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Search Results (3,983)

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20 pages, 5610 KiB  
Article
Numerical Simulations of Thermodynamic Processes in the Chamber of a Liquid Piston Compressor for Hydrogen Applications
by Valerijs Bezrukovs, Vladislavs Bezrukovs, Marina Konuhova, Deniss Bezrukovs, Imants Kaldre and Anatoli I. Popov
Technologies 2024, 12(12), 266; https://doi.org/10.3390/technologies12120266 (registering DOI) - 18 Dec 2024
Abstract
This paper presents the results of numerical simulations examining the thermodynamic processes during hydraulic hydrogen compression, using COMSOL Multiphysics® 6.0. These simulations focus on the application of hydrogen compression systems, particularly in hydrogen refueling stations. The computational models employ the CFD and [...] Read more.
This paper presents the results of numerical simulations examining the thermodynamic processes during hydraulic hydrogen compression, using COMSOL Multiphysics® 6.0. These simulations focus on the application of hydrogen compression systems, particularly in hydrogen refueling stations. The computational models employ the CFD and heat transfer modules, along with deforming mesh technology, to simulate gas compression and heat transfer dynamics. The superposition method was applied to simplify the analysis of hydrogen and liquid piston interactions within a stainless-steel chamber, accounting for heat exchange between the hydrogen, the oil (working fluid), and the cylinder walls. The study investigates the effects of varying compression stroke durations and initial hydrogen pressures, providing detailed insights into temperature distributions and energy consumption under different conditions. The results reveal that the upper region of the chamber experiences significant heating, highlighting the need for efficient cooling systems. Additionally, the simulations show that longer compression strokes reduce the power requirement for the liquid pump, offering potential for optimizing system design and reducing equipment costs. This study offers crucial data for enhancing the efficiency of hydraulic hydrogen compression systems, paving the way for improved energy consumption and thermal management in high-pressure applications. Full article
(This article belongs to the Special Issue Technological Advances in Science, Medicine, and Engineering 2024)
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Figure 1
<p>Schematic diagram of the delivery, storage, and preparation of compressed high-pressure hydrogen for use at refueling stations.</p>
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<p>A model of a steel cylinder shaped chamber where hydrogen is compressed by the oil (working fluid) coming from the bottom in the direction of the arrow.</p>
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<p>Model of a stainless-steel cylinder chamber for hydrogen compression via fluid injection.</p>
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<p>Mesh cell distribution in the numerical model during the change in hydrogen volume within the compression chamber and the position of the liquid piston column as it moves upward at times 0, 10, and 20 s over a single stroke period.</p>
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<p>The structure of the mesh cells in the numerical model during hydrogen compression in the chamber to a compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0 for time intervals of (<b>a</b>) 0 s and (<b>b</b>) 20 s.</p>
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<p>Distribution of the temperature of hydrogen in the compression chamber during a single 20 s compression stroke: (<b>a</b>) the initial pressure 3.0 MPa, (<b>b</b>) the initial pressure 20.0 MPa.</p>
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<p>Temperature distribution in the compression chamber wall during a single 20 s compression stroke: (<b>a</b>) initial pressure of 3.0 MPa, and (<b>b</b>) initial pressure of 20.0 MPa.</p>
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<p>Average temperature increases in hydrogen ∆<span class="html-italic">T<sub>H</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0, 10.0, 15.0, and 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>Average temperature increases in oil ∆<span class="html-italic">T<sub>F</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0, 10.0, 15.0, and 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>Average temperature increases in the cylinder body ∆<span class="html-italic">T<sub>C</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0, 10.0, 15.0, and 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>Diagrams of thermal energy distribution <span class="html-italic">Q<sub>T</sub></span> between energies accumulated in hydrogen <span class="html-italic">Q<sub>H</sub></span>, oil <span class="html-italic">Q<sub>F</sub></span>, and compression cylinder body <span class="html-italic">Q<sub>C</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>Diagrams of thermal energy distribution <span class="html-italic">Q<sub>T</sub></span> between energies accumulated in hydrogen <span class="html-italic">Q<sub>H</sub></span>, oil <span class="html-italic">Q<sub>F</sub></span>, and compression cylinder body <span class="html-italic">Q<sub>C</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>Increase in overall system temperature ∆<span class="html-italic">T<sub>O</sub></span> for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span>, at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0, 10.0, 15.0, and 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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<p>The power <span class="html-italic">W</span> required for hydrogen compression for different durations of the compression stroke <span class="html-italic">t<sub>s</sub></span> at initial pressures <span class="html-italic">P</span><sub>1</sub> = 3.0, 10.0, 15.0, and 20.0 MPa and compression ratio <span class="html-italic">K<sub>c</sub></span> = 5.0.</p>
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20 pages, 20421 KiB  
Article
Structure Improvement of Two-Cylinder Engine Cooling Water Jacket Based on Flow Field Simulation
by Lei Yang, Guangtao Lu and Tao Wang
Sustainability 2024, 16(24), 11092; https://doi.org/10.3390/su162411092 (registering DOI) - 18 Dec 2024
Abstract
The flow and heat transfer of the coolant directly affect the cooling performance, thermal load, and emissions of gasoline engine. The accurate estimation of heat transfer and temperature distribution within engines is crucial for studying thermal stresses and calculating engine performance. This study [...] Read more.
The flow and heat transfer of the coolant directly affect the cooling performance, thermal load, and emissions of gasoline engine. The accurate estimation of heat transfer and temperature distribution within engines is crucial for studying thermal stresses and calculating engine performance. This study focuses on the design of a new cooling water jacket structure for a two-cylinder gasoline engine. In the novel structure, the coolant flows from the cylinder block to the cylinder head and then returns to the cylinder block, providing better cooling for the cylinder head. The three-dimensional simulation results show that the overall flow velocity of this structure ranges between 0.1 m/s and 3 m/s, which meets the design requirement of 0.1 m/s to 5 m/s. However, there are still some flow dead zones in this structure, which may lead to insufficient heat transfer. Therefore, the water jacket structure is further optimized. After optimization, the pressure drop between the inlet and outlet is decreased, and the velocity distribution becomes more rational. Both the flow velocity and the heat transfer coefficient meet the design targets. These results can provide theoretical guidance for the structural improvement of the water jacket and approaches to studying the flow characteristics of the coolants. Full article
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<p>Schematic diagram of different cooling structures.</p>
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<p>Structure of WJ.</p>
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<p>The coolant flow direction of the cooling WJ (The arrows represent the flow direction).</p>
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<p>Material properties of coolant. (<b>a</b>) Variation in coolant density with temperature; (<b>b</b>) variation in coolant viscosity with temperature; (<b>c</b>) variation in coolant thermal conductivity with temperature; (<b>d</b>) variation in coolant-specific heat with temperature.</p>
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<p>Grid model of WJ.</p>
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<p>Grid independent result.</p>
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<p>Pressure distribution of WJ.</p>
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<p>Flow velocity of WJ. (<b>a</b>) Cylinder block; (<b>b</b>) cylinder block; (<b>c</b>) lower cylinder head; (<b>d</b>) upper cylinder head; (<b>e</b>) flange region.</p>
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<p>HTC levels of WJ. (<b>a</b>) Cylinder block; (<b>b</b>) cylinder block; (<b>c</b>) lower cylinder head; (<b>d</b>) upper cylinder head; (<b>e</b>) flange region.</p>
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<p>The design modifications of the cylinder block.</p>
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<p>Prototype engine (Red arrow pointing to the V-drilling).</p>
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<p>The design modifications of the lower cylinder head.</p>
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<p>The design modifications of the upper cylinder head.</p>
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<p>The coolant flow direction of the cooling WJ (V2) (Arrow represents the flow direction).</p>
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<p>Pressure distribution of WJ.</p>
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<p>Flow velocity of WJ (V1 vs. V2).</p>
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<p>The flow velocity of the critical areas.</p>
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<p>HTC levels of WJ (V1 vs. V2).</p>
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<p>HTC levels of key areas.</p>
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<p>Photograph of engine bench test. (<b>a</b>) Intake side of engine; (<b>b</b>) exhaust side of engine.</p>
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<p>The schematic diagram of the experimental setup for the WJ study.</p>
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22 pages, 7029 KiB  
Article
A Hybrid Model for Freight Train Air Brake Condition Monitoring
by Alessandro Galimberti, Federico Zanelli and Gisella Tomasini
Appl. Sci. 2024, 14(24), 11770; https://doi.org/10.3390/app142411770 - 17 Dec 2024
Viewed by 227
Abstract
The Digital Freight Train is expected to revolutionise the rail freight industry. A critical aspect of this transformation is real-time condition monitoring of air brake systems, which are among the leading causes of train malfunctions. To achieve this goal, advanced algorithms for air [...] Read more.
The Digital Freight Train is expected to revolutionise the rail freight industry. A critical aspect of this transformation is real-time condition monitoring of air brake systems, which are among the leading causes of train malfunctions. To achieve this goal, advanced algorithms for air brake modelling are required. This paper introduces a computationally efficient air brake model tailored for real-time diagnostic applications. A hybrid approach, integrating both empirical data and simplified fluid-dynamic equations, has been adopted. Compared to other air brake models found in the literature, the innovative contributions of the presented model are the reduction of the number of required parameters and the estimation of the brake cylinder pressure directly from the main brake pipe pressure using a feed-forward approach. Moreover, a new approach in the evaluation of the first braking phase and the brake cylinder pressure build-up as the saturation of the brake mode is presented. The model input includes the main brake pipe pressure, the weighing valve pressure, and the brake mode, and the output includes the pressure at the brake cylinder. The air brake model has been validated using data from a previous experimental campaign. The model’s accuracy in replicating the air brake system mechanism makes it well-suited for future development of model-based algorithms designed for air brake fault detection. Full article
(This article belongs to the Section Mechanical Engineering)
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<p>Graphical abstract of the methodological approach adopted.</p>
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<p>T3000e wagon air brake plant scheme.</p>
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<p>Air brake system model flow chart overview.</p>
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<p>Time histories of (<b>a</b>) the main brake pipe peak detection algorithm and (<b>b</b>) the main brake pipe partition.</p>
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<p>Time histories of (<b>a</b>) main brake pipe pressure, (<b>b</b>) filtered distributor pressure, (<b>c</b>) Filtered distributor pressure time derivative and (<b>d</b>) main brake pipe pressure phase partition and classification.</p>
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<p>Simplified scheme of the air brake system.</p>
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<p>Schematic overview of (<b>a</b>) the distributor and (<b>b</b>) a free body diagram of the forces acting on the piston-valve assembly of the distributor.</p>
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<p>Comparison between the main brake pipe pressure and the distributor pressure.</p>
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<p>Transfer function of (<b>a</b>) wagon weight distribution and (<b>b</b>) the weighing valve.</p>
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<p>Schematic overview of (<b>a</b>) first braking phase activation and (<b>b</b>) first braking phase de-activation.</p>
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<p>First braking phase peak detection.</p>
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<p>First braking phase model.</p>
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<p>Simplified scheme of the kink valve.</p>
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<p>Kink valve transfer function of (<b>a</b>) the braking phase and (<b>b</b>) the releasing phase.</p>
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<p>Simplified scheme of the relay valve.</p>
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<p>Alimentation valve opening model for braking phase.</p>
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<p>Comparison between the model and the experimental brake cylinder pressure with input parameters from (<b>a</b>) Dataset 1, (<b>b</b>) Dataset 2 and (<b>c</b>) Dataset 3.</p>
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<p>Comparison between the model and the experimental brake cylinder pressure with input parameters from (<b>a</b>) Dataset 4, (<b>b</b>) Dataset 5 and (<b>c</b>) Dataset 6.</p>
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<p>Relative error comparison between the model and the experimental brake cylinder pressure (<b>a</b>) for each Dataset at different phases and (<b>b</b>) for all Datasets at different phases.</p>
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<p>Comparison between the braking time calculated in [<a href="#B27-applsci-14-11770" class="html-bibr">27</a>] and the braking time coming from the model.</p>
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20 pages, 18907 KiB  
Article
From Experimentation to Optimization: Surface Micro-Texturing for Low-Friction and Durable PTFE–Steel Interfaces Under Full Film Lubrication
by Risheng Long, Jincheng Hou, Yimin Zhang, Qingyu Shang, Chi Ma, Florian Pape and Max Marian
Polymers 2024, 16(24), 3505; https://doi.org/10.3390/polym16243505 - 17 Dec 2024
Viewed by 340
Abstract
To enhance the sliding tribological performance between PTFE and 40#steel (AISI 1040) under full film lubrication conditions, laser surface texturing (LST) technology was employed to prepare micro-dimples on the contact surfaces of 40# steel discs. The Box–Behnken design response surface methodology (BBD-RSM) was [...] Read more.
To enhance the sliding tribological performance between PTFE and 40#steel (AISI 1040) under full film lubrication conditions, laser surface texturing (LST) technology was employed to prepare micro-dimples on the contact surfaces of 40# steel discs. The Box–Behnken design response surface methodology (BBD-RSM) was applied to optimize the micro-dimple parameters. Coefficients of friction (COFs), wear losses and worn contact surfaces of the PTFE–40# steel tribo-pairs were researched through repeated wear tests, as lubricated with sufficient anti-wear hydraulic oil. The influencing mechanism of micro-dimples on the tribological behavior of tribo-pairs was also discussed. The results proved that micro-dimples can significantly improve the tribological properties of PTFE–40#steel tribo-pairs. The deviation between the final obtained average COF and the prediction by the BBD-RSM regression model was only 0.0023. Following optimization, the average COF of the PTFE–40# steel tribo-pair was reduced by 39.34% compared to the smooth reference. The wear losses of the PTFE ring and 40# steel disc decreased by 91.8% and 30.3%, respectively. This study would offer a valuable reference for the optimal design of key seals used in hydraulic cylinders. Full article
(This article belongs to the Section Polymer Applications)
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Figure 1
<p>PTFE–40# steel tribo-pair and laser marking system. (<b>a</b>) Photos of the steel disc and upper counter rings (PTFE); (<b>b</b>) Section view of the lower sample (40# steel disc); (<b>c</b>) Photo of laser marking machine; (<b>d</b>) Section view of the upper sample (PTFE ring); (<b>e</b>) Textured surface of the 40#steel disc before re-polishing and the angle between two adjacent sets of micro-dimples in circumference.</p>
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<p>Vertical universal tribological test rig. (<b>a</b>) Photo of the MMW-1A vertical universal tribo-meter; (<b>b</b>) Photo of the fixtures used; (<b>c</b>) Section view of the fixtures: ① upper fixture; ② upper sample (PTFE ring); ③ lower sample (40# steel disc); ④ oil deflector; ⑤ lower fixture; ⑥ loading flange.</p>
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<p>COF data of different groups as the PTFE rings were tested against the 40# steel discs: (<b>a</b>) COF curves of T1–T4; (<b>b</b>) COF curves of R1–R4; (<b>c</b>) COF curves of X1–X4; (<b>d</b>) COF curves of X5-1 to X5-5; (<b>e</b>) Average COFs of 17 groups.</p>
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<p>Representative worn surfaces of the PTFE rings and wear losses of different groups after wear tests. (<b>a</b>) Worn surfaces of the PTFE rings after ultrasonic cleaning. (<b>b</b>) Mass losses of the PTFE rings and 40# steel discs: (<b>b1</b>) mass losses of T1–T4; (<b>b2</b>) mass losses of R1–R4; (<b>b3</b>) mass losses of X1–X4; (<b>b4</b>) mass losses of X5-1–X5-5.</p>
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<p>Representative worn surfaces of the 40# steel discs of different groups after wear tests and the FTIR curve of the PTFE transfer film. (<b>a</b>) Worn surfaces of the 40# steel discs after ultrasonic cleaning. (<b>b</b>) Typical infrared spectral characteristics of the PTFE debris collected from the transfer film on the contact surface of the 40# steel disc. (<b>c</b>) Section view of one black spot on the worn surface of the steel disc of the CT group.</p>
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<p>Representative 3D worn morphologies (with an enlargement of 2000% in the height direction) of the PTFE–40# steel tribo-pairs (T1, T3, T4, R1, X3, X5-4) after ultrasonic cleaning. (<b>a</b>) PTFE rings; (<b>b</b>) 40# steel discs.</p>
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<p>Response surfaces of the interaction among three factors (<span class="html-italic">D</span>, <span class="html-italic">P</span>, <span class="html-italic">H</span>) on the average COFs of the PTFE–40# steel tribo-pairs. (<b>a</b>) Response surface among average COF, <span class="html-italic">P</span> and <span class="html-italic">H</span>; (<b>b</b>) Response surface among average COF, <span class="html-italic">D</span> and <span class="html-italic">P</span>; (<b>c</b>) Response surface among average COF, <span class="html-italic">D</span> and <span class="html-italic">H</span>.</p>
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<p>COF curves and wear losses of three groups (OT, LT and CT). (<b>a</b>) COF curves and average COF lines of OT, LT and CT; (<b>b</b>) Wear losses of OT, LT and CT.</p>
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<p>Representative worn surfaces and 3D morphologies of the PTFE rings of OT, LT and CT after ultrasonic cleaning. (<b>a</b>) OT; (<b>b</b>) LT; (<b>c</b>) CT.</p>
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<p>Representative worn surfaces and 3D morphologies of the 40# steel discs of OT, LT and CT after ultrasonic cleaning. (<b>a</b>) OT; (<b>b</b>) LT; (<b>c</b>) CT.</p>
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<p>Influence mechanism of micro-dimples on the tribological performance of the PTFE–40# steel tribo-pair as lubricated with sufficient anti-wear hydraulic oil. (<b>a</b>) PTFE–40# steel tribo-pair and transfer film: (<b>a1</b>) section view of PTFE–40# steel tribo-pair; (<b>a2</b>) top view of PTFE–40# steel tribo-pair; (<b>a3</b>) transfer film left on the surface. (<b>b</b>) Micro-eddies in micro-dimples and the debris migration: (<b>b1</b>) influence of micro-eddies on the load-carrying capacity along the circumference; (<b>b2</b>) migration of wear debris along the radius direction. (<b>c</b>) Cavitation phenomenon and its formation mechanism: (<b>c1</b>) image of black spots; (<b>c2</b>) formation mechanism of cavitation.</p>
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16 pages, 2594 KiB  
Article
Mitigating Mode Switching Oscillation in a One-Motor-One-Pump Motor-Controlled Hydraulic Cylinder via System Pressure Control: Simulation Study
by Wei Zhao, Morten Kjeld Ebbesen, Michael Rygaard Hansen and Torben Ole Andersen
Energies 2024, 17(24), 6334; https://doi.org/10.3390/en17246334 - 16 Dec 2024
Viewed by 300
Abstract
This study focuses on a hydraulic cylinder that is directly connected to a fixed-displacement hydraulic pump driven by an electric servo motor. This particular setup is referred to as a one-motor-one-pump motor-controlled hydraulic cylinder (MCC). This paper presents a new approach to address [...] Read more.
This study focuses on a hydraulic cylinder that is directly connected to a fixed-displacement hydraulic pump driven by an electric servo motor. This particular setup is referred to as a one-motor-one-pump motor-controlled hydraulic cylinder (MCC). This paper presents a new approach to address mode switching oscillation (MSO) in MCCs by incorporating system pressure control capabilities. It conducts a detailed investigation into the factors that contribute to MSO in standard MCCs and thoroughly evaluates the effectiveness of the proposed system in mitigating MSO. The simulation results demonstrate the successful suppression of MSO. In conclusion, the proposed MCC with system pressure control capabilities is validated and, furthermore, it shows great potential for practical applications involving small loads and rapid retraction. Full article
(This article belongs to the Section F: Electrical Engineering)
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Figure 1
<p>Structure of a one-motor-one-pump motor-controlled cylinder (MCC) [<a href="#B1-energies-17-06334" class="html-bibr">1</a>].</p>
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<p>A standard MCC with two POCVs.</p>
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<p>Four-quadrant operations of the cylinder and the MCC drive unit.</p>
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<p>The proposed MCC [<a href="#B1-energies-17-06334" class="html-bibr">1</a>].</p>
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<p>Demonstration of four-quadrant operation in operation mode [<a href="#B1-energies-17-06334" class="html-bibr">1</a>].</p>
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<p>Sketch of the laboratory single-boom crane [<a href="#B1-energies-17-06334" class="html-bibr">1</a>].</p>
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<p>Block diagram of the control algorithm [<a href="#B1-energies-17-06334" class="html-bibr">1</a>].</p>
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<p>Simulation results for the standard MCC in MSO.</p>
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<p>Simulation results for the proposed MCC mitigating MSO.</p>
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16 pages, 4375 KiB  
Article
Investigation of Surface Hardness and Microstructural Changes in S45C Carbon Steel Cylinders Through Arc Quenching
by Pham Son Minh, Van-Thuc Nguyen, Thanh Tan Nguyen and Nguyen Ho
Metals 2024, 14(12), 1438; https://doi.org/10.3390/met14121438 - 16 Dec 2024
Viewed by 316
Abstract
Arc quenching has many advantages, including generating large amounts of heat in a short time, a self-quenching ability, and simple equipment. The electric arc energy from a TIG welding machine was used to modify the surface properties of S45C Carbon Steel Cylinders. The [...] Read more.
Arc quenching has many advantages, including generating large amounts of heat in a short time, a self-quenching ability, and simple equipment. The electric arc energy from a TIG welding machine was used to modify the surface properties of S45C Carbon Steel Cylinders. The study focuses on the impact of arc length, current intensity, travel speed, gas flow rate, heating angle, and pulse on surface hardness after arc quenching an S45C steel tube with a cylinder surface. The study found that the hardness reduces from 45.1 HRC to 41.2 HRC as the current intensity increases from 125 A to 140 A. According to Taguchi’s results, the ranking of factors which have the greatest impact on surface hardness are pulse time, travel speed, intensity, gas flow rate, arc length, and heating angle. The pulse time has the highest impact because it directly influences the heating input, followed by the travel speed. Arc length and heating angle, on the other hand, have the least effect. The base metal, heat-affected area, and hardened area are the three distinct areas that make up the microstructure structure. After the arc quenching process, the case hardening depth is represented by the heat-affected zone at 1536 μm. A highly colored residual austenite and a needle-shaped martensite phase make up the hardened region. The hardened region is 1200 μm thick and has a hardness of more than 300 HV0.3. The study’s findings may improve the application and understanding of the arc quenching treatment procedure in the industrial sector. Full article
(This article belongs to the Section Metal Casting, Forming and Heat Treatment)
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<p>Schematic illustration of a double-ellipsoidal heat source.</p>
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<p>S45C steel tube sample and arc equipment: (<b>a</b>,<b>b</b>) arc quenching equipment, and (<b>c</b>) S45C steel tube after the quenching using the arc energy of the TIG gun corresponding to 25 cases designed by the Taguchi method.</p>
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<p>Influences of current intensity on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of arc length on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of shielding gas flow rate on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of travel speed on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of pulse time on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of heating angle on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Influences of water cooling angle on the cylinder surface hardness of S45C steel tube after arc quenching.</p>
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<p>Main influences plot for SN ratios of the S45C steel tube hardness with cylinder surface (larger is better).</p>
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<p>Microstructure of hardened S45 steel tube of sample No. 6: (<b>a</b>) cross-section of the sample at 50× magnification, (<b>b</b>) boundary of the cross-section of the sample at 500× magnification, (<b>c</b>) base metal, (<b>d</b>) hardened zone, and (<b>e</b>) cross-section of the sample at 3000× magnification.</p>
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<p>Distribution of microhardness in the cross-section of S45C steel tubes of sample No.6.</p>
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16 pages, 5803 KiB  
Article
3D-Printed Self-Assembling Helical Models for Exploring Viral Capsid Structures
by Donald Plante, Keegan Unzen and John R. Jungck
Biomimetics 2024, 9(12), 763; https://doi.org/10.3390/biomimetics9120763 - 16 Dec 2024
Viewed by 282
Abstract
This work presents a novel application of additive manufacturing in the design of self-assembling helical viral capsids using 3D-printed components. Expanding on prior work with 3D-printed self-assembling spherical capsids, we developed helical models that integrate geometric parameters and magnetic interactions to mimic key [...] Read more.
This work presents a novel application of additive manufacturing in the design of self-assembling helical viral capsids using 3D-printed components. Expanding on prior work with 3D-printed self-assembling spherical capsids, we developed helical models that integrate geometric parameters and magnetic interactions to mimic key features of the assembly process of helical viral capsids. Using dual-helix phyllotactic patterns and simplified electrostatic simulations, these models consistently self-assemble into a cylinder, providing unique insights into the structural organization and stability of helical capsids. This accessible 3D-printed approach demonstrates the potential of additive manufacturing for research in mesoscale self-assembling models and in the education of complex biological assembly processes, promoting hands-on exploration of viral architecture and self-assembly mechanisms. Full article
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Graphical abstract

Graphical abstract
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<p>Helix and helical net diagram: (<b>a</b>) the helix, as defined by Equation (1), with parameter <math display="inline"><semantics> <mrow> <mi>t</mi> </mrow> </semantics></math> varying from <math display="inline"><semantics> <mrow> <mn>0</mn> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mn>4</mn> <mi>π</mi> </mrow> </semantics></math>; (<b>b</b>) helical net diagram showing the helical angle, <math display="inline"><semantics> <mrow> <mi>θ</mi> </mrow> </semantics></math>, where the x-axis is the unwrapped circumference of the helix. The vertical distance between successive layers corresponds to the pitch, <math display="inline"><semantics> <mrow> <mi>p</mi> </mrow> </semantics></math>.</p>
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<p>Capsomere and assembled helical tube: (<b>a</b>) fully assembled self-assembling helical tube composed of 50 3D-printed capsomeres; (<b>b</b>) three-dimensional rendering of an individual capsomere, highlighting the interlocking trapezoidal prongs and lock mechanism.</p>
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<p>Helical organization in Tobacco Mosaic Virus (TMV). The image highlights left-handed (red curve) and right-handed (blue curve) helices. To aid in visualization the left-handed helices are depicted throughout in blue and purple. The image has been adapted under a Creative Commons license from the Protein Data Bank’s Molecule of the Month (<a href="https://pdb101.rcsb.org/motm/109" target="_blank">https://pdb101.rcsb.org/motm/109</a> (accessed on 5 December 2024)).</p>
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<p>Dual-spiral phyllotactic helical model: (<b>a</b>) planar projection of an infinite cylinder with left- and right-handed spiral wrappings with a 2,3 phyllotaxis. The three left-handed helices are represented by the red lines: solid, short-dashed, and long-dashed, while the two right-handed helices are represented by the blue lines: sold and short-dashed; (<b>b</b>) self-assembled helical model demonstrating the 2,3 phyllotaxis, where the red and blue lines shown in (<b>a</b>) are represented as solid lines on the model.</p>
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<p>Charge distribution and magnet orientation in capsomeres: (<b>a</b>) charged residues on TMV capsomeres, with positive arginine (blue) and negative aspartic acid (red) residues; (<b>b</b>) interior of our 3D-printed capsomere model showing magnets aligned to mimic the TMV charge pattern, with north (negative, red) and south (positive, blue) poles.</p>
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<p>Cylindrical tumbler. Our cylindrical tumbler designed to facilitate random tumbling and self-assembly of capsomeres.</p>
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<p>Capsomere design process: (<b>a</b>) five intersecting helical paths; (<b>b</b>) rectangles swept along paths to form 3D bodies; (<b>c</b>) subtraction of helical bodies from cylinder; (<b>d</b>) resulting parallelogram-shaped capsomere pieces following a dual-spiral pattern.</p>
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<p>Magnet orientation tools. Custom, color-coded tools to ensure consistent north–south polarity during magnet installation.</p>
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<p>Time versus assembly groups for single-helix model: (<b>a</b>) assembly with tumbler at 17.7 RPM; (<b>b</b>) assembly with tumbler at 33.2 RPM.</p>
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<p>Time versus assembly groups for dual-helix model: (<b>a</b>) assembly with tumbler at 17.7 RPM; (<b>b</b>) assembly with tumbler at 33.2 RPM.</p>
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<p>Drop height versus disassembly groups for single- and dual-helix models: (<b>a</b>) single-helix model; (<b>b</b>) dual-helix model.</p>
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16 pages, 3434 KiB  
Article
Structural Concrete from 100% Recycled Aggregates
by Antonio Brencich, Andrea Dubesti and Farhad Ali Akbari Hamed
Appl. Sci. 2024, 14(24), 11709; https://doi.org/10.3390/app142411709 - 16 Dec 2024
Viewed by 337
Abstract
In spite of the amount of construction debris produced every year, recycled aggregates are still not commonly used in the concrete industry. A 100% recycled aggregate concrete—RAC—is not yet allowed by technical codes even though it would greatly help reduce the disposal of [...] Read more.
In spite of the amount of construction debris produced every year, recycled aggregates are still not commonly used in the concrete industry. A 100% recycled aggregate concrete—RAC—is not yet allowed by technical codes even though it would greatly help reduce the disposal of debris. This paper considers a construction site that can only be reached by small trucks, where concrete production is performed using manual procedures and the transportation of building materials is difficult and expensive. The aim of this research is to establish a mix design for 100% RAC for structural applications. In this context, recycled aggregates are obtained from the debris crushed by a small portable crusher Crunchy©. Based on a series of tests on concrete cubes and cylinders of aggregates originating from different types of debris, it is shown that 100% RAC is also a promising material for structural applications. At the cost of more cement in comparison to standard concrete, RAC from high-strength aggregates (concrete and gres-porcelain tiles) may be used in r.c. structures. Some of its features, such as its low pH value and low compressive strength in the case of clay-originated aggregates, still need to be studied for an optimized mix design. In addition, it is shown that RACs have approximately the same carbon footprint as standard concrete. Full article
(This article belongs to the Section Civil Engineering)
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<p>Crunchy<sup>®</sup> crusher (<b>left</b>) and jaw crunching system (<b>right</b>).</p>
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<p>Granulometric curve for concrete. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for concrete roof tiles. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for clay roof tiles. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for gres-porcelain tiles. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for mixed tiles. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for mixed debris. Dashed curves: +5% and −5% curves.</p>
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<p>Granulometric curve for mixed 50% concrete + 50% mixed debris. Dashed curves: +5% and −5% curves.</p>
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<p>Recycled aggregates from concrete—strength vs. time.</p>
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<p>Recycled aggregates from mixed debris—strength vs. time.</p>
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<p>Recycled aggregates from mixed tiles—strength vs. time.</p>
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<p>Recycled aggregates from 50% concrete + 50% mixed debris—strength vs. time.</p>
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20 pages, 5882 KiB  
Article
Contact Parameter Calibration for Discrete Element Potato Minituber Seed Simulation
by Kai Chen, Xiang Yin, Wenpeng Ma, Chengqian Jin and Yangyang Liao
Agriculture 2024, 14(12), 2298; https://doi.org/10.3390/agriculture14122298 - 14 Dec 2024
Viewed by 509
Abstract
The discrete element method (DEM) has been widely applied as a vital auxiliary technique in the design and optimization processes of agricultural equipment, especially for simulating the behavior of granular materials. In this study, the focus is placed on accurately calibrating the simulation [...] Read more.
The discrete element method (DEM) has been widely applied as a vital auxiliary technique in the design and optimization processes of agricultural equipment, especially for simulating the behavior of granular materials. In this study, the focus is placed on accurately calibrating the simulation contact parameters necessary for the V7 potato minituber seed DEM simulation. Firstly, three mechanical tests are conducted, and through a combination of actual tests and simulation tests, the collision recovery coefficient between the seed and rubber material is determined to be 0.469, the static friction coefficient is 0.474, and the rolling friction coefficient is 0.0062. Subsequently, two repose angle tests are carried out by employing the box side plates lifting method and the cylinder lifting method. With the application of the response surface method and a search algorithm based on Matlab 2019, the optimal combination of seed-to-seed contact parameters, namely, the collision recovery coefficient, static friction coefficient, and rolling friction coefficient, is obtained, which are 0.500, 0.476, and 0.043, respectively. Finally, the calibration results are verified by a seed-falling device that combines collisions and accumulation, and it is shown that the relative error between the simulation result and the actual result in the verification test is small. Thus, the calibration results can provide assistance for the design and optimization of the potato minituber seed planter. Full article
(This article belongs to the Section Agricultural Technology)
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<p>Potato minituber seed triaxial size.</p>
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<p>Miniature potato compression test.</p>
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<p>Potato minituber seed simulation model. (<b>a</b>) ellipsoidal model, (<b>b</b>) spherical model.</p>
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<p>Potato minituber seed—rubber plate free fall test. (<b>a</b>) actual test, (<b>b</b>) simulation test.</p>
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<p>Collision recovery coefficient fits the curve.</p>
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<p>Slope sliding test. (<b>a</b>) actual test, (<b>b</b>) simulation test.</p>
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<p>Static friction coefficient fitting curve.</p>
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<p>Inclined plane rolling test. (<b>a</b>) actual test, (<b>b</b>) simulation test.</p>
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<p>Rolling friction coefficient fitting curve.</p>
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<p>Repose angle test device. (<b>a</b>) box side plates lifting method, (<b>b</b>) cylinder lifting method.</p>
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<p>Simulation test of box side plates lifting method. (<b>a</b>) initial state, (<b>b</b>) side plates lifting, (<b>c</b>) test completed.</p>
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<p>Simulation test of cylinder lifting method. (<b>a</b>) initial state, (<b>b</b>) cylinder lifting, (<b>c</b>) test completed.</p>
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<p>Repose angle image processing and angle acquisition. (<b>a</b>) initial image, (<b>b</b>) binarization, (<b>c</b>) boundary extraction, (<b>d</b>) linear fitting.</p>
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<p>3D response surface diagram of interaction term BC. (<b>a</b>) interaction terms AB, (<b>b</b>) interaction terms AC, (<b>c</b>) interaction terms BC.</p>
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<p>Test verification device physical drawing.</p>
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<p>Simulation seed drop test. (<b>a</b>) seeds began to pile up, (<b>b</b>) seed pile is almost complete.</p>
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21 pages, 6018 KiB  
Article
Optimization of the Filament Winding Process for Glass Fiber-Reinforced PPS and PP Composites Using Box–Behnken Design
by Sevinc Orman, Mustafa Dogu and Belma Ozbek
Polymers 2024, 16(24), 3488; https://doi.org/10.3390/polym16243488 - 14 Dec 2024
Viewed by 380
Abstract
Filament winding is a widely used out-of-autoclave manufacturing technique for producing continuous fiber-reinforced thermoplastic composites. This study focuses on optimizing key filament winding process parameters, including heater temperature, roller pressure, and winding speed, to produce thermoplastic composites. Using Box–Behnken response surface methodology (RSM), [...] Read more.
Filament winding is a widely used out-of-autoclave manufacturing technique for producing continuous fiber-reinforced thermoplastic composites. This study focuses on optimizing key filament winding process parameters, including heater temperature, roller pressure, and winding speed, to produce thermoplastic composites. Using Box–Behnken response surface methodology (RSM), the study investigates the effects of these parameters on the compressive load of glass fiber-reinforced polypropylene (GF/PP) and polyphenylene sulfide (GF/PPS) composite cylinders. Mathematical models were developed to quantify the impact of each parameter and optimal processing conditions were identified across a wide temperature range, enhancing both manufacturing efficiency and the overall quality of the composites. This study demonstrates the potential of thermoplastic filament winding as a cost-effective and time-efficient alternative to conventional methods, addressing the growing demand for lightweight, high-performance, out-of-autoclave composites in industries such as aerospace, automotive, and energy. The optimized process significantly improved the performance and reliability of filament winding for various thermoplastic applications, offering potential benefits for industrial, aerospace, and other advanced sectors. The results indicate that GF/PPS composites achieved a compressive load of 3356.99 N, whereas GF/PP composites reached 2946.04 N under optimized conditions. It was also revealed that operating at elevated temperatures and reduced pressure levels enhances the quality of GF/PPS composites, while for GF/PP composites, maintaining lower temperature and pressure values is crucial for maximizing strength. Full article
(This article belongs to the Section Polymer Composites and Nanocomposites)
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<p>A schematic illustration of the thermoplastic filament winding system used in the present study.</p>
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<p>An illustration of the winding pattern created in CADWIND<sup>®</sup>.</p>
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<p>Filament winding system.</p>
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<p>Filament-wound composites.</p>
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<p>Flowchart of the experimental methodology.</p>
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<p>Compression test setup.</p>
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<p>Composite structure and test sampling.</p>
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<p>Predicted vs. actual compressive load of GF/PPS and GF/PP composites.</p>
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<p>The effects of (<b>a</b>) pressure and temperature, (<b>b</b>) winding speed and temperature, and (<b>c</b>) pressure and winding speed on the compressive load of GF/PPS composites produced by filament winding.</p>
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<p>The effects of (<b>a</b>) pressure and temperature, (<b>b</b>) winding speed and temperature, and (<b>c</b>) pressure and winding speed on the compressive load of GF/PPS composites produced by filament winding.</p>
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<p>The effects of (<b>a</b>) pressure and temperature, (<b>b</b>) winding speed and temperature, and (<b>c</b>) pressure and winding speed on the compressive load of GF/PP composites produced by filament winding.</p>
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<p>The effects of (<b>a</b>) pressure and temperature, (<b>b</b>) winding speed and temperature, and (<b>c</b>) pressure and winding speed on the compressive load of GF/PP composites produced by filament winding.</p>
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19 pages, 15008 KiB  
Article
Transversal Vortex-Induced Vibration of a Circular Cylinder in Tandem with a Stationary Square Structure
by Henry Francis Annapeh and Victoria Kurushina
Appl. Mech. 2024, 5(4), 978-996; https://doi.org/10.3390/applmech5040054 - 12 Dec 2024
Viewed by 474
Abstract
This paper considers a system with two offshore structures in tandem, where the upstream square structure is fixed and the downstream circular structure has one degree of freedom. Cylinders are subject to uniform and linearly sheared flow conditions. The dynamics of the downstream [...] Read more.
This paper considers a system with two offshore structures in tandem, where the upstream square structure is fixed and the downstream circular structure has one degree of freedom. Cylinders are subject to uniform and linearly sheared flow conditions. The dynamics of the downstream structure are investigated by using a computational fluid dynamics approach for a Reynolds number range of 1000–6500 at the centerline. The spacing ratio for the tandem structures is L/D = 6 in this work, corresponding to the wake interference regime. The effect of the shear parameter on the development of vortex-induced vibrations in the lock-in state within the downstream structure is studied, in comparison with the lock-in of an isolated circular structure. The results of this research include statistics on the displacement amplitude, drag and lift coefficients, frequency ratio, time histories and contours of vorticity. The results obtained show the maximum displacement amplitude of the isolated structure in a uniform flow at the level of 0.8 diameters during the upper branch. The investigation also shows a later development in the maximum displacement during the upper branch of the downstream structure under shear flow conditions, with the highest maximum displacement of 1.18 diameters seen for the shear parameter of 0.05. Full article
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<p>A schematic of the considered structures in the computational domain.</p>
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<p>Selected mesh around the isolated circular structure.</p>
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<p>The selected mesh for the area around the tandem structures.</p>
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<p>Maximum displacement amplitude vs. reduced velocity.</p>
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<p>Mean drag coefficient vs. reduced velocity.</p>
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<p>RMS of lift coefficient vs. Reynolds number.</p>
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<p>Vibration frequency ratio vs. reduced velocity.</p>
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<p>Displacement time history at reduced velocity of 2 for (<b>a</b>) single cylinder at <span class="html-italic">K</span> = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05 and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>Displacement time history at reduced velocity of 6 for (<b>a</b>) single cylinder at <span class="html-italic">K</span> = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05 and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>Displacement time history at reduced velocity of 10 for (<b>a</b>) single cylinder at <span class="html-italic">K</span> = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05, and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>The vorticity contour for the downstream cylinder at the reduced velocity of 6 and <span class="html-italic">K</span> = 0.0 for specific times within the flow: (i) t = 20.89 s, (ii) t = 20.95 s, (iii) t = 21.06 s and (iv) t = 21.13 s.</p>
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<p>The vorticity contour for the downstream cylinder at the reduced velocity of 6 and <span class="html-italic">K</span> = 0.05 for specific times within the flow: (i) t = 8.385 s, (ii) t = 8.445 s, (iii) t = 8.56 s and (iv) t = 8.625 s.</p>
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<p>Lift coefficient time history at reduced velocity of 2 for (<b>a</b>) single cylinder at = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05 and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>The power spectrum density (PSD) diagrams for the displacement time history at a different <span class="html-italic">K</span> and the reduced velocity of 2 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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<p>The power spectrum density (PSD) for the lift coefficient at a different <span class="html-italic">K</span> and the reduced velocity of 2 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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<p>Lift coefficient time history at reduced velocity of 6 for (<b>a</b>) single cylinder at = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05 and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>The power spectrum density (PSD) diagrams for the displacement time history at a different <span class="html-italic">K</span> and the reduced velocity of 6 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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<p>The power spectrum density (PSD) diagrams for the lift coefficient at a different <span class="html-italic">K</span> and the reduced velocity of 6 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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<p>Lift coefficient time history at reduced velocity of 10 for (<b>a</b>) single cylinder at = 0.0, (<b>b</b>) single cylinder at <span class="html-italic">K</span> = 0.05, (<b>c</b>) single cylinder at <span class="html-italic">K</span> = 0.07, (<b>d</b>) DC at <span class="html-italic">K</span> = 0.0, (<b>e</b>) DC at <span class="html-italic">K</span> = 0.05 and (<b>f</b>) DC at <span class="html-italic">K</span> = 0.07.</p>
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<p>The power spectrum density (PSD) diagrams for the displacement time history at a different <span class="html-italic">K</span> and the reduced velocity of 10 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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<p>The power spectrum density (PSD) for the lift coefficient at a different <span class="html-italic">K</span> and the reduced velocity of 10 for (<b>a</b>) the single cylinder and (<b>b</b>) the DC.</p>
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23 pages, 472 KiB  
Review
Exploring the Effects of Synergistic Combustion of Alcohols and Biodiesel on Combustion Performance and Emissions of Diesel Engines: A Review
by Fangyuan Zheng and Haeng Muk Cho
Energies 2024, 17(24), 6274; https://doi.org/10.3390/en17246274 (registering DOI) - 12 Dec 2024
Viewed by 400
Abstract
Diesel engines are extensively employed in transportation, agriculture, and industry due to their high thermal efficiency and fuel economy. However, the combustion of conventional diesel fuel is accompanied by substantial emissions of pollutants, including carbon monoxide (CO), hydrocarbons (HC), nitrogen oxides (NOx [...] Read more.
Diesel engines are extensively employed in transportation, agriculture, and industry due to their high thermal efficiency and fuel economy. However, the combustion of conventional diesel fuel is accompanied by substantial emissions of pollutants, including carbon monoxide (CO), hydrocarbons (HC), nitrogen oxides (NOx), and carbon dioxide (CO2), posing significant threats to environmental quality. Biodiesel, as a renewable and cleaner alternative fuel, can significantly reduce emissions of CO, HC, and particulate matter (PM) due to its unique molecular structure. Nonetheless, its lower calorific value and poor cold-start performance limit its application, while its high oxygen content may contribute to increased NOx emissions. To address these limitations, researchers have proposed blending biodiesel with alcohol-based fuels such as methanol, ethanol, or butanol to create synergistic combustion systems that optimize engine performance and emission characteristics. This paper systematically reviews the effects of alcohol fuels on the performance and emission characteristics of biodiesel blends in diesel engines. Studies indicate that the addition of alcohol fuels can significantly enhance engine performance by improving fuel atomization, extending ignition delay, and increasing premixed combustion efficiency. These enhancements result in higher cylinder pressure, net heat release rate (HRR), and brake thermal efficiency (BTE), while reducing brake-specific fuel consumption (BSFC) to some extent. Moreover, most studies report that alcohol fuels help reduce CO, HC, smoke, and NOx emissions but tend to increase CO2 emissions. However, some findings suggest that in certain cases, the opposite results may occur. The impact of different types of alcohol fuels on performance and emissions varies significantly, requiring a comprehensive evaluation of their properties, such as latent heat, viscosity, and oxygen content. Although the appropriate addition of alcohol fuels demonstrates substantial potential for optimizing engine performance and reducing emissions, excessive blending may lead to adverse effects, necessitating careful control of the blending ratio. Future research should consider mixing two or more alcohol fuels with biodiesel to explore synergistic effects beyond the capabilities of single alcohols. Additionally, further studies should focus on optimizing fuel compositions and emission control strategies for varying operating conditions. Full article
(This article belongs to the Special Issue Combustion of Alternative Fuel Blends)
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<p>Types of raw materials for producing biofuels [<a href="#B12-energies-17-06274" class="html-bibr">12</a>].</p>
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17 pages, 2736 KiB  
Article
Effects of Decanol Blended Diesel Fuel on Engine Efficiency and Pollutant Emissions
by Kwonwoo Jang, Jeonghyeon Yang, Beomsoo Kim and Jaesung Kwon
Energies 2024, 17(24), 6223; https://doi.org/10.3390/en17246223 - 10 Dec 2024
Viewed by 387
Abstract
This study examined the effects of blending decanol, an oxygenated fuel, with diesel on diesel engine performance and emissions. Experiments were conducted on a single-cylinder engine at 1700 rpm and 2700 rpm, using diesel/decanol blends at 10%, 30%, and 50% by volume (D90de10, [...] Read more.
This study examined the effects of blending decanol, an oxygenated fuel, with diesel on diesel engine performance and emissions. Experiments were conducted on a single-cylinder engine at 1700 rpm and 2700 rpm, using diesel/decanol blends at 10%, 30%, and 50% by volume (D90de10, D70de30, D50de50). Results showed that brake thermal efficiency decreased with higher decanol ratios at low speeds. As a result, brake specific fuel consumption and brake specific energy consumption increased due to decanol’s lower calorific value. Regarding emissions, decanol blending reduced NOx, CO, HC, and smoke. NOx emissions were lowered by the cooling effect resulting from decanol’s higher latent heat of vaporization and lower calorific value, especially at low speeds. CO and HC emissions declined as decanol’s oxygen content promoted oxidation, reducing incomplete combustion. Smoke emissions were minimized in fuel-rich zones by preventing unburned carbon particle formation. This study highlights decanol’s potential as an eco-friendly diesel blending option. Future work should optimize blending ratios and injection settings to enhance diesel engine performance. Full article
(This article belongs to the Special Issue Renewable Fuels for Internal Combustion Engines: 2nd Edition)
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<p>Schematic diagram of the experimental apparatus.</p>
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<p>Comparison of brake thermal efficiency with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of brake specific fuel consumption with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of brake specific energy consumption with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of NO<sub>x</sub> emissions with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of CO emissions with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of HC emissions with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of smoke emissions with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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<p>Comparison of CO<sub>2</sub> emissions with brake mean effective pressure at (<b>a</b>) 1700 rpm and (<b>b</b>) 2700 rpm.</p>
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20 pages, 5980 KiB  
Article
Comprehensive Investigation of Partitioned Thermal Barrier Coating: Impact on Thermal and Mechanical Stresses, and Performance Enhancement in Diesel Engines
by Hüsna Topkaya, M. Quinn Brewster and Hüseyin Aydın
Appl. Sci. 2024, 14(24), 11506; https://doi.org/10.3390/app142411506 - 10 Dec 2024
Viewed by 407
Abstract
The thermal barrier coating method is applied using materials with low thermal conductivity to increase the efficiency and improve the emissions of internal combustion engines. However, coated surfaces may be damaged due to the high thermal and pressure stresses encountered by the piston [...] Read more.
The thermal barrier coating method is applied using materials with low thermal conductivity to increase the efficiency and improve the emissions of internal combustion engines. However, coated surfaces may be damaged due to the high thermal and pressure stresses encountered by the piston surface in the combustion chamber during engine operation. In this study, experiments and analysis were carried out for four piston models to analyze the coating layer and increase its strength: two partially coated piston surface models, a fully coated model, and an uncoated piston model. The results of the transient thermal analysis revealed that the fully coated piston model exhibited the highest surface temperature. Additionally, heat losses were observed to be lower in the fully coated model compared to the other piston models. Partially coated piston models exhibited lower heat flux on the coated surface but higher heat flux on the uncoated combustion chamber surfaces. Combustion analysis indicated that the fully coated piston model exhibited the highest in-cylinder temperature and pressure values, while the uncoated model had the lowest values. When comparing heat transfer rates on the walls, the uncoated piston model exhibited the highest transfer, whereas the fully coated piston model exhibited the lowest. Finally, the fully coated piston demonstrated the highest combustion efficiency. Full article
(This article belongs to the Section Applied Thermal Engineering)
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Figure 1
<p>Schematic diagram of the experimental setup.</p>
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<p>(<b>a</b>) Fully coated piston. (<b>b</b>) Piston with a 5 mm wide uncoated area on the piston top surface. (<b>c</b>) Piston with a 10 mm uncoated area on the piston top surface.</p>
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<p>(<b>a</b>) FC piston geometry and coating layers. (<b>b</b>) PC-5 piston model. (<b>c</b>) PC-10 piston model.</p>
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<p>Thermal boundary conditions used in finite element analysis.</p>
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<p>Computational grid of combustion chamber.</p>
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<p>(<b>a</b>) Temperature distribution of NC assembly model, (<b>b</b>) FC assembly model, (<b>c</b>) PC-5 assembly model, and (<b>d</b>) PC-10 assembly model.</p>
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<p>(<b>a</b>) Temperature distribution of NC, FC, PC-5, and PC-10 pistons for 60 s. (<b>b</b>) Temperature distribution in the range of 59.88 to 60 s; (<b>c</b>) temperature distribution for the first 0.08 s; (<b>d</b>) temperature distribution for the first 5 s.</p>
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<p>(<b>a</b>) Temperature distribution of FC piston layers along the path from 1 to 2: (<b>b</b>) coated surfaces, (<b>c</b>) bond-coated surfaces, (<b>d</b>) substrate surfaces.</p>
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<p>(<b>a</b>) Total heat flux change; (<b>b</b>) total heat flux change for the first cycle; (<b>c</b>) total heat flux change for the last two cycles.</p>
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<p>(<b>a</b>) von Mises stress variation. (<b>b</b>) von Mises stress variation at the coating surface. (<b>c</b>) von Mises stress variation on the piston surface.</p>
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<p>The total deformation distribution for (<b>a</b>) NC assembly model, (<b>b</b>) FC assembly model, (<b>c</b>) PC-5 assembly model, and (<b>d</b>) PC-10 assembly model.</p>
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<p>Comparison of experimental and simulation pressure values for NC and FC piston models.</p>
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<p>In-cylinder pressure and HRR values for different piston models.</p>
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<p>In-cylinder temperature values and variation in the heat transfer on the wall as a function of crank angle for different piston models.</p>
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<p>The impact of thermal barrier coating (TBC) on exhaust emissions: (<b>a</b>) NO<sub>X</sub>, (<b>b</b>) CO, and (<b>c</b>) HC.</p>
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<p>Cylinder internal temperature distribution according to different piston models and crank angles.</p>
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<p>The effect of TBC on efficiency.</p>
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18 pages, 4360 KiB  
Article
Fluid Dynamic and Thermal Performance of a V-Shape Slotted Cylinder
by Abdulwahab Alhashem, Sultan Alshareef, Ali Y. Alharbi and Mosab A. Alrahmani
Energies 2024, 17(23), 6192; https://doi.org/10.3390/en17236192 - 9 Dec 2024
Viewed by 369
Abstract
The flow characteristics and thermal performance of circular cylinders with V-shape slots are investigated numerically. The simulation is a two-dimensional incompressible flow that employs the semi-implicit finite volume multi-material algorithm MPM-ICE, which is a module of the Uintah framework. The normalized slot width [...] Read more.
The flow characteristics and thermal performance of circular cylinders with V-shape slots are investigated numerically. The simulation is a two-dimensional incompressible flow that employs the semi-implicit finite volume multi-material algorithm MPM-ICE, which is a module of the Uintah framework. The normalized slot width s2/D ranges from 0.1 to 0.2, and the corresponding increases in total surface area are from ~99% to ~70%, respectively. Compared to the solid cylinder, the slotted cylinder has the largest total drag reduction of ~67% at s2/D of 0.2. Meanwhile, although the heat transfer is proportional with the surface area, the thermal performance of the V-shape slot first improves with the slot width, and then declines. The heat transfer improvement has an optimum value of ~192% at s2/D of 0.15. The overall slot performance, defined by the ratio of the heat transfer to the drag force, is best at 0.175. Full article
(This article belongs to the Section J1: Heat and Mass Transfer)
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<p>Numerical details: (<b>a</b>) problem setup and (<b>b</b>) mesh quality (coarsest mesh) of the upper half of a cylinder with a horizontal slot with constant width of <span class="html-italic">s</span>/<span class="html-italic">D</span> = 0.1 [<a href="#B31-energies-17-06192" class="html-bibr">31</a>].</p>
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<p>Convergence trend of Nusselt number <span class="html-italic">Nu</span> as a function of normalized mesh resolution.</p>
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<p>Time history of <span class="html-italic">C<sub>D</sub></span> and <span class="html-italic">C<sub>L</sub></span> for a cylinder in cross flow for <span class="html-italic">Re<sub>D</sub></span> = 1000.</p>
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<p>Validation of the numerical results versus benchmark data of a solid cylinder (<span class="html-italic">s</span><sub>1</sub> = <span class="html-italic">s</span><sub>2</sub> = 0) (<b>a</b>) <span class="html-italic">C<sub>D</sub></span> [<a href="#B31-energies-17-06192" class="html-bibr">31</a>] (<b>b</b>) <span class="html-italic">Nu</span> [<a href="#B31-energies-17-06192" class="html-bibr">31</a>].</p>
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<p>Normalized time-averaged velocity magnitude for (<b>a</b>) solid cylinder (<span class="html-italic">s</span><sub>1</sub>= <span class="html-italic">s</span><sub>2</sub> = 0), (<b>b</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.1, (<b>c</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.125, (<b>d</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.15, (<b>e</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.175, and (<b>f</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.2.</p>
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<p>Normalized instantaneous velocity magnitude for (<b>a</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.1, (<b>b</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.125, (<b>c</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.15, (<b>d</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.175, and (<b>e</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.2.</p>
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<p>Transient <span class="html-italic">C<sub>D</sub></span> and <span class="html-italic">C<sub>L</sub></span> plots: (<b>a</b>) solid cylinder (<span class="html-italic">S</span><sub>1</sub> = <span class="html-italic">S</span><sub>2</sub> = 0), (<b>b</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.1, (<b>c</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.125, (<b>d</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.15, (<b>e</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.175, and (<b>f</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.2.</p>
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<p>Normalized time-averaged <span class="html-italic">x</span>-velocity component profile at slot entrance.</p>
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<p>Normalized instantaneous <span class="html-italic">x</span>-velocity component profile inside the slot showing the flip-flop phenomenon: (<b>a</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.1 and (<b>b</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.125.</p>
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<p>Normalized time-averaged temperature for (<b>a</b>) solid cylinder (<span class="html-italic">s</span><sub>1</sub>= <span class="html-italic">s</span><sub>2</sub> = 0), (<b>b</b>) <span class="html-italic">s</span><sub>2</sub><span class="html-italic">/D</span> = 0.1, (<b>c</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.125, (<b>d</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.15, (<b>e</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.175, and (<b>f</b>) <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> = 0.2.</p>
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<p>Performance analysis as a function of <span class="html-italic">s</span><sub>2</sub>/<span class="html-italic">D</span> (<b>a</b>) <span class="html-italic">C<sub>D</sub></span>*, (<b>b</b>) <span class="html-italic">Q</span>*, and (<b>c</b>) <span class="html-italic">Q</span>*/<span class="html-italic">C<sub>D</sub></span>*.</p>
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