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19 pages, 14492 KiB  
Article
Structural Parameter Design of Magnetic Pulse Welding Coil for Dissimilar Metal Joints: Numerical Simulation, Parameter Optimization, and Experiments
by Yangfan Qin, Changhui Ji, Hao Jiang, Yuefan Jiang, Junjia Cui and Guangyao Li
Machines 2025, 13(1), 28; https://doi.org/10.3390/machines13010028 - 6 Jan 2025
Viewed by 234
Abstract
As a main component of the magnetic pulse welding (MPW) system, the working coil exerts a great influence on the electromagnetic force and its distribution, which, in turn, affects the quality of the MPW joints. This study proposes a structural parameter optimization of [...] Read more.
As a main component of the magnetic pulse welding (MPW) system, the working coil exerts a great influence on the electromagnetic force and its distribution, which, in turn, affects the quality of the MPW joints. This study proposes a structural parameter optimization of the MPW coil, with the objective of achieving a higher induced current density on the flyer plate. The optimal Latin hypercube sampling technique (OLHS), Kriging approximate model, and the Non-Linear Programming by Quadratic Lagrangian (NLPQL) algorithm were employed in the optimization procedure, based on the finite element model built in LS-DYNA. The results of the sensitivity analysis indicated that all the selected parameters of the coil had a specific influence on the induced current density in the flyer plate. The optimized coil structure serves to refine the pulse current flowing path within the coil, effectively reducing the current loss within the coil. Additionally, the structure reduces the adverse effect of the current within the coil on the induced current within the flyer plate. Numerical results show the peak-induced current of the flyer plate increasing by 25.72% and the maximum Lorentz force rising by 58.10% at 25 kJ with the optimized coil structure. The experimental results show that with the same 25 kJ discharge energy, the optimized coil could increase the collision velocity from 359.92 m/s to 458.93 m/s. Moreover, 30 kJ of discharge energy should be needed to achieve the failure mode of base material failure with the original coil, while only 15 kJ should be applied to the optimized coil. These findings verify the optimization model and give some outline for coil design. Full article
(This article belongs to the Special Issue Design and Manufacturing for Lightweight Components and Structures)
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<p>Schematic diagram, experiment equipment, and the discharge current of MPW technology: (<b>a</b>) principle of discharge process; (<b>b</b>) MPW equipment and Photonic Doppler Velocimeter equipment; (<b>c</b>) discharge current and the fitted current curve.</p>
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<p>FE model of the MPW process.</p>
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<p>Comparison between experimental and simulated results: (<b>a</b>) velocity–displacement curve; (<b>b</b>) weldment appearance.</p>
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<p>Electromagnetic field simulation results of (<b>a</b>) current density cloud diagram within coil and Al/Cu sheets at 5 μs and (<b>b</b>,<b>c</b>) current density–time history in the central area of the coil and the Al sheet.</p>
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<p>Structural field simulation results of the flyer plate during the welding process: (<b>a</b>) effective plastic strain cloud diagram; (<b>b</b>) displacement in Z-direction.</p>
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<p>Schematic diagram of the coil shape dimensions and design variables: (<b>a</b>) configuration and dimensions of coil (unit: mm); (<b>b</b>) diagram of coil design parameters.</p>
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<p>Optimization flow chart of MPW coil.</p>
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<p>Pareto diagram of the optimized parameters of the coil.</p>
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<p>Kriging fitting surface of different parameters along inducted current density response: (<b>a</b>) the side arm width <span class="html-italic">A</span> and the bottom width <span class="html-italic">B</span>; (<b>b</b>) the side arm width <span class="html-italic">A</span> and the thickness <span class="html-italic">C</span>; (<b>c</b>) the bottom width <span class="html-italic">B</span> and the thickness <span class="html-italic">C</span>.</p>
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<p>Simulation results under the baseline coil design at 5μs: (<b>a</b>) discharge current density and Lorentz force distribution within the coil; (<b>b</b>) current density distribution within the Al sheet; (<b>c</b>) current density distribution within the copper sheet; (<b>d</b>) Lorentz force distribution within the Al sheet.</p>
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<p>Simulation results under the optimal coil design at 5 μs: (<b>a</b>) discharge current density and Lorentz force distribution within the coil; (<b>b</b>) current density distribution within the Al sheet; (<b>c</b>) current density distribution within the copper sheet; (<b>d</b>) Electric field distribution within the Al sheet; (<b>e</b>) Lorentz force distribution within the Al sheet.</p>
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<p>Velocity clouds comparison of Al sheet before and after optimization.</p>
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<p>Comparison of simulation results: (<b>a</b>) schematic diagram of different node locations, (<b>b</b>) current density–time curve; (<b>c</b>) Lorentz force–time curve; (<b>d</b>) velocity–time curve.</p>
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<p>Comparison of welding speed profiles before and after optimization: (<b>a</b>) welding speed–time curve; (<b>b</b>) physical coil before and after optimization.</p>
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<p>Experimental results of (<b>a</b>) diagram of the actual tensile tester and clamping of the welded parts, (<b>b</b>) tensile test results of welded joints welded by original coil, (<b>c</b>) tensile test results of welded joints welded by optimal coil.</p>
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<p>Mechanical experiment results for original and optimized coils: (<b>a</b>) tensile force–displacement performance of the joints at 15 kJ; (<b>b</b>) Weldability test results under different energy.</p>
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20 pages, 15749 KiB  
Article
Study on the Vibration Propagation Law and Stress Distribution Characteristics in Double-Arch Tunnels During Blasting
by Xiaofei Sun, Ying Su, Dunwen Liu, Yu Tang, Pei Zhang, Jishuang Hu and Xianghao Sun
Buildings 2025, 15(1), 139; https://doi.org/10.3390/buildings15010139 - 5 Jan 2025
Viewed by 448
Abstract
Highway tunnel construction in mountainous areas of China has been developing rapidly. The influence of drilling and blasting on the existing tunnel structure has become a key factor affecting the safety and stability of tunnel construction. The double-arch tunnel has unique structural characteristics. [...] Read more.
Highway tunnel construction in mountainous areas of China has been developing rapidly. The influence of drilling and blasting on the existing tunnel structure has become a key factor affecting the safety and stability of tunnel construction. The double-arch tunnel has unique structural characteristics. The propagation characteristics of blasting vibrations and the resulting stress responses exhibit a certain level of complexity. There is little research on the influence of single-line blasting excavation of double-arch tunnel on the other line tunnel. This paper analyzes the blasting vibration of a double-arch tunnel by ANSYS/LS-DYNA. The propagation law of blasting vibration velocity and stress distribution law of blasting vibration in different sections of the tunnel is revealed. At the same time, the relationship between the peak particle velocity (PPV) and tensile stress is established, and the threshold vibration velocity is proposed. It provides a scientific basis for tunnel design and construction. The propagation of blasting vibration in the adjacent roadway is affected by the middle pilot tunnel. The peak vibration velocity of different parts decreases with the increase in distance. The monitoring of vibration velocity and stress in section A of the right line of the adjacent tunnel should be strengthened, especially in the tunnel vault, blast-facing side wall, and arch foot. The difference in vibration strength across different tunnel parts provides a basis for optimizing the structure. It helps strengthen the parts susceptible to vibration during the design stage of the multi-arch tunnel, improving the tunnel’s safety and stability. Full article
(This article belongs to the Special Issue Dynamic Response of Civil Engineering Structures under Seismic Loads)
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<p>Borehole layout.</p>
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<p>The Blast-UM blasting vibrometer.</p>
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<p>Flowchart.</p>
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<p>The layout of the monitoring points.</p>
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<p>On-site monitoring equipment.</p>
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<p>Vibration diagram.</p>
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<p>PPV–frequency.</p>
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<p>Simulation result.</p>
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<p>Simulation result.</p>
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<p>Mesh fineness.</p>
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<p>Mesh quality.</p>
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<p>Material condition.</p>
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<p>Simulated vibration velocity on the blast-facing side.</p>
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<p>Simulated vibration velocity on the blast-opposite side.</p>
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<p>Effect of smooth blasting.</p>
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<p>Blast vibration propagation diagram.</p>
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<p>Section and selected points distribution diagram.</p>
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<p>The PPV distribution diagram 1.</p>
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<p>The PPV distribution diagram 2.</p>
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<p>Distribution of effective stresses.</p>
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<p>Unit selection and naming.</p>
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<p>Variation law of effective stresses.</p>
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<p>Maximum tensile stress–PPV.</p>
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13 pages, 3890 KiB  
Article
Thermo-Mechanical Coupled Analysis of Electric Vehicle Drive Shafts
by Se-Eun Kim, Chang-Ho Jung, Moon-Gu Lee, Sangwon Han, Jung-Lyul Park and Yongho Jeon
Appl. Sci. 2024, 14(24), 11768; https://doi.org/10.3390/app142411768 - 17 Dec 2024
Viewed by 392
Abstract
With the growing concerns over global warming and abnormal weather patterns, the development of eco-friendly technologies has emerged as a critical research area in the transportation industry. In particular, the global automotive market, one of the most widely used sectors, has witnessed a [...] Read more.
With the growing concerns over global warming and abnormal weather patterns, the development of eco-friendly technologies has emerged as a critical research area in the transportation industry. In particular, the global automotive market, one of the most widely used sectors, has witnessed a surge in research on electric vehicles (EVs) in line with these trends. Compared to traditional internal combustion engine vehicles, EVs require components with high strength and durability to achieve optimal performance. This study focuses on the development of a constant velocity (CV) joint, a critical component for reliably transmitting the maximum output of an electric vehicle motor. Unlike conventional numerical methods, the proposed thermo-mechanical coupled analysis simultaneously accounts for thermal and mechanical interactions, providing more realistic operational performance predictions. This analysis, conducted using the thermal modules of Ls-Dyna and ANSYS Mechanical, effectively simulated field operation scenarios. Prototype testing under simulated conditions showed a 6% discrepancy compared to numerical predictions, validating the high accuracy and reliability of the proposed method. This robust thermo-mechanical coupled analysis is expected to improve the durability and reliability of CV joint designs, advancing electric vehicle component development. Full article
(This article belongs to the Special Issue Mathematical Methods and Simulations in Mechanics and Engineering)
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<p>Schematic of ball spline joint.</p>
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<p>Proposed methodology.</p>
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<p>Angle of joint.</p>
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<p>Velocity vector. (<b>a</b>) Schematic of velocity vector. (<b>b</b>) Rotational speed.</p>
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<p>Resultant stress. (<b>a</b>) Stress of cage. (<b>b</b>) Effective stress of ball.</p>
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<p>Heat flux on parts. (<b>a</b>) Heat flux on outer race groove. (<b>b</b>) Heat flux on inner race groove. (<b>c</b>) Heat flux on cage. (<b>d</b>) Heat flux on ball.</p>
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<p>Resultant temperature. (<b>a</b>) Resultant temperature of all parts. (<b>b</b>) Resultant temperature of outer race. (<b>c</b>) Resultant temperature of cage wall. (<b>d</b>) Resultant temperature of ball.</p>
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<p>Experimental validation apparatus.</p>
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23 pages, 26520 KiB  
Article
A Study on the Impact of Different Delay Times on Rock Mass Throwing and Movement Characteristics Based on the FEM–SPH Method
by Guoqiang Wang, Hui Chen and Jingkun Zhao
Appl. Sci. 2024, 14(23), 11468; https://doi.org/10.3390/app142311468 - 9 Dec 2024
Viewed by 633
Abstract
Burst morphology is a crucial indicator for evaluating the effectiveness of blasting, as it directly reflects the actual state of the blasting results. The results of rock displacement following blasting partially reflect the effectiveness of throw blasting, while the rock ejection process serves [...] Read more.
Burst morphology is a crucial indicator for evaluating the effectiveness of blasting, as it directly reflects the actual state of the blasting results. The results of rock displacement following blasting partially reflect the effectiveness of throw blasting, while the rock ejection process serves as the macroscopic manifestation of the blasting method. To accurately assess the impact of different delay times on burst formation, this study addressed the issues of rock movement and ejection in underground blasting. Using three-dimensional modeling, we constructed a FEM–SPH model and utilized LS-DYNA numerical simulation software to investigate the movement patterns of rock in precise delayed blasting scenarios underground. This study explored the spatiotemporal evolution characteristics of rock movement post-blasting. Digital electronic detonators were used to set precise inter-row delay times of 25 ms, 50 ms, and 75 ms. The results revealed that the ejection distance of blasted rock in underground mining increased with longer inter-row delay times, while the slope angle of the blasted muck pile decreased as the delay time increased. Furthermore, at a micro level, the study found that a 75 ms delay created new free surfaces, providing effective compensation space for subsequent blasts, thereby improving blasting outcomes. Analysis of the 25 ms and 50 ms delay periods indicated a clamping effect on rock movement. Field comparisons of blasting results were conducted to validate the influence of precise delay times on the movement patterns and spatiotemporal evolution characteristics of blasted rock. Full article
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<p>Blasting design: (<b>a</b>) blast-hole arrangement, (<b>b</b>) initiation network.</p>
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<p>FEM–SPH numerical simulation modeling.</p>
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<p>Linear fit to calibrated A and N parameters.</p>
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<p>Schematic diagram of the ejection model of fragmented rock mass following the detonation of equivalent spherical charges in underground mining.</p>
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<p>Rock mass movement under different delay timing conditions following the detonation of blast holes. (25 ms (<b>a1</b>), 50 ms (<b>a2</b>), 75 ms (<b>a3</b>) represent the delay times of 25 ms, 50 ms, and 75 ms for the internal rock movement after the detonation of the first row of blast holes; 25 ms (<b>b1</b>), 50 ms (<b>b2</b>), 75 ms (<b>b3</b>) represent the same delay times for the second row; 25 ms (<b>c1</b>), 50 ms (<b>c2</b>), 75 ms (<b>c3</b>) for the third row; 25 ms (<b>d1</b>), 50 ms (<b>d2</b>), 75 ms (<b>d3</b>) for the fourth row; 25 ms (<b>e1</b>), 50 ms (<b>e2</b>), 75 ms (<b>e3</b>) for the fifth row; and 25 ms (<b>f1</b>), 50 ms (<b>f2</b>), 75 ms (<b>f3</b>) for the sixth row of blast holes, all indicating the subsequent internal rock movement).</p>
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<p>Rock mass movement under different delay timing conditions following the detonation of blast holes. (25 ms (<b>a1</b>), 50 ms (<b>a2</b>), 75 ms (<b>a3</b>) represent the delay times of 25 ms, 50 ms, and 75 ms for the internal rock movement after the detonation of the first row of blast holes; 25 ms (<b>b1</b>), 50 ms (<b>b2</b>), 75 ms (<b>b3</b>) represent the same delay times for the second row; 25 ms (<b>c1</b>), 50 ms (<b>c2</b>), 75 ms (<b>c3</b>) for the third row; 25 ms (<b>d1</b>), 50 ms (<b>d2</b>), 75 ms (<b>d3</b>) for the fourth row; 25 ms (<b>e1</b>), 50 ms (<b>e2</b>), 75 ms (<b>e3</b>) for the fifth row; and 25 ms (<b>f1</b>), 50 ms (<b>f2</b>), 75 ms (<b>f3</b>) for the sixth row of blast holes, all indicating the subsequent internal rock movement).</p>
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<p>Rock mass movement under different delay timing conditions following the detonation of blast holes. (25 ms (<b>a1</b>), 50 ms (<b>a2</b>), 75 ms (<b>a3</b>) represent the delay times of 25 ms, 50 ms, and 75 ms for the internal rock movement after the detonation of the first row of blast holes; 25 ms (<b>b1</b>), 50 ms (<b>b2</b>), 75 ms (<b>b3</b>) represent the same delay times for the second row; 25 ms (<b>c1</b>), 50 ms (<b>c2</b>), 75 ms (<b>c3</b>) for the third row; 25 ms (<b>d1</b>), 50 ms (<b>d2</b>), 75 ms (<b>d3</b>) for the fourth row; 25 ms (<b>e1</b>), 50 ms (<b>e2</b>), 75 ms (<b>e3</b>) for the fifth row; and 25 ms (<b>f1</b>), 50 ms (<b>f2</b>), 75 ms (<b>f3</b>) for the sixth row of blast holes, all indicating the subsequent internal rock movement).</p>
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<p>Overall trend of rock mass movement and comparison between numerical simulation and field blasting tests; (<b>a</b>) Movement of the fractured rock mass after detonation of the second row of blast holes; (<b>b</b>) Movement of the fractured rock mass after detonation of the third row of blast holes; (<b>c</b>) Movement of the fractured rock mass after detonation of the fourth row of blast holes; (<b>d</b>) Movement of the fractured rock mass after detonation of the fifth row of blast holes; (<b>e</b>) Movement of the fractured rock mass after detonation of the sixth row of blast holes; (<b>f</b>) Numerical simulation of roof fracturing (leading to rock face spalling); (<b>g</b>) Actual state of rock face spalling after on-site blasting; (<b>h</b>) Actual angle of rock face spalling after on-site blasting.</p>
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<p>Trend curves of rock mass movement under different delay conditions (various elevation levels).</p>
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<p>Trend curves of rock mass movement under different delay conditions (various elevation levels).</p>
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<p>Velocity–time curves of rock movement under different delay time conditions following blast-hole detonation.</p>
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<p>Burst morphology and ejection distances at the blast site.</p>
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20 pages, 4761 KiB  
Article
Geostress-Adaptive Charge Structure Design and Field Validation for Machinery Room Excavation
by Xiaocui Chen, Yuan Mi, Xinru Shuai, Yuan Zheng and Wenhu Zhao
Sensors 2024, 24(23), 7738; https://doi.org/10.3390/s24237738 - 3 Dec 2024
Viewed by 375
Abstract
The application of blasting in modern engineering construction is prized for its speed, efficiency, and cost-effectiveness. However, the resultant vibrations can have significant adverse effects on surrounding buildings and residents. The challenge of optimizing blasting procedures to satisfy excavation needs while minimizing vibration [...] Read more.
The application of blasting in modern engineering construction is prized for its speed, efficiency, and cost-effectiveness. However, the resultant vibrations can have significant adverse effects on surrounding buildings and residents. The challenge of optimizing blasting procedures to satisfy excavation needs while minimizing vibration impacts is a critical concern in blasting excavation. This research addresses this challenge through the development of a 3D simulation and analysis model for an underground pumped storage power plant in East China, utilizing the LS-DYNA finite element analysis software. To explore the influence of charging structures on rock fragmentation and vibration propagation, three distinct blasting programs were formulated, each featuring varied configurations within the machinery room. The analysis revealed that the adoption of an optimized charging structure can significantly decrease damage to the protective layer by approximately 40%, while also reducing the impact on the upstream and downstream side walls by 27.25% and 12.03%, respectively, without compromising the efficacy of the main blast zone. Moreover, the vibration velocities at the remote measurement point were found to be reduced across multiple directions, indicating effective control of the vibration effects. The post-implementation of the optimized blasting strategy at the site, the assessment of the retained surrounding rock integrity, and the impact on protected structures demonstrated that the proposed solution met satisfactory outcomes. This study underscores the potential of simulation-based optimization in managing vibration risks during blasting operations, offering a valuable tool for engineers and practitioners in the field of underground construction. Full article
(This article belongs to the Section Intelligent Sensors)
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<p>Schematic diagram of the cavern of the underground factory building.</p>
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<p>Schematic diagram of vibration velocity measurement.</p>
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<p>Field photographs of wave speed and stress.</p>
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<p>Overall model of the plant section to be excavated.</p>
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<p>Localized exposed bedrock of a pumped storage power plant.</p>
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<p>Schematic diagram of the excavation section model and grid segmentation in the machinery room.</p>
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<p>Three charge structures.</p>
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<p>Damage evolution of the surrounding rock in the blasting area.</p>
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<p>Damage evolution of the surrounding rock in the blasting area.</p>
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<p>Rock fragmentation morphology of the excavated section of the machinery room at 30 ms.</p>
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<p>Rock fragmentation morphology of the excavated section of the machinery room at 30 ms.</p>
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<p>Proportion of rock fragmentation at different locations.</p>
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<p>Surrounding rock damage under Case B.</p>
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<p>Time history curves of vibration velocity at each measuring point under three cases.</p>
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<p>Peak vibration velocity in different directions at each measurement point.</p>
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<p>On site diagram of charge layout.</p>
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<p>Variation in wave velocity with hole depth.</p>
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<p>Numerical simulation values and field survey values during the blasting of the machinery room.</p>
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23 pages, 4970 KiB  
Article
Sequential Multi-Scale Modeling Using an Artificial Neural Network-Based Surrogate Material Model for Predicting the Mechanical Behavior of a Li-Ion Pouch Cell Under Abuse Conditions
by Alexander Schmid, Christian Ellersdorfer, Eduard Ewert and Florian Feist
Batteries 2024, 10(12), 425; https://doi.org/10.3390/batteries10120425 - 1 Dec 2024
Viewed by 583
Abstract
To analyze the safety behavior of electric vehicles, mechanical simulation models of their battery cells are essential. To ensure computational efficiency, the heterogeneous cell structure is represented by homogenized material models. The required parameters are calibrated against several characteristic cell experiments. As a [...] Read more.
To analyze the safety behavior of electric vehicles, mechanical simulation models of their battery cells are essential. To ensure computational efficiency, the heterogeneous cell structure is represented by homogenized material models. The required parameters are calibrated against several characteristic cell experiments. As a result, it is hardly possible to describe the behavior of the individual battery components, which reduces the level of detail. In this work, a new data-driven material model is presented, which not only provides the homogenized behavior but also information about the components. For this purpose, a representative volume element (RVE) of the cell structure is created. To determine the constitutive material models of the individual components, different characterization tests are performed. A novel method for carrying out single-layer compression tests is presented for the characterization in the thickness direction. The parameterized RVE is subjected to a large number of load cases using first-order homogenization theory. This data basis is used to train an artificial neural network (ANN), which is then implemented in commercial FEA software LS-DYNA R9.3.1 and is thus available as a material model. This novel data-driven material model not only provides the stress–strain relationship, but also outputs information about the condition of the components, such as the thinning of the separator. The material model is validated against two characteristic cell experiments. A three-point-bending test and an indentation test of the cell is used for this purpose. Finally, the influence of the architecture of the neural network on the computational effort is discussed. Full article
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<p>Different scales of experiments and simulations of electric vehicles.</p>
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<p>Modeling concept for data-driven multi-scale approach.</p>
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<p>(<b>a</b>) Initial configuration. (<b>b</b>) Deformed configuration with linear boundary conditions. (<b>c</b>) Deformed configuration with periodic boundary conditions.</p>
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<p>Training space for normal directions.</p>
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<p>Architecture of a feed-forward neural network with three inputs, three outputs, and two hidden layers with six neurons each.</p>
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<p>Different experimental setups for characterization and validation of component and cell level: (<b>a</b>) In-plane characterization of components. (<b>b</b>) Novel out-of-plane characterization of components. (<b>c</b>) Three-point-bending test. (<b>d</b>) Indentation test with cylindrical impactor.</p>
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<p>Results of the tensile tests for the in-plane characterization of the components: (<b>a</b>) Separator. (<b>b</b>) Anode. (<b>c</b>) Cathode. (<b>d</b>) Pouch.</p>
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<p>Results of the compression tests for the out-of-plane characterization of the components: (<b>a</b>) Anode. (<b>b</b>) Cathode. (<b>c</b>) Separator.</p>
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<p>(<b>a</b>) Comparison of component behavior detailed RVE vs. ANN single element. (<b>b</b>) Results of neural network training.</p>
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<p>Comparison of experimental and simulative force–displacement curves for (<b>a</b>) three-point-bending test, (<b>b</b>) indentation test with cylindrical impactor, and (<b>c</b>) predicted separator true strain for different intrusions as well as (<b>d</b>) comparison of relative simulation duration for different network architectures.</p>
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16 pages, 5687 KiB  
Article
The Effect of Protective Barriers on the Dynamic Response of Underground Structures
by Behnam Mobaraki and Mohammad Vaghefi
Buildings 2024, 14(12), 3764; https://doi.org/10.3390/buildings14123764 - 26 Nov 2024
Viewed by 456
Abstract
Engineers have dedicated considerable attention over the past ten years to studying the influences of dynamic loads caused by both intentional and unintentional events on infrastructures. As a result, determining how buried structures react to explosions and enhancing their security against blast loads [...] Read more.
Engineers have dedicated considerable attention over the past ten years to studying the influences of dynamic loads caused by both intentional and unintentional events on infrastructures. As a result, determining how buried structures react to explosions and enhancing their security against blast loads have become crucial subjects in defensive engineering. To achieve this goal, constructing a protective barrier, which is known as a blast wall, in front of structures can be an effective measure. This research focused on examining the impact of a protective barrier on the response of a box-shaped tunnel located in Kobe, Japan, using a comprehensive numerical approach. The results revealed that incorporating a barrier with widths of either 1 m or 2 m resulted in a significant reduction in peak pressure. Specifically, the use of a 1 m wide barrier resulted in a 77% decrease, while a 2 m wide barrier achieved an even greater reduction of 84%. Additionally, it was observed that minimizing the distance between the barrier and the explosion point, as well as increasing the width of the barrier, resulted in reduced peak pressure throughout all sections of the tunnel. Full article
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<p>Number of publications associated with blast response of different types of structures referenced in the Scopus database.</p>
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<p>Configuration of problem.</p>
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<p>Schematic of the finite element model.</p>
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<p>Triaxial hydrostatic compression data for sandy loam [<a href="#B45-buildings-14-03764" class="html-bibr">45</a>].</p>
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<p>Comparison between peak pressure of finite element model and TM5-855-1.</p>
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<p>Comparison between peak acceleration of finite element model and TM5-855-1.</p>
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<p>Stress distribution in the protective barrier for L/D = 0.4 (<b>a</b>) and L/D = 0.8 (<b>b</b>), illustrating the effect of barrier distance on blast mitigation.</p>
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<p>Impact of barrier length on vertical stress reduction for <math display="inline"><semantics> <mrow> <mi mathvariant="normal">L</mi> <mo>/</mo> <mi mathvariant="normal">D</mi> </mrow> </semantics></math> = 0.8: case 4 (<b>a</b>) and case 8 (<b>b</b>).</p>
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<p>Position of critical elements in the finite element model.</p>
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<p>The variation of the peak pressure at point 1 for cases 1, 5, and 10.</p>
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<p>The variation of the peak pressure at point 2 for cases 1, 5, and 10.</p>
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<p>The variation of the peak pressure for cases 3 and 5.</p>
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<p>Variation of <math display="inline"><semantics> <mrow> <mi>L</mi> <mo>/</mo> <mi>D</mi> </mrow> </semantics></math> on blast response of tunnel.</p>
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20 pages, 5725 KiB  
Article
Analysis of Damage Factors of Reinforced Concrete Frame Under Internal Explosion
by Jiaxin Li, Jianping Yin, Xudong Li and Shi Rui
Buildings 2024, 14(12), 3761; https://doi.org/10.3390/buildings14123761 - 26 Nov 2024
Viewed by 502
Abstract
To explore the mechanisms of the damage to reinforced concrete (RC) frame structures subjected to internal explosions, this paper establishes a precise finite element model (FEM) of an RC frame utilizing ANSYS/LS-DYNA software 14.5. The influence of four important damage factors on the [...] Read more.
To explore the mechanisms of the damage to reinforced concrete (RC) frame structures subjected to internal explosions, this paper establishes a precise finite element model (FEM) of an RC frame utilizing ANSYS/LS-DYNA software 14.5. The influence of four important damage factors on the degree of structural damage is systematically analyzed. Specifically, the vertical displacement at the top center of the frame serves as the primary evaluation metric, while the four damage factors are treated as independent variables. An empty column is incorporated as an error term, facilitating a five-factor, four-level orthogonal optimization design for the simulation experiments. Based on this design, a variance analysis of the simulation outcomes is conducted. The results show that by increasing the reinforcement ratio of the beam section and reducing the charge weight, when the explosion point is located at the higher part of the building floor and near the external window, the vertical displacement of the building after the internal explosion can be reduced. The order of the influence degree of each damage factor on the damage to the reinforced concrete frame structure is as follows: explosion floor, charge weight, beam section reinforcement ratio, and explosion horizontal position. Full article
(This article belongs to the Section Building Structures)
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<p>Schematic diagram of geometric structure of building: (<b>a</b>) geometric size of building structure; (<b>b</b>) plane layout; (<b>c</b>) reinforcement details of beam; (<b>d</b>) reinforcement details of column.</p>
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<p>Schematic diagram of Beam161 unit.</p>
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<p>Schematic diagram of SOLID164 unit.</p>
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<p>The influence of different mesh sizes on the vertical displacement of the top of the RC frame.</p>
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<p>FEM of frame structure.</p>
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<p>PLASTIC_KINEMATIC model.</p>
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<p>Test model [<a href="#B31-buildings-14-03761" class="html-bibr">31</a>] and FEM. (<b>a</b>) is the test model; (<b>b</b>) is the FEM.</p>
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<p>Grid convergence verification of test model: (<b>a</b>) the influence of different mesh sizes on peak acceleration; (<b>b</b>) the influence of different mesh sizes on the calculation time.</p>
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<p>Dynamic response of a structure under the action of 50 g of emulsion explosives: (<b>a</b>) acceleration response curve of A2; (<b>b</b>) acceleration response curve of A3; (<b>c</b>) the frequency–power spectral density curve of A2; (<b>d</b>) the frequency–power spectral density curve of A3.</p>
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<p>Characteristic response of structural damage under 200 g emulsion explosives: (<b>a</b>) holistic model; (<b>b</b>) the top of the frame; (<b>c</b>) beam–column joint.</p>
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<p>The influence of reinforcement ratio on RC frame damage.</p>
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<p>The influence of the charge weight on the damage to RC frame.</p>
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<p>The influence of horizontal position of explosion on the damage to RC frame.</p>
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<p>The effect of the floor where the explosion occurred on the damage to the RC frame.</p>
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<p>Frame structure damage cloud map at different moments: (<b>a</b>) 8 ms; (<b>b</b>) 40 ms; (<b>c</b>) 650 ms; (<b>d</b>) 2000 ms.</p>
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16 pages, 12639 KiB  
Article
Study on the Crashworthiness of a Battery Frame Design for an Electric Vehicle Using FEM
by Adrian Daniel Muresanu, Mircea Cristian Dudescu and David Tica
World Electr. Veh. J. 2024, 15(11), 534; https://doi.org/10.3390/wevj15110534 - 19 Nov 2024
Viewed by 912
Abstract
This paper presents an optimized method for evaluating and enhancing the crashworthiness of an electric vehicle (EV) battery frame, leveraging finite element model (FEM) simulations with minimal computational effort. The study begins by utilizing a publicly available LS-DYNA model of a conventional Toyota [...] Read more.
This paper presents an optimized method for evaluating and enhancing the crashworthiness of an electric vehicle (EV) battery frame, leveraging finite element model (FEM) simulations with minimal computational effort. The study begins by utilizing a publicly available LS-DYNA model of a conventional Toyota Camry, simplifying it to include only the structures relevant to a side pole crash scenario. The crash simulations adhere to FMVSS214 and UNR135 standards, while also extending to higher speeds of 45 km/h to evaluate performance under more severe conditions. A dummy frame with virtual mass is integrated into the model to approximate the realistic center of gravity (COG) of an EV and to facilitate visualization. Based on the side pole crash results, critical parameters are extracted to inform the development of load cases for the EV battery. The proposed battery frame, constructed from aluminum, houses a representative volume of battery cells. These cells are defined through a homogenization process derived from individual and pack of cell crash tests. The crashworthiness of the battery frame is assessed by measuring the overall intrusion along the Y-axis and the specific intrusion into the representative volume. This method not only highlights the challenges of adapting conventional vehicle platforms for EVs or for dual compatibility with both conventional and electric powertrains but also provides a framework for developing and testing battery frames independently. By creating relevant load cases derived from full vehicle crash data, this approach enables battery frames to be optimized and evaluated as standalone components, offering a method for efficient and adaptable battery frame development. This approach provides a streamlined yet effective process for optimizing the crash performance of EV battery systems within existing vehicle platforms. Full article
(This article belongs to the Special Issue Electric Vehicle Crash Safety Design)
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<p>FEM conversion of the sedan Toyota Camry [<a href="#B18-wevj-15-00534" class="html-bibr">18</a>].</p>
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<p>Toyota Camry 2012 FEM simplification: (<b>a</b>) original model, bottom view; (<b>b</b>) original model, side middle-section view; (<b>c</b>) simplified model, bottom view; and (<b>d</b>) simplified model, side middle-section view.</p>
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<p>Part groups for virtual mass: (<b>a</b>) front-part group, (<b>b</b>) back-part group, and (<b>c</b>) middle-part group.</p>
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<p>Battery dummy frame under the transparent EV model.</p>
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<p>Positions of the pole barriers.</p>
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<p>Internal energies graphics of each load case.</p>
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<p>Energies diagram vs. intrusions.</p>
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<p>Intrusion of the pole until contact with the battery frame, cut on X and top view.</p>
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<p>Maximal intrusion of the pole, cut on X and top view.</p>
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<p>Battery frame configurations.</p>
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<p>Compression test configuration including 10 cells and representing volume.</p>
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<p>Cell-pressing simulation doubled in size.</p>
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<p>Load–displacement curves matching.</p>
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<p>V1 configuration results.</p>
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<p>V2 configuration results.</p>
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<p>V3 configuration results.</p>
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<p>V4 configuration results.</p>
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15 pages, 4340 KiB  
Article
A Study on the Attenuation Patterns of Underground Blasting Vibration and Their Impact on Nearby Tunnels
by Zhengrong Li, Zhiming Cheng, Yulian Shi, Yongjie Li, Yonghui Huang and Zhiyu Zhang
Appl. Sci. 2024, 14(22), 10651; https://doi.org/10.3390/app142210651 - 18 Nov 2024
Viewed by 649
Abstract
The natural caving method, as a new technique in underground mining, has been promoted and applied in several countries worldwide. The destruction of the bottom rock mass structure directly impacts the structural stability of underground engineering, resulting in damage and collapse of underground [...] Read more.
The natural caving method, as a new technique in underground mining, has been promoted and applied in several countries worldwide. The destruction of the bottom rock mass structure directly impacts the structural stability of underground engineering, resulting in damage and collapse of underground tunnels. Therefore, based on the principles of explosion theory and field monitoring data, a scaled three-dimensional numerical simulation model of underground blasting was constructed using LS-DYNA19.0 software to investigate the attenuation patterns of underground blasting vibrations and their impact on nearby tunnels. The results show that the relative error range between the simulated blasting vibration velocities based on the FEM-SPH (Finite Element Method–Smoothed Particle Hydrodynamics) algorithm and the measured values is between 7.75% and 9.85%, validating the feasibility of this method. Significant fluctuations in blasting vibration velocities occur when the blast center increases to within a range of 10–20 m. As the blast center distance exceeds 25 m, the vibration velocities are increasingly influenced by the surrounding stress. Additionally, greater stress results in higher blasting vibration velocities and stress wave intensities. Fitting the blasting vibration velocities of various measurement points using the Sadovsky formula yields fitting correlation coefficients ranging between 0.92 and 0.97, enabling the prediction of on-site blasting vibration velocities based on research findings. Changes in propagation paths lead to localized fluctuations in the numerical values of stress waves. These research findings are crucial for a deeper understanding of underground blasting vibration patterns and for enhancing blasting safety. Full article
(This article belongs to the Special Issue New Insights into Digital Rock Physics)
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<p>Schematic diagram of three-dimensional modeling for underground blasting engineering.</p>
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<p>Diagram of model grid division and positions of vibration measurement points.</p>
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<p>Layout diagram of underground blasting engineering.</p>
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<p>Model diagram with applied initial boundary conditions.</p>
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<p>Stress state diagram of the model under initial in situ stress load.</p>
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<p>Vibration velocity history curves of various measurement points under in situ stress of 1 MPa and 5 MPa.</p>
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<p>Layout of vibration wave monitoring points in the tunnel at the blasting site.</p>
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<p>Graph of field-measured three-axis vibration velocity history.</p>
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<p>Stress history curve of various measurement points under in situ stress of 1 MPa and 5 MPa.</p>
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<p>The stress distribution at different measurement points under in situ stress of 1 MPa and 5 MPa.</p>
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<p>Displacement history curve of various measurement points under in situ stress of 1 MPa and 5 MPa.</p>
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23 pages, 12151 KiB  
Article
Study on the Suitability of Concrete Constitutive Models for Perforation Simulation
by Jianxing Li, Yize Liu, Peiyu Li, Haifu Wang and Pengwan Chen
Materials 2024, 17(22), 5562; https://doi.org/10.3390/ma17225562 - 14 Nov 2024
Viewed by 754
Abstract
The choice of constitutive model significantly affects the accuracy of concrete perforation simulation. This study analyzes four concrete constitutive models, HJC, RHT, KCC, and TCK, focusing on their strength models, damage evolution, and strain rate effects. Combining the damage pattern and erosion cracks, [...] Read more.
The choice of constitutive model significantly affects the accuracy of concrete perforation simulation. This study analyzes four concrete constitutive models, HJC, RHT, KCC, and TCK, focusing on their strength models, damage evolution, and strain rate effects. Combining the damage pattern and erosion cracks, the effectiveness of the four constitutive models in simulating the penetration of reinforced concrete targets is evaluated using LS-DYNA 11.0. The results indicate that the RHT and TCK models accurately depict the concrete damage and failure modes under the same test conditions. In contrast, the KCC and HJC models demonstrate superior capability in predicting the residual velocity of the projectile. Additionally, this study highlights the significant impact of the erosion parameters on the simulation results. This study offers a valuable reference for the application and parameter set of constitutive models in simulating concrete target perforation. Full article
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<p>The EOS of the HJC model.</p>
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<p>Strength surfaces in deviatoric and meridian planes.</p>
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<p>The damage evolution of HJC and RHT models.</p>
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<p>The damage evolution of the KCC model.</p>
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<p>Compressive and tensile strain rate effects.</p>
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<p>The target size and projectile used in the test.</p>
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<p>The numerical simulation model.</p>
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<p>Uniaxial compression stress–strain curves at different strain rates (<span class="html-italic">f</span><sub>c</sub> = 48 MPa).</p>
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<p>Uniaxial tensile stress–strain curves at different strain rates (<span class="html-italic">f</span><sub>t</sub> = 4 MPa).</p>
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<p>The damage pattern on the front face of the concrete targets.</p>
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<p>The damage pattern on the back face of the concrete targets.</p>
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<p>A section view of the damage pattern in concrete targets.</p>
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<p>The experiment results of the front face [<a href="#B34-materials-17-05562" class="html-bibr">34</a>].</p>
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<p>The simulation results of the failure pattern on the front face.</p>
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<p>A comparison of the simulation and test results of the front cratering range.</p>
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<p>The experimental results of the back face [<a href="#B34-materials-17-05562" class="html-bibr">34</a>].</p>
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<p>The simulation results of the failure pattern on the back face.</p>
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<p>A comparison of the simulation and test results of the back scrabbing range.</p>
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<p>An isometric view of the overall failure pattern.</p>
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<p>The residual velocity at different conditions.</p>
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<p>The effect of <span class="html-italic">e<sub>c</sub></span> on the simulation results of the penetration test.</p>
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<p>The effects of <span class="html-italic">e<sub>t</sub></span> on the simulation results of the penetration test.</p>
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21 pages, 10123 KiB  
Article
Development of an FEM for the Combined Electromagnetic and Hydraulic Forming Process Based on Experimental Data
by Yoonho Jang and Jeong Kim
Processes 2024, 12(11), 2520; https://doi.org/10.3390/pr12112520 - 12 Nov 2024
Viewed by 601
Abstract
Electrohydraulic forming (EHF) which demonstrates reduced bouncing effect, formation in narrow areas, and no effect on the electrical conductivity of the blank can overcome the shortcomings of deep drawing and electromagnetic forming. However, considerable time is involved in evaluating the possibility of forming [...] Read more.
Electrohydraulic forming (EHF) which demonstrates reduced bouncing effect, formation in narrow areas, and no effect on the electrical conductivity of the blank can overcome the shortcomings of deep drawing and electromagnetic forming. However, considerable time is involved in evaluating the possibility of forming a specific part through experiments. Developing an accurate finite element model can reduce the opportunity costs of an experiment by reducing unnecessary trial and error in forming a specific part. In this study, the chamber, die, and blank components of the EHF experimental equipment in our laboratory were reverse-modeled using CATIA V5R18. Subsequently, the IGES format of the components was imported into LS-DYNA R12, and an FEM model to simulate the EHF experiment was constructed. The experimental and simulation results of nine cases, based on the SUS430 material, input voltage, and blank thickness, were compared for model verification. The forming results for all cases in the constructed finite element analysis model nearly matched the experimental results. Moreover, the linear increase in the blank thickness with input voltage and thickness was simultaneously confirmed. In a computing environment using a 4.3 GHz, 24-Core CPU and 64 GB memory, the time required for one finite element analysis was approximately 1 h. Full article
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<p>Process of EHF experiment.</p>
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<p>EHF apparatus: 3D model (<a href="#processes-12-02520-f003" class="html-fig">Figure 3</a>).</p>
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<p>Cross-section of the essential parts of EHF.</p>
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<p>Locational parameters of EHF force.</p>
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<p>Current curves measured by Rogowski coil and oscilloscope.</p>
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<p>Voltage curves measured by probe and oscilloscope.</p>
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<p>Power curve calculated by the measured voltage and current.</p>
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<p>Electric energy curve calculated by integrating the power curve.</p>
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<p>Schematic of surface measurement obtained for 2D contour.</p>
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<p>Experimental result of 0.3 mm blank.</p>
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<p>Experimental result of 0.5 mm blank.</p>
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<p>Experimental result of 0.7 mm blank.</p>
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<p>Modeling of the EHF components for finite element method (FEM).</p>
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<p>Arbitrary Lagrangian–Eulerian part divided into plasma, working fluid, and surrounding air.</p>
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<p>Plastic region strain-stress diagram of SUS430 according to the strain rate.</p>
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<p>Simulation process of constructed EHF FEM.</p>
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<p>Simulation result with 0.3 mm blank.</p>
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<p>Simulation result with 0.5 mm blank.</p>
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<p>Simulation result with 0.7 mm blank.</p>
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<p>(<b>a</b>) Simulation and experimental results with 0.3 mm blank and 6 kV input voltage. (<b>b</b>) Simulation and experimental results with 0.3 mm blank and 7 kV input voltage. (<b>c</b>) Simulation and experimental results with 0.3 mm blank and 8 kV input voltage.</p>
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<p>(<b>a</b>) Simulation and experimental results with 0.5 mm blank and 6 kV input voltage. (<b>b</b>) Simulation and experimental results with 0.5 mm blank and 7 kV input voltage. (<b>c</b>) Simulation and experimental results with 0.5 mm blank and 8 kV input voltage.</p>
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<p>(<b>a</b>) Simulation and experimental results with 0.7 mm blank and 6 kV input voltage. (<b>b</b>) Simulation and experimental results with 0.7 mm blank and 7 kV input voltage. (<b>c</b>) Simulation and experimental results with 0.7 mm blank and 8 kV input voltage.</p>
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<p>Increase rate of the maximum bulge height with input voltage for each specimen.</p>
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21 pages, 9157 KiB  
Article
Numerical Study of Air Cushion Effect in Notched Disk Water Entry Process Using Structured Arbitrary Lagrangian–Eulerian Method
by Zhe Zhang, Nana Yang, Jinlong Ju, Xingzhi Bai, Houcun Zhou and Wenhua Wu
J. Mar. Sci. Eng. 2024, 12(11), 2012; https://doi.org/10.3390/jmse12112012 - 8 Nov 2024
Viewed by 501
Abstract
This paper presents a novel numerical investigation into the air cushion effect and impact loads during the water entry of notched discs, utilizing the Structured Arbitrary Lagrangian–Eulerian (S-ALE) algorithm in LS-DYNA. Unlike prior studies that focused on smooth or unnotched geometries, the present [...] Read more.
This paper presents a novel numerical investigation into the air cushion effect and impact loads during the water entry of notched discs, utilizing the Structured Arbitrary Lagrangian–Eulerian (S-ALE) algorithm in LS-DYNA. Unlike prior studies that focused on smooth or unnotched geometries, the present study explores how varying notch parameters influence the fluid–solid coupling process during high-speed water entry. The reliability and accuracy of the computational method are validated through grid independence verification and comparisons with experimental data and empirical formulas. Systematic analysis of the effects of notch size, water entry velocity, and entry angle on the evolution of the free surface, impact loads, and structural responses uncovers several novel findings. Notably, increasing the notch diameter significantly enhances the formation and stability of the air cushion, leading to a considerable reduction in peak impact loads—a phenomenon not previously quantified. Additionally, higher water entry Froude numbers are shown to accelerate air cushion compression and formation, markedly affecting free surface morphology and force distribution. The results also reveal that varying the water entry angle alters the air cushion’s morphological characteristics, where larger angles induce a more pronounced but less stable air cushion, influencing the internal structural response differently across regions. Full article
(This article belongs to the Section Ocean Engineering)
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<p>Diagram of flat-plate impact into water.</p>
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<p>(<b>a</b>) Total plate force; (<b>b</b>) centre plate pressure.</p>
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<p>Air cushion effect of disc impact.</p>
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<p>(<b>a</b>) The disc forms a notch on the impact surface; (<b>b</b>) disc top view; (<b>c</b>) the disc hits the water, and the free surface is displaced by the air compression surface.</p>
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<p>Computational domain. (<b>a</b>) Boundary condition diagram. (<b>b</b>) The percentage of the mesh refinement area to the base size. (<b>c</b>) Initial VOF fractions: red represents air, blue represents water, and the board is white (dimensions are measured in disc diameter).</p>
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<p>(<b>a</b>) Computational efficiency for different grid size; (<b>b</b>) Comparison of pressure at different grid sizes.</p>
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<p>Time-step independent verification.</p>
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<p>(<b>a</b>) Punishment function mechanism diagram; (<b>b</b>) impact pressures for disc models with different <math display="inline"><semantics> <mrow> <msub> <mi>p</mi> <mi>f</mi> </msub> </mrow> </semantics></math> values.</p>
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<p>(<b>a</b>) The time history of the pressure of discs with different <math display="inline"><semantics> <mi>d</mi> </semantics></math> values during the attack process. (<b>b</b>) The standard deviation of peak pressure during disc attacks.</p>
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<p>(<b>a</b>) Evolution of free surface under different <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>/</mo> <mi>D</mi> </mrow> </semantics></math> conditions; (<b>b</b>) a comparative analysis of the maximum air cushion thickness in relation to varying notch diameters.</p>
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<p>Schematic of flow field with different notch diameters. (<b>a</b>) Flow field pressure; (<b>b</b>) volume fraction of flow field.</p>
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<p>The impact force of the <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>=</mo> <mn>60</mn> </mrow> </semantics></math> disc at different speeds.</p>
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<p>(<b>a</b>) Time series of impulse when <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>=</mo> <mn>60</mn> </mrow> </semantics></math> at different impact velocities. All time series are centred on <math display="inline"><semantics> <mrow> <mi>t</mi> <mo>=</mo> <mn>0</mn> </mrow> </semantics></math>, the moment when the pressure at the centre of the disc reaches its maximum. (<b>b</b>) The cumulative impulse of different <math display="inline"><semantics> <mi>d</mi> </semantics></math> during the first shock peak compared with the theoretical value [<a href="#B17-jmse-12-02012" class="html-bibr">17</a>,<a href="#B28-jmse-12-02012" class="html-bibr">28</a>,<a href="#B29-jmse-12-02012" class="html-bibr">29</a>].</p>
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<p>Evolution of the air cushion of a 60 mm disc with a groove diameter for different Fr values: (<b>a</b>) air cushion change at the same time t = 6 ms; (<b>b</b>) comparison of the moments of maximum air cushion thickness.</p>
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<p>(<b>a</b>) Pressure load distribution of d = 60 mm disc for different Fr values; (<b>b</b>) time course of air cushion thickness variation for different Fr values.</p>
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<p>(<b>a</b>) Resistance curve with time with different speeds; (<b>b</b>) resistance coefficient curve with time with different speeds.</p>
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<p>(<b>a</b>) Velocity variation in the disc during water entry at different tilt angles (3°, 5°, 6°); (<b>b</b>) angle change in the disc during water entry with different initial inclination angles.</p>
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<p>Stress cloud images for a disc with <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>=</mo> <mn>60</mn> <mo> </mo> <mi>mm</mi> </mrow> </semantics></math> and velocity of 2 m/s tilted at different angles (3°, 5°).</p>
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<p>Time chart of force: (<b>a</b>) velocity: 3 m/s, <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>3</mn> <mo>°</mo> </mrow> </semantics></math>, distance y = 0 (the midpoint of the <span class="html-italic">Y</span>-axis direction of the disc; the tilt is positive), and load curve at different distances; (<b>b</b>) load curve at a speed of 2 m/s and <math display="inline"><semantics> <mrow> <mi>θ</mi> <mo>=</mo> <mn>3</mn> <mo>°</mo> </mrow> </semantics></math>.</p>
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<p>Evolution of free liquid surface when the disc with a notch <math display="inline"><semantics> <mrow> <mi>d</mi> <mo>=</mo> <mn>60</mn> <mo> </mo> <mi>mm</mi> </mrow> </semantics></math> is impacted at different attitude angles.</p>
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19 pages, 14426 KiB  
Article
Numerical Simulation of Ice and Structure Interaction Using Common-Node DEM in LS DYNA
by Xiaolong Bai, Yin Jiang, Zhongxiang Shen, Renwei Liu and Zhen Liu
J. Mar. Sci. Eng. 2024, 12(11), 1999; https://doi.org/10.3390/jmse12111999 - 6 Nov 2024
Viewed by 641
Abstract
In this work, the icebreaking performance of the cone structure was investigated using a new numerical model called the common-node DEM developed within LS DYNA. The icebreaking characteristics of a typical conical jacket platform in the Bohai Sea focusing on the JZ20-2NW single-pile-leg [...] Read more.
In this work, the icebreaking performance of the cone structure was investigated using a new numerical model called the common-node DEM developed within LS DYNA. The icebreaking characteristics of a typical conical jacket platform in the Bohai Sea focusing on the JZ20-2NW single-pile-leg platform was studied and the ice load characteristics of the cone structure and the dynamic response of the jacket platform under various ice conditions was investigated. The findings indicate that ice thickness significantly impacts the icebreaking mechanism of the cone structure. Specifically, both the peak ice load and the peak acceleration of ice-induced vibrations are proportional to the square of the ice thickness. Additionally, the upward trend in positive vibration displacement of the jacket platform becomes more pronounced with increasing ice thickness. While both the acceleration and displacement caused by ice-induced vibrations on the jacket increase with rising ice velocity, this effect is less significant compared to the influence of ice thickness. Importantly, the ice load remains below the yield strength of the conical shell plate, demonstrating that traditional conical shell plate structures possess a margin of strength redundancy. Full article
(This article belongs to the Section Ocean Engineering)
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<p>Schematic diagram of common-node DEM-SPH particles.</p>
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<p>A schematic for model contact.</p>
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<p>The JZ20-2NW offshore platform.</p>
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<p>Illustration for sea ice and the JZ20-2NW platform interaction.</p>
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<p>Natural frequencies and modes of the first six modes of JZ20-2NW model.</p>
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<p>Interaction between sea ice and JZ20-2NW under different ice thicknesses.</p>
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<p>Ice load history of vertebral body structure under different ice thicknesses with 0.24, 0.30, 0.36 and 0.42 m.</p>
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<p>Ice load history of vertebral body structure under different ice thicknesses with 0.24, 0.30, 0.36 and 0.42 m.</p>
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<p>Ice load versus ice thickness.</p>
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<p>Peak ice force obtained by simulation and formula under different ice thicknesses.</p>
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<p>Time-history curve of ice-induced vibration acceleration of deck platform under different ice thicknesses.</p>
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<p>Time-history curve of ice-induced vibration acceleration of deck platform under different ice thicknesses.</p>
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<p>Relationship between peak acceleration of ice-induced vibration and ice thickness. (<b>a</b>) Ice-induced vibration versus ice thickness. (<b>b</b>) Ice induced vibration versus the square of ice thickness.</p>
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<p>Time-history curve of ice-induced vibration displacement for the JZ20-2NW platform at various ice thicknesses.</p>
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<p>Time-history curve of ice-induced vibration displacement for the JZ20-2NW platform at various ice thicknesses.</p>
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<p>Time-history curve of surface stress of conical shell plate with different ice thicknesses.</p>
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<p>Ice load time-history curve at different ice speeds.</p>
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<p>Time-history curve of ice-induced vibration acceleration of deck platform at different ice speeds.</p>
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<p>Time-history curve of ice-induced vibration displacement of deck platform at different ice speeds.</p>
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<p>Time-history curve of surface stress of conical shell plate at different ice speeds with 0.3, 0.4, 0.5 and 0.6 m/s.</p>
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17 pages, 6403 KiB  
Article
The Mechanical Properties and the Threshing Damage and Its Effects on Nutritional Quality of Buckwheat Grains
by Yun Liu, Yang Zhang, Lufei Yang, Shuai Feng, Haoran Yan and Decong Zheng
Agronomy 2024, 14(11), 2585; https://doi.org/10.3390/agronomy14112585 - 1 Nov 2024
Viewed by 830
Abstract
Buckwheat grains will suffer varying degrees of damage during the threshing process. Damaged grains are prone to changes in nutritional quality during storage. To explore the relationship between the threshing damage mechanism and nutritional quality, the mechanical properties of buckwheat with different moisture [...] Read more.
Buckwheat grains will suffer varying degrees of damage during the threshing process. Damaged grains are prone to changes in nutritional quality during storage. To explore the relationship between the threshing damage mechanism and nutritional quality, the mechanical properties of buckwheat with different moisture contents were determined through compression and friction tests, obtaining some conventional mechanical property indicators. On this basis, a 3D collision model of buckwheat–nail tooth was established, and the dynamic process of collision was simulated with LS-DYNA. During collision, the changes in energy, von Mises stress, and critical damage velocity of grains with different moisture contents were analyzed. After the threshing test, the grains were observed and classified according to the degree of damage. The differences in nutritional components of different types of grains were analyzed through physicochemical experiments. The experimental results showed that the failure force, elastic modulus, and ultimate strength of buckwheat grains were negatively correlated with moisture content, while the deformation and friction coefficient were positively correlated with moisture content. During collision, the von Mises stress of the grains showed a pattern of increase and then decrease. The maximum stress value occurred at the contact area center, spreading along the periphery and gradually decreasing. The maximum von Mises stress decreased with increasing moisture content and increased with increasing collision velocity. The critical damage velocities of grains at moisture contents of 11.98%, 15.77%, 18.04%, 20.82%, and 25.22% were 13.07, 11.72, 10.94, 10.55, and 10.15 m/s, respectively. After threshing, grains were divided into three types: undamaged, surface cracked, and shell damaged. The nutritional quality of the last two damaged grains decreased during the storage process. These results are of great significance for optimizing buckwheat threshing parameters, reducing buckwheat damage, and improving the economic performance of the buckwheat industry. Full article
(This article belongs to the Section Agricultural Biosystem and Biological Engineering)
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Figure 1

Figure 1
<p>Buckwheat grain: (<b>a</b>) front view and (<b>b</b>) left view. Note: <span class="html-italic">L</span> represents length, <span class="html-italic">W</span> represents width, and <span class="html-italic">T</span> represents thickness.</p>
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<p>Self-made digital inclinometer.</p>
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<p>Three-dimensional model: (<b>a</b>) buckwheat grain and (<b>b</b>) collision model.</p>
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<p>Finite element model: (<b>a</b>) front view and (<b>b</b>) vertical view.</p>
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<p>5TG-85 buckwheat thresher.</p>
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<p>Force–distance curve of buckwheat grain compression.</p>
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<p>Dynamic simulation results of grain collision: (<b>A</b>) stress nephogram, (<b>B</b>) changes in von Mises stress, and (<b>C</b>) changes in energy.</p>
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<p>Contour plot of maximum von Mises stress under different collision schemes: (<b>a</b>) grains with different moisture contents at a collision speed of 8 m/s and (<b>b</b>) grains with different collision velocities at a moisture content of 11.98%.</p>
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<p>Maximum von Mises stress variation curve under different collision schemes. Note: R<sup>2</sup> indicates the correlation coefficient between stress and velocity.</p>
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<p>Changes in broken rate under different linear velocities. Note: The letters indicate significant differences (<span class="html-italic">p</span> &lt; 0.05).</p>
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<p>Types of damage: (<b>a</b>) undamaged grain, (<b>b</b>) surface crack, and (<b>c</b>) shell damage.</p>
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<p>Differences in nutritional components content: (<b>a</b>) protein, (<b>b</b>) starch, (<b>c</b>) fat, (<b>d</b>) total phenols, and (<b>e</b>) total flavonoids. Note: The letters a, b, and c indicate significant differences (<span class="html-italic">p</span> &lt; 0.05).</p>
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