve, (<b>c</b>) deformation process.</p>
Full article ">Figure 21
<p>The geometric configurations of the central enhanced modular honeycomb (CEMH), external enhanced modular honeycomb (EEMH), and uniform wall thickness honeycomb (UWTH), as well as the deformation modes of these three types of honeycombs under biaxial compression at longitudinal strains of 0.2, 0.4, and 0.6.</p>
Full article ">Figure 22
<p>The <span class="html-italic">x</span>- and <span class="html-italic">y</span>-directional force–displacement curves of (<b>a</b>) CEMH, (<b>b</b>) EEMH, and (<b>c</b>) UWTH under biaxial compression.</p>
Full article ">
15 pages, 5177 KiB  
Article
Study on Rain Absorption Performance and Flow Field of Transonic Compressor under Different Working Conditions
by Shamiao Luo, Shaobin Li and Xizhen Song
Aerospace 2024, 11(10), 829; https://doi.org/10.3390/aerospace11100829 - 9 Oct 2024
Viewed by 327
Abstract
Taking a four-stage transonic compressor as the research object, the Lagrange particle tracking method was used to simulate the multiphase flow by considering the particle fragmentation, collision and evaporation models, and the influence of different inlet conditions (raindrop diameter, velocity, temperature and flow [...] Read more.
Taking a four-stage transonic compressor as the research object, the Lagrange particle tracking method was used to simulate the multiphase flow by considering the particle fragmentation, collision and evaporation models, and the influence of different inlet conditions (raindrop diameter, velocity, temperature and flow rate) on the compressor’s performance and stable working range was studied. The results show that inlet rain absorption can weaken the clearance leakage vortex make the shock wave move downstream, thus increasing the inlet flow rate, resulting in a decrease in stability margin and the highest efficiency point moving in the direction of flow increase. With the decrease in raindrop diameter, the pressure ratio and wet compression efficiency increase, and the stability margin decreases. With the increase in inlet raindrop velocity, the degree of pneumatic breakage increases and the raindrop diameter becomes smaller, which leads to the decrease in pressure ratio and efficiency. The influence of the mass flow rate of imported raindrops on the stable working range is significant. When the mass flow rate of imported raindrops accounts for 5% of the design flow, the stable working range can be reduced by more than half. Rain absorption increases the reaction force of the compressor and increases the load of the rotor blade. Full article
(This article belongs to the Section Aeronautics)
Show Figures

Figure 1

Figure 1
<p>Meridian view of four-stage transonic axial compressor.</p>
Full article ">Figure 2
<p>Four-stage compressor single-channel computing grid.</p>
Full article ">Figure 3
<p>Grid independence verification.</p>
Full article ">Figure 4
<p>Rebound diagram when the horizontal and vertical rebound coefficient is 0.5.</p>
Full article ">Figure 5
<p>Particle independent verification.</p>
Full article ">Figure 6
<p>Total pressure ratio—flow curve.</p>
Full article ">Figure 7
<p>Efficiency–flow characteristic curve.</p>
Full article ">Figure 8
<p>Total temperature–flow characteristic curve.</p>
Full article ">Figure 9
<p>Raindrop temperature distribution.</p>
Full article ">Figure 10
<p>Distribution of reaction force along leaf height.</p>
Full article ">Figure 10 Cont.
<p>Distribution of reaction force along leaf height.</p>
Full article ">Figure 11
<p>First stage rotor channel with different blade heights relative to Mach number cloud image.</p>
Full article ">Figure 12
<p>Local magnification of 99% blade height first stage rotor relative to Mach number.</p>
Full article ">Figure 13
<p>Static entropy cloud image of 99% blade height first stage rotor channel.</p>
Full article ">Figure 14
<p>First stage rotor outlet static entropy cloud image.</p>
Full article ">Figure 15
<p>Limit flow diagram of the suction surface of the first stage blade.</p>
Full article ">
18 pages, 5486 KiB  
Article
Design and Testing of Key Components for a Multi-Stage Crushing Device for High-Moisture Corn Ears Based on the Discrete Element Method
by Chunrong Li, Zhounan Liu, Min Liu, Tianyue Xu, Ce Ji, Da Qiao, Yang Wang, Limin Jiang, Jingli Wang and Weizhi Feng
Appl. Sci. 2024, 14(19), 9108; https://doi.org/10.3390/app14199108 - 9 Oct 2024
Viewed by 419
Abstract
To improve the crushing efficiency and crushing pass rate of high-moisture corn ears (HMCEs), a multi-stage crushing scheme is proposed in this paper. A two-stage crushing device for HMCEs is designed, and the ear crushing process is analyzed. Firstly, a simulation model for [...] Read more.
To improve the crushing efficiency and crushing pass rate of high-moisture corn ears (HMCEs), a multi-stage crushing scheme is proposed in this paper. A two-stage crushing device for HMCEs is designed, and the ear crushing process is analyzed. Firstly, a simulation model for HMCEs was established in EDEM software (2018), and the accuracy of the model was verified by the shear test. Subsequently, single-factor simulation experiments were conducted, with the crushing rate serving as the evaluation index. The optimal working parameter ranges for the HMCE device were identified as a primary crushing roller speed of 1200–1600 revolutions per minute (r/min), a secondary crushing roller clearance of 1.5–2.5 mm, and a secondary crushing roller speed of 2750–3750 r/min. A Box–Behnken experiment was conducted to establish a multiple regression equation. With the objective of maximizing the qualified crushing pass rate, the optimal combination of parameters was revealed: a primary crushing roller speed of 1500 r/min, a secondary crushing roller clearance of 2.5 mm, and a secondary crushing roller speed of 3280 r/min. The pass rate of corn cob crushing in the simulation test was 98.2%. The physical tests, using the optimized parameter combination, yielded a qualified crushing rate of 97.5%, which deviates by 0.7% from the simulation results, satisfying the requirement of a qualified crushing rate exceeding 95%. The experimental outcomes validate the rationality of the proposed crushing scheme and the accuracy of the model, providing a theoretical foundation for subsequent research endeavors. Full article
Show Figures

Figure 1

Figure 1
<p>Three-dimensional diagram of HCME crushing device. Components: 1, feeding hopper; 2, primary crushing roller; 3, receiving hopper; 4, discharge hopper; 5, secondary crushing roller; 6, conveyor belt; 7, frame; 8, transmission components; 9, electrical control box; 10, motor.</p>
Full article ">Figure 2
<p>Diagram of the principle of corn ear shattering.</p>
Full article ">Figure 3
<p>Mechanical analysis of the primary crushing plant.</p>
Full article ">Figure 4
<p>Mechanical analysis of secondary crushing plant.</p>
Full article ">Figure 5
<p>Discrete element modeling of corn ears.</p>
Full article ">Figure 6
<p>Comparative shear testing and experimental results of the discrete element model for corn ears: (<b>a</b>) shear test (Here the yellow is the corn kernels and the green is the corn cob); (<b>b</b>) load–displacement relative error diagram.</p>
Full article ">Figure 7
<p>Results of the one-way test. (<b>a</b>) Relationship between the primary crushing roll speed and crushing rate. (<b>b</b>) Relationship between the secondary crushing roll gap and crushing rate. (<b>c</b>) Relationship between the secondary crushing roll speed and crushing rate.</p>
Full article ">Figure 8
<p>Simulation of broken effect; (<b>a</b>) schematic diagram of the crushing process; (<b>b</b>) crushed particles passing through a 2 mm sieve; (<b>c</b>) crushed particles passing through a 10 mm sieve; (<b>d</b>) crushed particles that do not pass through the 10 mm sieve (Here the yellow is the corn kernels and the green is the corn cob).</p>
Full article ">Figure 9
<p>Schematic diagram of high-humidity corn ear simulation.</p>
Full article ">Figure 10
<p>Response surface diagrams for interaction: (<b>a</b>) interaction of A–B on S; (<b>b</b>) interaction ofA–C on S; (<b>c</b>) interaction of B–C on S.</p>
Full article ">Figure 11
<p>High-humidity corn ear crushing test bench and crushing effect picture; (<b>a</b>) high-moisture corn crushing device; (<b>b</b>) crushing effect photograph.</p>
Full article ">
Back to TopTop