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Keywords = serration structure

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10 pages, 3952 KiB  
Article
A Comparative Study on the Performance and Microstructure of 304NG Stainless Steel in Underwater and Air Laser Welding
by Jiaqi Sun, Yue Yang, Kai Wang, Shaohua Yin, Zhen Li and Zhen Luo
Materials 2024, 17(15), 3854; https://doi.org/10.3390/ma17153854 - 3 Aug 2024
Viewed by 475
Abstract
In order to facilitate the application of underwater laser welding technology in in situ repairs of nuclear power plants, this study conducted comparative experiments between local dry underwater laser welding and laser welding in air on 304NG nitrogen-controlled stainless steel. The aim was [...] Read more.
In order to facilitate the application of underwater laser welding technology in in situ repairs of nuclear power plants, this study conducted comparative experiments between local dry underwater laser welding and laser welding in air on 304NG nitrogen-controlled stainless steel. The aim was to explore its microstructural evolution and mechanical properties in underwater environments. It was found that, near the fusion line of laser welding in air, columnar dendrites gradually evolved into cellular dendrites toward the weld center, eventually disappearing, resulting in a skeletal ferrite and serrated austenite structure. The underwater laser welding joints exhibited similar characteristics yet with more pronounced alternation between columnar and cellular dendrites. Additionally, the size of cellular dendrites decreased significantly, and needle-like ferrite was observed at the weld center. The hardness of underwater laser welded joints was slightly higher than that of in-air laser welded joints. Compared to laser welding in air, the strength of underwater laser welding joints increased from 443 MPa to 471 MPa, and the displacement increased from 2.95 mm to 3.45 mm, both types of welded joints exhibited a mixed mode fracture characterized by plasticity and brittleness. Full article
(This article belongs to the Special Issue Advanced Welding in Alloys and Composites)
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Figure 1

Figure 1
<p>The microstructure of 304NG nitrogen-containing stainless steel.</p>
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<p>(<b>a</b>) Schematic diagram of underwater laser beam welding and (<b>b</b>) 3D structural of drain cover.</p>
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<p>The type of specimens for tensile testing.</p>
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<p>Macromorphology of the overlap joints under different welding conditions: (<b>a</b>) in air and (<b>b</b>) underwater.</p>
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<p>Microstructure of the in-air welded joints in <a href="#materials-17-03854-f004" class="html-fig">Figure 4</a>a: (<b>a</b>) region I, (<b>b</b>) region II, (<b>c</b>) region III and (<b>d</b>) region IV.</p>
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<p>Microstructure of the underwater welded joints in <a href="#materials-17-03854-f004" class="html-fig">Figure 4</a>b: (<b>a</b>) region I, (<b>b</b>) region II, (<b>c</b>) region III and (<b>d</b>) region IV.</p>
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<p>Microhardness distribution of the welded joints.</p>
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<p>(<b>a</b>) Displacement–force curve and (<b>b</b>) corresponding lap shear strength and displacement.</p>
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<p>SEM of fracture surface morphology of joints: (<b>a</b>,<b>b</b>) in air and (<b>c</b>,<b>d</b>) underwater.</p>
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25 pages, 11862 KiB  
Article
Experimental Investigation of the Bond Performance at the Interface between Engineered Geopolymer Composites and Existing Concrete
by Zhibin Li, Jiaqi Tan, Ji Ouyang, Yongxin Yu, Shibin Li, Taoxin Lin, Runan Liu and Wen Li
Buildings 2024, 14(6), 1819; https://doi.org/10.3390/buildings14061819 - 15 Jun 2024
Cited by 1 | Viewed by 409
Abstract
Engineered geopolymer composite (EGC) exhibits ultra-high toughness, excellent crack control capability, and superior durability, making it highly promising for applications in bridge connecting slabs, wet joints of prefabricated components, and concrete structure reinforcement. However, the bond performance and failure mechanisms at the interface [...] Read more.
Engineered geopolymer composite (EGC) exhibits ultra-high toughness, excellent crack control capability, and superior durability, making it highly promising for applications in bridge connecting slabs, wet joints of prefabricated components, and concrete structure reinforcement. However, the bond performance and failure mechanisms at the interface between EGC and existing concrete remain unclear. To elucidate the bond performance of EGC to existing concrete, direct shear tests were conducted on 15 sets of EGC–existing concrete bond specimens. This study explored the effects of existing concrete strength, interface roughness, and EGC strength on the bond performance and mechanisms. Additionally, a direct shear bond mechanical model was established to predict the interface bond strength. The results indicate that, with comparable compressive strength, the preparation of EGC can reduce the total carbon emissions by up to 127% compared to ECC. The failure mode of EGC-existing concrete bond specimens was mainly adhesive failure (except for specimen C30-III-G95), which can be categorized into serrated interfacial failure and alternating crack paths. The change in interface roughness was the primary factor leading to the transition between failure paths. The changes in interface roughness and EGC strength significantly influenced the bond performance. Under their combined effect, the interface bond strength of specimen C50-III-G95 increased by 345% compared to C50-I-G45. In contrast, the improvement in existing concrete strength had a relatively smaller effect on the increase in interface bond strength. Based on the experimental results and the bonding mechanism under direct shear stress, a direct shear bond mechanical model correlating existing concrete strength, interface roughness, and EGC strength was established. The model predictions showed good consistency with the experimental results. This study provides theoretical support and experimental data for the engineering application of EGC. Full article
(This article belongs to the Special Issue Next-Gen Cementitious Composites for Sustainable Construction)
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Figure 1

Figure 1
<p>Particle size distribution curves of binder materials and aggregates.</p>
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<p>Dimensions of specimens for test: (<b>a</b>) dumbbell-shaped specimen for axial tensile test; (<b>b</b>) cylinder specimen for axial compressive test; (<b>c</b>) cube double-sided bonding specimen for direct shear test.</p>
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<p>Schematic diagram of three types of interfacial roughness of EGC-existing concrete bond specimens.</p>
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<p>Mold for EGC–existing concrete bond specimens.</p>
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<p>Test equipment for axial compression test.</p>
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<p>Test equipment for axial tensile test.</p>
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<p>Test setup of existing concrete’s axial compressive test.</p>
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<p>Test setup of direct shear bond performance test.</p>
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<p>Tensile stress–strain curve of EGC.</p>
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<p>Failure modes of EGC–existing concrete bond specimens.</p>
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<p>Failure modes of EGC–existing concrete bond specimens.</p>
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<p>Load–slip curves of the bond interface for EGC–existing concrete bond specimens.</p>
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<p>The impact of interface roughness on interface bond strength.</p>
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<p>The impact of existing concrete strength grade on interface bond strength.</p>
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<p>Comparison of experimental and predicted values of interface bond strength.</p>
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<p>Comparison of experimental and predicted values of interface bond strength from relevant reference [<a href="#B17-buildings-14-01819" class="html-bibr">17</a>,<a href="#B70-buildings-14-01819" class="html-bibr">70</a>].</p>
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24 pages, 17878 KiB  
Article
Numerical Analysis of Broadband Noise Generated by an Airfoil with Spanwise-Varying Leading Edges
by Lei Wang, Xiaomin Liu, Chenye Tian and Dian Li
Biomimetics 2024, 9(4), 229; https://doi.org/10.3390/biomimetics9040229 - 11 Apr 2024
Viewed by 945
Abstract
Here, the single-target parameterization of alternatives to leading-edge noise is carried out using analytical models based on the Wiener–Hopf technique. Four leading-edge serration profiles with different frequencies, amplitudes, and phases are implemented to aid the understanding of sound suppression mechanisms. The effects of [...] Read more.
Here, the single-target parameterization of alternatives to leading-edge noise is carried out using analytical models based on the Wiener–Hopf technique. Four leading-edge serration profiles with different frequencies, amplitudes, and phases are implemented to aid the understanding of sound suppression mechanisms. The effects of the serrated shape factor, wavelength, and amplitude are analyzed at tip-to-root ratios of 0.5, 1, and 2, respectively. An effective double-wavelength sinusoidal serration design can substantially reduce the noise emissions of 5.2 dB at h¯ = 2. Additionally, compared to single-wavelength serrations, an additional 1.47 dB noise reduction effect can be obtained by double-wavelength serrations under the appropriate design parameters. The surface pressure and phase distribution of different spanwise-varying leading edges indicate that the phase interference effect affected by source-radiated noise reduction is enhanced by this serration at the hills for serrations with a small curvature, and noise emission in the low-frequency band is more effectively suppressed. The sharper the serration is, the more conducive it is to a reduction in high-frequency noise. Nevertheless, the effectiveness of serrations is usually partially limited by the non-negligible trailing-edge self-noise. The sound source intensity of the root is decreased by the ogee-shaped serrations with a large curvature transition. A secondary noise reduction mechanism with a local source cut-off effect caused by nonlinearity is demonstrated. Full article
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Figure 1

Figure 1
<p>Schematic illustration of the leading-edge serrations.</p>
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<p>Comparison between the measured axial velocity spectra and theoretical spectra.</p>
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<p>SPL comparison for analytical and experimental results of trailing-edge self-noise.</p>
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<p>SPL generated by the analytical results in view of self-noise and experimental results at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>.</p>
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<p>SPL generated by the analytical results in view of self-noise and experimental results at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>SPL generated by the analytical results in view of self-noise and experimental results at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>The serration profiles of diverse leading edges.</p>
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<p>Comparison of decay rates of <math display="inline"><semantics> <mrow> <mfenced open="|" close="|" separators="|"> <mrow> <msub> <mrow> <mi>E</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </mfenced> </mrow> </semantics></math> for different leading-edge serrations.</p>
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<p>Comparison of decay rates of <math display="inline"><semantics> <mrow> <mfenced open="|" close="|" separators="|"> <mrow> <msub> <mrow> <mi>E</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </mfenced> </mrow> </semantics></math> for different leading-edge serrations.</p>
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<p>SPL spectra of different leading-edge serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>.</p>
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<p>SPL spectra of different leading-edge serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>SPL spectra of different leading-edge serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>The serration profiles of the diverse leading edge with different values of b in Equation (16).</p>
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<p>The serration profiles of the diverse leading edge with different values of b in Equation (17).</p>
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<p>SPL spectra of leading-edge serrations with different b values in Equation (16) at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>SPL spectra of leading-edge serrations with different b values in Equation (17) at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>Schematic diagram of a double-wavelength serration.</p>
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<p>The serration profiles of leading edges with minimum test value (SPL) at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>.</p>
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<p>The serration profiles of lading edges with minimum test value (SPL) at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>The serration profiles of leading edges with minimum test value (SPL) at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>OASPLs of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>0.5</mn> </mrow> </semantics></math>.</p>
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<p>OASPLs of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>1</mn> </mrow> </semantics></math>.</p>
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<p>OASPLs of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>SPL<sub>CA</sub> and SPL<sub>0</sub> distributions of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 0.5.</p>
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<p>SPL<sub>CA</sub> and SPL<sub>0</sub> distributions of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 1.</p>
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<p>SPL<sub>CA</sub> and SPL<sub>0</sub> distributions of representative serrations with double wavelengths at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math>2.</p>
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<p>Cloud chart of <math display="inline"><semantics> <mrow> <msup> <mrow> <mfenced open="|" close="|" separators="|"> <mrow> <msub> <mrow> <mi>E</mi> </mrow> <mrow> <mi>n</mi> </mrow> </msub> </mrow> </mfenced> </mrow> <mrow> <mn>2</mn> </mrow> </msup> </mrow> </semantics></math> built for the smooth leading edge.</p>
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<p>Cloud charts of <math display="inline"><semantics> <mrow> <msup> <mrow> <mfenced open="|" close="|" separators="|"> <mrow> <msub> <mrow> <mi>E</mi> </mrow> <mrow> <mi>n</mi> </mrow> </msub> </mrow> </mfenced> </mrow> <mrow> <mn>2</mn> </mrow> </msup> </mrow> </semantics></math> for different double-wavelength serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math>2, including (<b>a</b>) traditional serrations, (<b>b</b>) ogee-shaped serrations, (<b>c</b>) sinusoidal serrations, and (<b>d</b>) iron-shaped serrations.</p>
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<p>SPL spectra of representative double-wavelength serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 2.</p>
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<p>Sound pressure reduction levels of representative double-wavelength serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 2.</p>
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<p>Integration of OASPLs of representative double-wavelength serrations over different frequency bands at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> <mn>2</mn> </mrow> </semantics></math>.</p>
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<p>Surface pressure generating outgoing acoustic waves for double-wavelength serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 2.</p>
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<p>Phase distribution of surface pressure along the spanwise-varying leading edge of double-wavelength serrations at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 2, M = 0.17, k<sub>1</sub> = 62.83, k<sub>3</sub> = 0.</p>
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<p>Spatial distribution of OASPL integrated over the frequency bands of (<b>a</b>) 0~10,000 Hz, (<b>b</b>) 0~500 Hz, (<b>c</b>) 500~5000 Hz, and (<b>d</b>) 5000~10,000 Hz at <math display="inline"><semantics> <mrow> <mover accent="true"> <mrow> <mi>h</mi> </mrow> <mo>¯</mo> </mover> <mo>=</mo> </mrow> </semantics></math> 2.</p>
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19 pages, 6960 KiB  
Article
Simulation and Structural Analysis of a Flexible Coupling Bionic Desorption Mechanism Based on the Engineering Discrete Element Method
by Jinguang Li, Hongyan Qi, Yunhai Ma, Peng Gao and Baoguang Wu
Biomimetics 2024, 9(4), 224; https://doi.org/10.3390/biomimetics9040224 - 8 Apr 2024
Viewed by 1045
Abstract
Soil adhesion is one of the important factors affecting the working stability and quality of agricultural machinery. The application of bionic non-smooth surfaces provides a novel idea for soil anti-adhesion. The parameters of sandy loam with 21% moisture content were calibrated by the [...] Read more.
Soil adhesion is one of the important factors affecting the working stability and quality of agricultural machinery. The application of bionic non-smooth surfaces provides a novel idea for soil anti-adhesion. The parameters of sandy loam with 21% moisture content were calibrated by the Engineering Discrete Element Method (EDEM). The final simulated soil repose angle was highly consistent with the measured soil repose angle, and the obtained regression equation of the soil repose angle provides a numerical reference for the parameter calibration of different soils. By simulating the sinusoidal swing of a sandfish, it was found that the contact interface shows the phenomenon of stress concentration and periodic change, which reflects the effectiveness of flexible desorption and soil anti-adhesion. The moving resistance of the wedge with different wedge angles and different serrated structures was simulated. Finally, it was found that a 40° wedge with a high-tail sparse staggered serrated structure on the surface has the best drag reduction effect, and the drag reduction is about 10.73%. Full article
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Figure 1
<p>(<b>a</b>) Adult sandfish (<span class="html-italic">Scincus scincus</span>); (<b>b</b>) body shape when sandfish swing [<a href="#B21-biomimetics-09-00224" class="html-bibr">21</a>]; (<b>c</b>) model of sandfish body swing.</p>
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<p>(<b>a</b>) Sandfish head; (<b>b</b>) head restoration model and angle measurement; (<b>c</b>) models with different angles.</p>
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<p>(<b>a</b>) Adult sandfish; (<b>b</b>) dorsal scales; (<b>c</b>) stripe structure of scale surface; (<b>d</b>) serrated structure of stripe end; (<b>e</b>) wedge model of bionic serrated structure.</p>
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<p>(<b>a</b>) Soil weighing; (<b>b</b>) soil drying; (<b>c</b>) soil sampling.</p>
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<p>(<b>a</b>) Soil sieving; (<b>b</b>) soil analyzing; (<b>c</b>) results of soil analyzing.</p>
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<p>(<b>a</b>) Preparation of soil repose angle measurement; (<b>b</b>) process of soil repose angle measurement.</p>
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<p>(<b>a</b>) Measurement of soil repose angle; (<b>b</b>) simulation of soil repose angle.</p>
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<p>(<b>a</b>) EDEM simulation of the movement of sandfish model in soil; (<b>b</b>) states at different times of sandfish model.</p>
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<p>(<b>a</b>) Soil particle generation and wedge model import; (<b>b</b>) the state of wedges at a certain moment.</p>
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<p>Simulate motion resistance of different wedges.</p>
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<p>Non-smooth surface wedges with different microstructures: (<b>a</b>) wedge of low-tail sparse staggered distribution; (<b>b</b>) wedge of low-tail sparse parallel distribution; (<b>c</b>) wedge of low-tail dense staggered distribution; (<b>d</b>) wedge of low-tail dense parallel distribution; (<b>e</b>) wedge of high-tail sparse staggered distribution; (<b>f</b>) wedge of high-tail sparse parallel distribution; (<b>g</b>) wedge of high-tail dense staggered distribution; (<b>h</b>) wedge of high-tail dense parallel distribution.</p>
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<p>Simulation results of wedge resistance with different microstructures.</p>
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<p>(<b>a</b>) Motion state of the wedge. (<b>b</b>) Motion state of the soil particle.</p>
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<p>(<b>a</b>) The stress distribution on the surface of the wedge; (<b>b</b>) the contact model of soil and soil-engaging components.</p>
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19 pages, 2514 KiB  
Article
Analysis and Evaluation of Seed-Filling Performance of a Pneumatic Interference Precision Seeder for Small Cabbages
by Xiong Liu, Chunjian Su, Zhongyang Li, Kai Wang, Fuxiang Xie, Yanan Tian and Jiangtao Qi
Appl. Sci. 2024, 14(7), 2825; https://doi.org/10.3390/app14072825 - 27 Mar 2024
Viewed by 780
Abstract
To address the current problems of poor seed-filling performance and seed leakage of the pneumatic seed filler for cabbage, we designed a pneumatic disturbing precision seed filler for cabbage based on the auxiliary disturbing seed-filling method. This seeder can completely perturb the seed [...] Read more.
To address the current problems of poor seed-filling performance and seed leakage of the pneumatic seed filler for cabbage, we designed a pneumatic disturbing precision seed filler for cabbage based on the auxiliary disturbing seed-filling method. This seeder can completely perturb the seed population entering the bottom of the seed box casing during the seed-filling process, thereby increasing the initial velocity of the cabbage seeds, and facilitating the smooth progress of the seed-filling process. Firstly, we carried out a theoretical analysis based on the particle dynamics of the seed-filling process of the seeder and obtained the influencing factors affecting the seed-filling performance of the seeder. Secondly, through EDEM discrete element simulation, the average speed of the seed population, the disturbance frequency, and the degree of disturbance were used as the indicators to select the seed discharge disk structure with the best seed-filling performance. In the experimental aspect, a four-factor three-level orthogonal standardized test was conducted to evaluate the seed filling performance of the planter, using the seed suction qualification rate and the seed leakage rate as the evaluation indexes. The optimal structure of the seed discharge tray was selected through polarity analysis and ANOVA. The optimal combination of parameters for the seed-filling process of the planter was obtained; linear serrated disk, 40 rpm disk rotation speed, −2500 Pa negative fan pressure, and 1.2 mm aperture diameter. After comparative validation tests, the seed suction qualification rate of the seed absorber was 95.32%, and the leakage rate was 3.11%, which was in line with the agronomic planting of Chinese cabbage seeds. Full article
(This article belongs to the Section Agricultural Science and Technology)
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Figure 1
<p>Structure of pneumatic seeder. 1. Seed box housing, 2. seed box cover, 3. seed guide tube 4. drive bearing, 5. drive shaft, 6. linear serrated disk, 7. air chamber sealing ring, 8. air chamber cavity.</p>
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<p>Kinematic analysis of the seed-filling process. Where <math display="inline"><semantics> <mrow> <mi>ω</mi> </mrow> </semantics></math> is the angular velocity, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>1</mn> </mrow> </msub> </mrow> </semantics></math> is the forward speed of the planter, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>v</mi> </mrow> <mrow> <mn>2</mn> </mrow> </msub> </mrow> </semantics></math> is the tangential velocity at disengagement, and <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>a</mi> </mrow> <mrow> <mi>k</mi> </mrow> </msub> </mrow> </semantics></math> is the centripetal acceleration.</p>
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<p>Three-dimensional structure of seed disk. 1. Linear serrated structure, 2. drive shaft connection holes, 3. type holes.</p>
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<p>Parameters of the sawtooth structure of seed disk. Where <span class="html-italic">L</span> is the length and width of the sawtooth structure, mm. <span class="html-italic">H</span> is the thickness of the sawtooth structure, mm.</p>
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<p>Structure of the seed box housing. (<b>a</b>) Rear view of the seed box housing, (<b>b</b>) Side view of seed box housing.</p>
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<p>3D model of seed disk used for simulation. (<b>a</b>) Flat disk, (<b>b</b>) circular serrated disk, (<b>c</b>) linear serrated disk.</p>
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<p>Model of seeder and cabbage seeds used for simulation. (<b>a</b>) Simplified model of seed expeller, (<b>b</b>) seed particle modeling.</p>
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<p>Distribution of changes in mean velocity of populations under different seed disks. (<b>a</b>) Flat disk, (<b>b</b>) circular−serrated disk, (<b>c</b>) straight−serrated disk.</p>
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<p>Changes in mean kinetic energy of populations at different speeds of seed discharging discs.</p>
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<p>Seed displacement performance test rig for seeding. 1. Digital display precision pressure gauge, 2. pneumatic precision seeder, 3. high-speed camera, 4. Servo motor, 5. LED flashlight.</p>
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<p>Seeder leakage in seed-filling performance tests. (<b>a</b>) Flat disk, (<b>b</b>) circular serrated disk, (<b>c</b>) linear serrated disk.</p>
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15 pages, 5335 KiB  
Article
A Study of the Influence of Fin Parameters on Porous-Medium Approximation
by Junjie Tong, Shuming Li, Tingyu Wang, Shuxiang Wang, Hu Xu and Shuiyu Yan
Energies 2024, 17(5), 1133; https://doi.org/10.3390/en17051133 - 27 Feb 2024
Cited by 1 | Viewed by 655
Abstract
The porous-medium approximation (PM) approach is extensively employed in large-quantity grid simulations of heat exchangers, providing a time-saving approach in engineering applications. To further investigate the influence of different geometries on the implementation of the PM approach, we reviewed existing experimental conditions and [...] Read more.
The porous-medium approximation (PM) approach is extensively employed in large-quantity grid simulations of heat exchangers, providing a time-saving approach in engineering applications. To further investigate the influence of different geometries on the implementation of the PM approach, we reviewed existing experimental conditions and performed numerical simulations on both straight fins and serrated fins. Equivalent flow and heat-transfer factors were obtained from the actual model, and computational errors in flow and heat transfer were compared between the actual model and its PM model counterpart. This exploration involved parameters such as aspect ratio (a*), specific surface area (Asf), and porosity (γ) to evaluate the influence of various geometric structures on the PM approach. Whether in laminar or turbulent-flow regimes, when the aspect ratio a* of straight fins is 0.98, the flow error (δf) utilizing the PM approach exceeds 45%, while the error remains within 5% when a* is 0.05. Similarly, for serrated fins, the flow error peaks (δf  > 25%) at higher aspect ratios (a* = 0.61) with the PM method and reaches a minimum (δf  < 5%) at lower aspect ratios (a* = 0.19). Under the same Reynolds numbers (Re), employing the PM approach results in an increased heat-transfer error (δh)with rising porosity (γ) and decreasing specific surface area (Asf), both of which remained under 10% within the range of this study. At lower aspect ratios (a*), the fin structure becomes more compact, resulting in a larger specific surface area (Asf) and smaller porosity ). This promotes more uniform flow and heat transfer within the model, which is closer to the characteristics of PM. In summary, for straight fins at 0 < a* < 0.17 in the laminar regime (200 < Re < 1000) and in the turbulent regime (1200 < Re < 5000) and for serrated fins at 0 < a* < 0.28 in the laminar regime (400 < Re < 1000) or 0 < a* < 0.32, in the turbulent regime (2000 < Re < 5000), the flow and heat-transfer errors are less than 15%. Full article
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<p>The geometry of the fin: (<b>a</b>) Straight fins; (<b>b</b>) Serrated fins.</p>
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<p>Actual model mesh and the PM model mesh: (<b>a</b>) Straight fins; (<b>b</b>) Serrated fins.</p>
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<p>Comparison between the calculated results of the straight fin model and the experimental results in the literature: (<b>a</b>) Laminar-flow state; (<b>b</b>) Turbulent-flow state.</p>
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<p>Comparison between the calculated results of the serrated fin model and the experimental results in the literature: (<b>a</b>) Laminar-flow state; (<b>b</b>) Turbulent-flow state.</p>
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<p>Influence of different fin geometries: (<b>a</b>) Influence of different <span class="html-italic">a*</span> values of straight fins on pressure drop; (<b>b</b>) Influence of different <span class="html-italic">a*</span> values of serrated fins on pressure drop; (<b>c</b>) Influence of different <span class="html-italic">A</span><sub><span class="html-italic">sf</span></sub> values of straight fins on outlet temperature; (<b>d</b>) Influence of different <span class="html-italic">A</span><sub><span class="html-italic">sf</span></sub> values of serrated fins on outlet temperature.</p>
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<p>Influence of different aspect ratios (<span class="html-italic">a</span>*) of straight fins on flow error: (<b>a</b>) Laminar-flow state; (<b>b</b>) Turbulent-flow state.</p>
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<p>Influence of different aspect ratios (<span class="html-italic">a</span>*) of serrated fins on flow error: (<b>a</b>) Laminar-flow state; (<b>b</b>) Turbulent-flow state.</p>
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<p>Influence of flow error on different geometrical structures of laminar straight fins: (<b>a</b>) Effect of different porosities <span class="html-italic">γ</span>; (<b>b</b>) Effect of different interfacial area densities <span class="html-italic">A<sub>sf.</sub></span></p>
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<p>Influence of flow error on different geometrical structures of turbulent straight fins: (<b>a</b>) Effect of different porosities <span class="html-italic">γ</span>; (<b>b</b>) Effect of different interfacial area densities <span class="html-italic">A<sub>sf.</sub></span></p>
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<p>Influence of different specific surface area (<span class="html-italic">A</span><sub>sf )</sub> values of serrated fins on flow error: (<b>a</b>) Laminar-flow state; (<b>b</b>) Turbulent-flow state.</p>
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16 pages, 8093 KiB  
Article
Mitigation of Shock-Induced Separation Using Square-Shaped Micro-Serrations—A Preliminary Study
by Fangyou Yu, Zhanbiao Gao, Qifan Zhang, Lianjie Yue and Hao Chen
Aerospace 2024, 11(2), 148; https://doi.org/10.3390/aerospace11020148 - 12 Feb 2024
Viewed by 1057
Abstract
Suppressing shock-induced flow separation has been a long-standing problem in the design of supersonic vehicles. To reduce the structural and design complexity of control devices, a passive control technique based on micro-serrations is proposed and its controlling effects are preliminarily investigated under test [...] Read more.
Suppressing shock-induced flow separation has been a long-standing problem in the design of supersonic vehicles. To reduce the structural and design complexity of control devices, a passive control technique based on micro-serrations is proposed and its controlling effects are preliminarily investigated under test conditions in which the Mach number is 2.5 and the ramp creating an incident shock is 15 deg. Meanwhile, a vorticity-based criterion for assessing separation scales is developed to resolve the inapplicability of the zero skin friction criterion caused by wall unevenness. The simulations demonstrate that the height of the first stair significantly influences the separation length. Generally, the separation length is shorter at higher stairs, but when the height is greater than half of the thickness of the incoming boundary layer, the corresponding separation point moves upstream. A stair with a height of only 0.4 times the thickness of the boundary layer reduces the separation length by 2.69%. Further parametric analysis reveals that while the remaining serrations have limited effects on the flow separation, an optimization of their shape (depth and width) can create more favorable spanwise vortices and offer a modest improvement of the overall controlling performance. Compared to the plate case, a 9.13% reduction in the separation length can be achieved using a slightly serrated design in which the leading stair is 0.1 high and the subsequent serrations are 0.2 deep and 0.05 wide (nondimensionalized, with the thickness of the incoming boundary layer). Meanwhile, the micro-serration structure even brings less drag. Considering the minor modification to the structure, the proposed method has the potential for use in conjunction with other techniques to exert enhanced control on separations. Full article
(This article belongs to the Special Issue Shock-Dominated Flow)
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<p>Computational domain and boundary conditions.</p>
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<p>Schematic diagram of micro-serrations.</p>
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<p>Comparison between experimental [<a href="#B42-aerospace-11-00148" class="html-bibr">42</a>] and numerical surface pressure distributions.</p>
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<p>Surface pressure distributions with different refinement levels (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Computed contour plots of vorticity magnitude and streamline distributions near the separation point (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Comparison of surface <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>C</mi> </mrow> <mrow> <mi>f</mi> </mrow> </msub> </mrow> </semantics></math> and vorticity magnitude distribution (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Separation length and location of the separation point (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Contours of the Mach number distributions with stair heights of (<b>a</b>) 0.4 and (<b>b</b>) 1.0 and (<b>c</b>) surface pressure distributions near the separation point (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Comparison of the pressure distributions for the stair and micro-serration configurations at typical sizes (<b>a</b>) 0.1, (<b>b</b>) 0.4,(<b>c</b>) 1.0 and (<b>d</b>) 4.0 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Pressure distributions of micro-serration configurations with different (<b>a</b>) depths and (<b>b</b>) widths at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0.4 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>(<b>a</b>) Pressure distributions and (<b>b</b>) separation length of micro-serration configurations with different depths at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0.1 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>(<b>a</b>) Pressure distributions and (<b>b</b>) separation length of micro-serration configurations with different widths at <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>h</mi> </mrow> <mrow> <mi>U</mi> </mrow> </msub> </mrow> </semantics></math> = 0.1 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Role of vortices in separation control. (<b>a</b>) The vortices in the micro-serrations. (<b>b</b>) Comparison of velocity profiles upstream of the separation point. (<b>c</b>) Pressure distributions before the first pressure plateau (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Vortices upstream of the separation point with different widths of the micro-serration: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>w</mi> </mrow> </semantics></math> = 0.05, (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>w</mi> </mrow> </semantics></math> = 0.1 (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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<p>Location of vortices in the micro-serration with different depths: (<b>a</b>) <math display="inline"><semantics> <mrow> <mi>h</mi> </mrow> </semantics></math> = 0.2 and (<b>b</b>) <math display="inline"><semantics> <mrow> <mi>h</mi> </mrow> </semantics></math> = 1.0; the micro-serration is not fully displayed (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>M</mi> </mrow> <mrow> <mn>0</mn> </mrow> </msub> </mrow> </semantics></math> = 2.5, <math display="inline"><semantics> <mrow> <mi>α</mi> </mrow> </semantics></math> = 15°, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>I</mi> </mrow> <mrow> <mi>P</mi> </mrow> </msub> </mrow> </semantics></math> = 65).</p>
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16 pages, 5678 KiB  
Article
Evaluation of a Serrated Edge to Mitigate the Adverse Effects of a Backward-Facing Step on an Airfoil
by Real J. KC, Trevor C. Wilson, Aaron S. Alexander, Jamey D. Jacob, Nicholas A. Lucido and Brian R. Elbing
Inventions 2023, 8(6), 160; https://doi.org/10.3390/inventions8060160 - 18 Dec 2023
Cited by 1 | Viewed by 1598
Abstract
Backward-facing steps are commonly formed on wings and blades due to misalignment between segments or the addition of protective films. A backward-facing step (BFS) is known to degrade the airfoil performance. To mitigate these adverse effects, a three-dimensional low-profile serrated pattern (termed sBFS) [...] Read more.
Backward-facing steps are commonly formed on wings and blades due to misalignment between segments or the addition of protective films. A backward-facing step (BFS) is known to degrade the airfoil performance. To mitigate these adverse effects, a three-dimensional low-profile serrated pattern (termed sBFS) was applied downstream of a BFS on an LA203A profile airfoil. The model drag was determined from wake surveys using a traversing Pitot-static probe within a subsonic wind tunnel operating at a chord-based Reynolds number of 300,000. The airfoil spanned the wind tunnel width (914 mm) and had a 197 mm chord length. Four different sBFS configurations were tested, each formed by applying a 1 mm thick film around the model leading edge. In addition, a BFS at various chord locations and a clean wing (i.e., no film applied) were tested for reference. The sBFS was able to reduce the drag relative the BFS by up to 8–10%, though not outperforming the clean wing configuration. In addition, the wake surveys showed the sBFS produced strong coherent structures that persist into the far-wake region (five chord length downstream of the model) with a scale that was much larger than the step height. Additionally, a computational study was carried out to further examine the flow behavior on the airfoil that produced the coherent structures. This showed that fluid near the surface gets entrained towards the sBFS downstream tip of the sBFS, which creates the initial rotation of these coherent structures that persist into the far-wake region. Full article
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<p>Side view schematic of the wind tunnel test section (dashed rectangle) with the airfoil and probe locations and their relative positions shown.</p>
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<p>(<b>a</b>) The LA203A airfoil profile with the definition of angle of attack (α). (<b>b</b>) Schematic of the top view of an sBFS configuration on the airfoil.</p>
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<p>(<b>a</b>) Clean wing contour plot of wake at Reynolds number of 300,000. (<b>b</b>) Coefficient of drag (<math display="inline"><semantics> <mrow> <msub> <mi>C</mi> <mi>d</mi> </msub> </mrow> </semantics></math>) versus angle of attack for the clean wing compared with estimation using XFOIL.</p>
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<p>BFS coefficient of drag as function of angle of attack and chord position compared to the clean wing.</p>
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<p>The maximum streamwise vorticity (<math display="inline"><semantics> <mrow> <msub> <mi>ω</mi> <mi>x</mi> </msub> </mrow> </semantics></math>) for the clean wing and BFS configurations tested with the five-hole probe.</p>
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<p>The coefficient of drag for all sBFS configurations tested as a function of the angle of attack. Curves for the clean wing and BFS at 10% chord are included for reference.</p>
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<p>Contour plots of the (<b>left column</b>) streamwise, (<b>middle column</b>) spanwise, and (<b>right column</b>) vertical velocity components from the (<b>top row</b>) clean wing, (<b>middle row</b>) BFS at 10% chord length, and (<b>bottom row</b>) sBFS-V1.</p>
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<p>Maximum streamwise vorticity for the sBFS-V1 configuration compared with the clean wing and 10% chord BFS.</p>
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<p>Comparison of the streamwise velocity contour plots produced by the (<b>left</b>) experimental measurements and (<b>right</b>) computational models.</p>
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<p>Computational simulation results of the streamwise vorticity in the far-wake region from the sBFS-V1 configuration.</p>
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<p>Flow entrainment over the sBFS visualized with streamlines colored based on the local relative speed (cool to warm colors indicate low to high speeds). Streamlines originate from either (<b>left</b>) the far-wall or (<b>right</b>) near-surface region upstream of the step.</p>
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<p>Comparison of the sBFS-V3 that produced the lowest <math display="inline"><semantics> <mrow> <msub> <mi>C</mi> <mi>d</mi> </msub> </mrow> </semantics></math> values with that of the clean wing and the BFS with the lowest drag (i.e., BFS at 45% chord length). The sBFS-V3 had the valley and peak at 27% and 45% chord length, respectively.</p>
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23 pages, 3806 KiB  
Article
Design and Experiment of Bionic Straw-Cutting Blades Based on Locusta Migratoria Manilensis
by Jinpeng Hu, Lizhang Xu, Yang Yu, Jin Lu, Dianlei Han, Xiaoyu Chai, Qinhao Wu and Linjun Zhu
Agriculture 2023, 13(12), 2231; https://doi.org/10.3390/agriculture13122231 - 1 Dec 2023
Cited by 2 | Viewed by 1271
Abstract
Aimed at addressing the problems of the existing straw choppers on combine harvesters, such as a large cutting resistance and poor cutting effect, combined with bionic engineering technology and biological characteristics, a bionic model was used to extract the characteristics of the cutting [...] Read more.
Aimed at addressing the problems of the existing straw choppers on combine harvesters, such as a large cutting resistance and poor cutting effect, combined with bionic engineering technology and biological characteristics, a bionic model was used to extract the characteristics of the cutting blades of locusta migratoria manilensis’s upper jaw. A 3D point cloud reconstruction and machine vision methods were used to fit the polynomial curve of the blade edge using Matlab 2016. A straw-cutting process was simulated using the discrete element method, and the cutting effect of the bionic blade was verified. Cutting experiments with rice straws were conducted using a physical property tester, and the cutting resistance of straw to bionic blades and general blades was compared. On the whole, the average cutting force of the bionic blades was lower than that of the general blades. The average cutting force of the bionic blade was 18.74~38.23% lower than that of a smooth blade and 1.63~25.23% lower than that of a serrated blade. Similarly, the maximum instantaneous cutting force of the bionic blade was reduced by 2.30~2.89% compared with the general blade, which had a significant drag reduction effect. By comparing the time–force curves of different blades’ cutting processes, it was determined that the drag-reducing effect of the bionic blade lies in shortening the straw rupture time. The larger the contact area between the blade and the straw, the more uniform the cutting morphology of the straw after cutting. Field experiment results indicate that the average power consumption of a straw chopper partially installed with bionic blades was 5.48% lower than one with smooth blades, measured using a wireless torque analysis module. In this research study, the structure of the straw chopper of an existing combine harvester was improved based on the bionic principle, which reduced resistance when cutting crop straw, thus reducing the power consumption required by the straw chopper and improving the effectiveness and stability of the blades. Full article
(This article belongs to the Section Agricultural Technology)
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<p>Locusta migratoria manilensis’s feeding process (female adult).</p>
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<p>Overall measurement of Locusta migratoria manilensis dimensions.</p>
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<p>Measurements of incised teeth of locusta migratoria manilensis.</p>
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<p>Reconstruction process of locusta migratoria manilensis cutting teeth.</p>
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<p>Specific flow chart of the extraction of the cutting blade’s contour.</p>
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<p>Cutting profile curves of locust incisors.</p>
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<p>Bionic cutting blades and general cutting blades. Note: I. the edge of the left tooth of the locusta migration manilensis blade; II. the edge of the right tooth of the locusta migration manilensis blade; III. a smooth-edge blade; IV. a serrated-edge blade. a means the blade width, mm; b means the blade length, mm; c means the blade thickness, mm; h means the blade width, mm; <span class="html-italic">l</span> means the blade length, mm; m means the tooth pitch, mm; n means the tooth height, mm; k means the diameter of the positioning hole, mm; α means the blade angle; A is an enlarged view of the serrated blade edge.</p>
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<p>Particle model of rice straw (<span class="html-italic">l</span><sub>2</sub> = 150 mm, <span class="html-italic">d</span><sub>2</sub> = 5 mm, d = 0.5 mm).</p>
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<p>Simplified straw-cutting device.</p>
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<p>Process of cutting rice straw (a. bionic blade; b. smooth blade).</p>
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<p>Process of chopping rice straw.</p>
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<p>Force of cutting rice straw using a bionic blade and a smooth blade.</p>
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<p>Contact condition of straw when being cut by bionic and smooth blades.</p>
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<p>Cutting blades with different curves used in the experiment. Note: (<b>a</b>) is the right tooth bionic blade, ratio: 1, 0.75, 0.5; (<b>b</b>) is the left tooth bionic blade, ratio: 1, 0.75; (<b>c</b>) is the general smooth blade; (<b>d</b>) is the general serrated blade.</p>
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<p>Rice straw for the cutting test.</p>
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<p>Cutting force test using rice straw (1. physical property tester; 2. self-made stem-clamping device; 3. blade; 4. self-made tool-clamping device).</p>
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<p>The display interface of physical tester.</p>
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<p>Trend chart of factors affecting the average cutting force applied to rice straw.</p>
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<p>Force of cutting straw with different blades.</p>
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<p>Combined cutting test of bionic blades.</p>
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<p>Scatter distribution of rotating–fixed blades and the rice-straw-cutting force.</p>
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<p>Force–time curves of cutting rice stems. ((<b>a</b>) smooth blade; (<b>b</b>) serrated blade; (<b>c</b>) left-tooth locusta migration manilensis blade; (<b>d</b>) right-tooth locusta migration manilensis blade). Note: I, II and III mean the first cutting stage, the second cutting stage and the third cutting stage, respectively.</p>
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<p>Incisions in straw stems after cutting using different types of blades.</p>
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<p>Slip splitting while cutting rice straw.</p>
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<p>Operating principle of DH5905 torque test and analysis system.</p>
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<p>Installation layout drawing of a wireless torque sensor and bionic cutting blades. (<b>1</b>) Installation and fixing the torque sensor bracket; (<b>2</b>) installation positions of the wireless sensor and strain gauge; (<b>3</b>) installation instructions for cutting blades; (<b>4</b>) WIFI installation location.</p>
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21 pages, 19271 KiB  
Article
Morphological Characterization of Cannabis sativa L. Throughout Its Complete Life Cycle
by Mohsen Hesami, Marco Pepe and Andrew Maxwell Phineas Jones
Plants 2023, 12(20), 3646; https://doi.org/10.3390/plants12203646 - 22 Oct 2023
Cited by 4 | Viewed by 8673
Abstract
This study extensively characterizes the morphological characteristics, including the leaf morphology, plant structure, flower development, and trichome features throughout the entire life cycle of Cannabis sativa L. cv. White Widow. The developmental responses to photoperiodic variations were investigated from germination to mature plant [...] Read more.
This study extensively characterizes the morphological characteristics, including the leaf morphology, plant structure, flower development, and trichome features throughout the entire life cycle of Cannabis sativa L. cv. White Widow. The developmental responses to photoperiodic variations were investigated from germination to mature plant senescence. The leaf morphology showed a progression of complexity, beginning with serrations in the 1st true leaves, until the emergence of nine leaflets in the 6th true leaves, followed by a distinct shift to eight, then seven leaflets with the 14th and 15th true leaves, respectively. Thereafter, the leaf complexity decreased, culminating in the emergence of a single leaflet from the 25th node. The leaf area peaked with the 12th leaves, which coincided with a change from opposite to alternate phyllotaxy. The stipule development at nodes 5 and 6 signified the vegetative phase, followed by bract and solitary flower development emerging in nodes 7–12, signifying the reproductive phase. The subsequent induction of short-day photoperiod triggered the formation of apical inflorescence. Mature flowers displayed abundant glandular trichomes on perigonal bracts, with stigma color changing from whitish-yellow to reddish-brown. A pronounced increase in trichome density was evident, particularly on the abaxial bract surface, following the onset of flowering. The trichomes exhibited simultaneous growth in stalk length and glandular head diameter and pronounced shifts in color. Hermaphroditism occurred well after the general harvest date. This comprehensive study documents the intricate photoperiod-driven morphological changes throughout the complete lifecycle of Cannabis sativa L. cv. White Widow. The developmental responses characterized provide valuable insights for industrial and research applications. Full article
(This article belongs to the Special Issue Cannabis sativa: Advances in Biology and Cultivation)
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<p>Leaf morphogenesis in cannabis from cotyledon (c) to 25th true leaf (L25) in the main stem. From “c” to “L12,” the plants were maintained under a long-day photoperiod. Starting from L13 and continuing thereafter, the plants were subjected to short-day photoperiod conditions.</p>
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<p>Leaf morphology-related traits including (<b>A</b>) leaflet length, (<b>B</b>) leaflet width, (<b>C</b>) ratio of leaflet length to leaflet width, (<b>D</b>) leaf area, (<b>E</b>) number of serrations, and (<b>F</b>) angle of serrations. Error bars show standard deviation. Error bars show standard deviation. TL: terminal leaflet; RLL1: first right lateral leaflet; RLL2: second right lateral leaflet; RLL3: third right lateral leaflet; RLL4: fourth right lateral leaflet. From “c” to “L12,” the plants were maintained under a long-day photoperiod. Starting from L13 and continuing thereafter, the plants were subjected to short-day photoperiod conditions.</p>
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<p>Correlation among morphological traits of cannabis leaf. LA: leaf area; LN: number of leaflets; LTL: length of terminal leaflet; WTL: width of terminal leaflet; LRLL: length of right lateral leaflet; LLLL: length of left lateral leaflet; WRLL: width of right lateral leaflet; WLLL: width of left lateral leaflet; ASTL: angle of serration in terminal leaflet; NSTL: number of serrations terminal leaflet; ASRLL: angle of serration in right lateral leaflet; ASLLL: angle of serration in left lateral leaflet; NSRLL: number of serrations in right lateral leaflet; NSLLL: number of serrations in left lateral leaflet.</p>
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<p>Phase-transition-related morphological changes. (<b>A</b>) Cannabis plants with stipules and opposite phyllotaxy, showing the vegetative phase; (<b>B</b>) Cannabis plants with bracts and solitary flowers, signifying the transition of the plants into the reproductive phase; (<b>C</b>) Cannabis plants with alternate phyllotaxy (red arrows show the alternate arrangement of leaves).</p>
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<p>Morphological characteristics of the cannabis plants during the vegetative phase and the reproductive phase. (<b>A</b>) Two stipules (small, leaf-like structures found at the base of a petiole), demonstrating the juvenile phase. (<b>B</b>) Bracts (modified leaves found just below a flower) and solitary flowers (i.e., perigonal bracts and style), demonstrating the reproductive phase. stp: stipule; sty: style; br: bract; pbr: perigonal bract.</p>
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<p>Plant growth and development under long-day photoperiod.</p>
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<p>Plant growth and development during the complete life cycle including: (<b>A</b>) 1 week, (<b>B</b>) 3 weeks, (<b>C</b>) 5 weeks, (<b>D</b>) 7 weeks, (<b>E</b>) 9 weeks, (<b>F</b>) 10 weeks, (<b>G</b>) 11 weeks, (<b>H</b>) 13 weeks, (<b>I</b>) 15 weeks, (<b>J</b>) 17 weeks, and (<b>K</b>) 19 weeks after seed germination. Scale bar = 10 cm; (<b>L</b>) Plant height during the complete life cycle of cannabis plants; (<b>M</b>) The length of the longest secondary branch of cannabis plants during the complete life cycle.</p>
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<p>Schematic representation of plant growth and development under short-day photoperiod.</p>
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<p>Flowering progress in cannabis. Main flower after (<b>A</b>) 3 days, (<b>B</b>) 1 week, (<b>C</b>) 2 weeks, (<b>D</b>) 4 weeks, (<b>E</b>) 6 weeks, and (<b>F</b>) 8 weeks.</p>
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<p>Hermaphroditic cannabis inflorescence. Red arrows show male flowers.</p>
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<p>Trichome distribution in the upper portion of the bracts after (<b>A</b>) 2 weeks of flowering or 86 days of seed germination, (<b>B</b>) 4 weeks of flowering or 100 days of seed germination, (<b>C</b>) 6 weeks of flowering or 114 days of seed germination, and (<b>D</b>) 8 weeks of flowering or 128 days of seed germination; (<b>E</b>) Trichome density during flower development.</p>
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<p>Glandular trichome after (<b>A</b>) 2 weeks of flowering or 86 days of seed germination, (<b>B</b>) 4 weeks of flowering or 100 days of seed germination, (<b>C</b>) 6 weeks of flowering or 114 days of seed germination, and (<b>D</b>) 8 weeks of flowering or 128 days of seed germination; (<b>E</b>) Trichome stalk length during flower development; (<b>F</b>) Glandular head diameter during flower development.</p>
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<p>Correlation among morphological traits of cannabis trichome. TD: trichome density; THD: trichome head diameter; SL: stalk length.</p>
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<p>Cannabis-leaf-related morphological traits. Red arrows show angle of serration. AS: Angle of serration; TL: terminal leaflet; RLL1: first right lateral leaflet; RLL2: second right lateral leaflet; RLL3: third right lateral leaflet; RLL4: fourth right lateral leaflet; LLL1: first left lateral leaflet; LLL2: second left lateral leaflet; LLL3: third left lateral leaflet; LLL4: fourth left lateral leaflet.</p>
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16 pages, 3354 KiB  
Article
Microstructure Effects on the Machinability of AM-Produced Superalloys
by Paul Wood, José Díaz-Álvarez, Alexis Rusinek, Urvashi Gunputh, Slim Bahi, Antonio Díaz-Álvarez, Maria Henar Miguélez, Yiling Lu, Pawel Platek and Judyta Sienkiewicz
Crystals 2023, 13(8), 1190; https://doi.org/10.3390/cryst13081190 - 31 Jul 2023
Cited by 4 | Viewed by 1435
Abstract
This paper discusses the microstructure effects on the machinability of Inconel 718 by conducting machining tests on an additively manufactured (AM) workpiece with a strongly textured grain structure and a wrought workpiece incorporating a finer and more equiaxed grain structure. The AM workpiece [...] Read more.
This paper discusses the microstructure effects on the machinability of Inconel 718 by conducting machining tests on an additively manufactured (AM) workpiece with a strongly textured grain structure and a wrought workpiece incorporating a finer and more equiaxed grain structure. The AM workpiece was produced as a thin tube using Laser Melting Powder Bed Fusion and optimal processing conditions for this alloy. A lathe was used to conduct instrumented orthogonal machining tests on the two workpiece materials under dry cut and coolant conditions using a semisynthetic emulsion coolant. The process parameters studied were feed from 0.05 to 0.15 mm/rev and cutting speed from 60 to 120 m/min with a cut time of 2 sec duration for each process condition. Measures for each process condition included cutting forces in the feed and main cut direction, and images of chip forms were obtained. The grain structures of the workpiece materials were characterized using Electron Back Scattered Diffraction (EBSD). New findings suggest that grain structures can significantly affect the machinability of the superalloy at a higher feed for all cutting speeds studied, and insights into the cause are discussed. Other important findings comment on the effectiveness of the coolant as a lubricant for reducing friction in machining. Full article
(This article belongs to the Section Crystalline Metals and Alloys)
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<p>Additive manufacturing (AM) of tube workpieces on 250 × 250 mm build plate.</p>
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<p>Engineering stress versus strain curves of AM Inconel 718 alloy fabricated in XY and ZY [<a href="#B13-crystals-13-01190" class="html-bibr">13</a>].</p>
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<p>Effect of f on F<sub>t</sub> (<b>a</b>) and F<sub>f</sub> (<b>b</b>).</p>
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<p>Effect of V<sub>c</sub> on µ<sub>rake</sub> for WR and AM materials.</p>
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<p>Effect of f on chip forms with V<sub>c</sub> = 60 m/min for WR and AM materials using coolant. (optical microscope at ×150 magnification).</p>
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<p>Effect of V<sub>c</sub> on chip forms at constant f = 0.15 mm/rev for WR and AM materials using coolant (optical microscope at ×150 magnification).</p>
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<p>Grain structures and textures of the AM and WR materials.</p>
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<p>Grain structure of the AM material normal to the tube thickness.</p>
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14 pages, 7187 KiB  
Article
Structure–Property Correlation between Friction-Welded Work Hardenable Al-4.9Mg Alloy Joints
by Aditya M. Mahajan, K. Vamsi Krishna, M. J. Quamar, Ateekh Ur Rehman, Bharath Bandi and N. Kishore Babu
Crystals 2023, 13(7), 1119; https://doi.org/10.3390/cryst13071119 - 18 Jul 2023
Viewed by 1094
Abstract
Friction welding of aluminum alloys holds immense potential for replacing riveted joints in the structural sections of the aeronautical and automotive sectors. This research aims to investigate the effects on the microstructural and mechanical properties when AA5083 H116 joints are subjected to rotary [...] Read more.
Friction welding of aluminum alloys holds immense potential for replacing riveted joints in the structural sections of the aeronautical and automotive sectors. This research aims to investigate the effects on the microstructural and mechanical properties when AA5083 H116 joints are subjected to rotary friction welding. To evaluate the quality of the welds, optical and scanning electron microanalysis techniques were utilized, revealing the formation of sound welds without porosity. The microstructural examination revealed distinct weld zones within the weldment, including the dynamically recrystallized zone (DRZ), thermo-mechanically affected zone (TMAZ), heat-affected zone (HAZ), and base metal (BM). During the friction-welding process, grain refinement occurred, leading to the development of fine equiaxed grains in the DRZ/weld zone. Tensile testing revealed that the weldment exhibited higher strength (YS: 301 ± 6 MPa; UTS: 425 ± 7 MPa) in the BM region compared to the base metal (YS: 207 ± 5 MPa; UTS: 385 ± 9 MPa). However, the weldment demonstrated slightly lower elongation (%El: 13 ± 2) compared to the base metal (%El: 15 ± 3). The decrease in ductility observed in the weldment can be attributed to the presence of distinct weld zones within the welded sample. Also, the tensile graph of the BM showed serrations throughout the curve, which is a characteristic phenomenon known as the Portevin–Le Chatelier effect (serrated yielding) in Al-Mg alloys. This effect occurs due to the influence of dynamic strain aging on the material’s macroscopic plastic deformation. Fractography analysis showcased a wide range of dimple sizes, indicating a ductile fracture mode in the weldment. These findings contribute to understanding the microstructural and mechanical behavior of AA5083 H116 joints subjected to rotary friction welding. Full article
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<p>The optical microstructure of the AA5083 base metal in (<b>a</b>) transverse plane (along the cross-section) and (<b>b</b>) longitudinal plane (along the central axis).</p>
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<p>SEM micrograph of the (<b>a</b>) AA5083 H116 base metal and (<b>b</b>) EDS analysis.</p>
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<p>Visual view of rotary friction-welded AA5083 H116 joint.</p>
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<p>Macrostructure of rotary friction-welded AA5083 H116 joint.</p>
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<p>Microstructure across the various weld zones formed along the weld interface during rotary friction welding of AA5083 H116 joint.</p>
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<p>EBSD orientation mapping of the AA5083 H116 friction-welded samples (<b>a</b>) DRZ, (<b>b</b>) TMAZ, (<b>c</b>) HAZ, and (<b>d</b>) BM.</p>
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<p>SEM micrograph of the AA5083 H116 friction-welded joint (<b>a</b>) weld interface and (<b>b</b>) EDS analysis of the weld interface.</p>
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<p>XRD pattern of the (<b>a</b>) AA5083 H116 base metal and (<b>b</b>) rotary friction-welded AA5083 joint.</p>
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<p>Microhardness distribution across the weld interface of AA5083 joint.</p>
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<p>Failure location of tensile specimen of AA5083 H116 joint.</p>
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<p>Typical tensile curves of AA5083 base compared with rotary friction-welded AA5083 H116 joint.</p>
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<p>Fracture surface of rotary friction-welded AA5083 H116 joint.</p>
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16 pages, 8100 KiB  
Article
Experimental and Numerical Study on Tensile Behavior of Double-Twisted Hexagonal Gabion Wire Mesh
by Yu-Liang Lin, Peng-Fei Fang, Xin Wang, Jie Wu and Guo-Lin Yang
Buildings 2023, 13(7), 1657; https://doi.org/10.3390/buildings13071657 - 28 Jun 2023
Cited by 2 | Viewed by 1803
Abstract
Double-twisted hexagonal gabion wire mesh is a type of reinforced soil material that is used in gabion retaining walls to stabilize the soil slope in geotechnical engineering. In this study, a series of tensile tests were conducted to investigate the tensile behavior of [...] Read more.
Double-twisted hexagonal gabion wire mesh is a type of reinforced soil material that is used in gabion retaining walls to stabilize the soil slope in geotechnical engineering. In this study, a series of tensile tests were conducted to investigate the tensile behavior of hexagonal gabion wire mesh. Meanwhile, numerical models of gabion wire mesh were built to investigate the whole tensile loading-strain process. The influence of wire diameter, mesh width, and mesh length on the tensile strength of hexagonal gabion wire mesh were evaluated based on laboratory tests and numerical simulation. The quantitative relationship of tensile strength versus wire diameter, mesh width, and mesh length was typically fitted by a quadratic function, linear function, and monotonically decreasing exponential function. The numerical result presents a good consistency with those obtained from the experiment. The result of the loading-strain curve obtained by both experiment and simulation exhibits an “S” shape with a distinct serrated characteristic. The loading-strain curve can be divided into the following four stages: mesh distortion stage, wire stretching stage, overall yield stage, and wire fracture stage, which well reflects the tensile behavior of double-twisted hexagonal wire mesh. The tensile behavior of gabion wire mesh is influenced by the structure pattern of wire mesh and the mechanical characteristic of steel wire. Full article
(This article belongs to the Collection Innovation of Materials and Technologies in Civil Construction)
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<p>Clamp for gabion wire mesh.</p>
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<p>Basic shape of hexagonal wire mesh.</p>
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<p>Tensile machine (SHT4106G electro-hydraulic servo machine, MTS Systems China, Shanghai, China).</p>
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<p>Tensile experiment testing of steel wire.</p>
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<p>Stress–strain test results of gabion wire mesh material. (<b>a</b>) Type A; (<b>b</b>) Type B; (<b>c</b>) Type C; (<b>d</b>) Type D.</p>
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<p>Tensile force–strain curve of gabion wire mesh with different mesh size.</p>
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<p>Tensile stress–strain response of gabion wire mesh with different wire diameter: (<b>a</b>) types A and B; (<b>b</b>) types C and D.</p>
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<p>Stress-strain characteristic of single wire in tensile test.</p>
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<p>Decomposition of total strain.</p>
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<p>Geometry and boundary condition of FEM model.</p>
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<p>Comparison between experiment and simulation.</p>
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<p>Displacement along wire mesh subjected to a boundary displacement (U<sub>y</sub> = 80 mm).</p>
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<p>Axial stress of wire subjected to an applied boundary displacement (U<sub>y</sub> = 36 mm).</p>
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<p>Distribution of plastic strain (PEEQ).</p>
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<p>Wire mesh in engineering practice.</p>
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<p>Influence of wire diameter.</p>
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<p>Influence of mesh height.</p>
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<p>Influence of mesh width.</p>
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<p>Nonlinear three element model.</p>
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<p>Comparison between the presented equation with the test results.</p>
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19 pages, 4969 KiB  
Article
Optimization Analysis of Thermodynamic Characteristics of Serrated Plate-Fin Heat Exchanger
by Ying Guan, Liquan Wang and Hongjiang Cui
Sensors 2023, 23(8), 4158; https://doi.org/10.3390/s23084158 - 21 Apr 2023
Cited by 2 | Viewed by 1538
Abstract
This study explores the use of Multi-Objective Genetic Algorithm (MOGA) for thermodynamic characteristics of serrated plate-fin heat exchanger (PFHE) under numerical simulation method. Numerical investigations on the important structural parameters of the serrated fin and the j factor and the f factor of [...] Read more.
This study explores the use of Multi-Objective Genetic Algorithm (MOGA) for thermodynamic characteristics of serrated plate-fin heat exchanger (PFHE) under numerical simulation method. Numerical investigations on the important structural parameters of the serrated fin and the j factor and the f factor of PFHE are conducted, and the experimental correlations about the j factor and the f factor are determined by comparing the simulation results with the experimental data. Meanwhile, based on the principle of minimum entropy generation, the thermodynamic analysis of the heat exchanger is investigated, and the optimization calculation is carried out by MOGA. The comparison results between optimized structure and original show that the j factor increases by 3.7%, the f factor decreases by 7.8%, and the entropy generation number decreases by 31%. From the data point of view, the optimized structure has the most obvious effect on the entropy generation number, which shows that the entropy generation number can be more sensitive to the irreversible changes caused by the structural parameters, and at the same time, the j factor is appropriately increased. Full article
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<p>Three-dimensional physical model.</p>
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<p>Mesh diagram of model.</p>
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<p>Grid independency check for Scheme.</p>
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<p>Comparison of <span class="html-italic">j</span> factor on air side.</p>
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<p>Comparison of <span class="html-italic">f</span> factors on air side.</p>
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<p>Comparison of <span class="html-italic">j</span> factors on water side.</p>
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<p>Comparison of <span class="html-italic">f</span> factors on water side.</p>
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<p>Temperature contour of fin.</p>
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<p>Pressure contour of fin.</p>
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<p>Effect of fin height and fin spacing on <span class="html-italic">j</span>.</p>
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<p>Effect of fin height and fin spacing on <span class="html-italic">f</span>.</p>
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<p>Effect of fin height and fin thickness on <span class="html-italic">j</span>.</p>
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<p>Effect of fin height and fin thickness on <span class="html-italic">f</span>.</p>
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<p>Effect of fin structure parameter on <span class="html-italic">j</span> factor.</p>
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<p>Effect of fin structure parameter on <span class="html-italic">f</span> factor.</p>
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<p>Effect of fin structure parameter on <span class="html-italic">N</span><span class="html-italic"><sub>s</sub></span>.</p>
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19 pages, 1327 KiB  
Systematic Review
Tissue vs. Fecal-Derived Bacterial Dysbiosis in Precancerous Colorectal Lesions: A Systematic Review
by Jurate Valciukiene, Kestutis Strupas and Tomas Poskus
Cancers 2023, 15(5), 1602; https://doi.org/10.3390/cancers15051602 - 4 Mar 2023
Cited by 3 | Viewed by 1782
Abstract
Alterations in gut microbiota play a pivotal role in the adenoma-carcinoma sequence. However, there is still a notable lack of the correct implementation of tissue and fecal sampling in the setting of human gut microbiota examination. This study aimed to review the literature [...] Read more.
Alterations in gut microbiota play a pivotal role in the adenoma-carcinoma sequence. However, there is still a notable lack of the correct implementation of tissue and fecal sampling in the setting of human gut microbiota examination. This study aimed to review the literature and to consolidate the current evidence on the use of mucosa and a stool-based matrix investigating human gut microbiota changes in precancerous colorectal lesions. A systematic review of papers from 2012 until November 2022 published on the PubMed and Web of Science databases was conducted. The majority of the included studies have significantly associated gut microbial dysbiosis with premalignant polyps in the colorectum. Although methodological differences hampered the precise fecal and tissue-derived dysbiosis comparison, the analysis revealed several common characteristics in stool-based and fecal-derived gut microbiota structures in patients with colorectal polyps: simple or advanced adenomas, serrated lesions, and carcinomas in situ. The mucosal samples considered were more relevant for the evaluation of microbiota’s pathophysiological involvement in CR carcinogenesis, while non-invasive stool sampling could be beneficial for early CRC detection strategies in the future. Further studies are required to identify and validate mucosa-associated and luminal colorectal microbial patterns and their role in CRC carcinogenesis, as well as in the clinical setting of human microbiota studies. Full article
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<p>PRISMA flow diagram indicating the selection of studies for the systematic review.</p>
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<p>Bacterial abundances in tissue vs. stool samples in patients with precancerous colorectal lesions.</p>
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<p>Advantages and disadvantages of mucosal vs. stool samples usage in gut microbiota studies.</p>
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