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23 pages, 77065 KiB  
Article
Effects of Temperature and Frequency on Fretting Wear Behavior of 316L Austenitic Stainless Steel Before and After Plasma Carburization
by Lu Sun, Yuandong Li, Chi Cao, Guangli Bi, Xiaomei Luo and Jin Qiu
Coatings 2024, 14(12), 1496; https://doi.org/10.3390/coatings14121496 - 28 Nov 2024
Viewed by 400
Abstract
Double-glow low-temperature plasma carburization (LTPC) was utilized to prepare a carburized layer (PC) on a 316L austenitic stainless steel (ASS) surface, and the fretting wear behavior was evaluated at various temperatures and frequencies. The friction coefficient curves could be divided into running-in, wear, [...] Read more.
Double-glow low-temperature plasma carburization (LTPC) was utilized to prepare a carburized layer (PC) on a 316L austenitic stainless steel (ASS) surface, and the fretting wear behavior was evaluated at various temperatures and frequencies. The friction coefficient curves could be divided into running-in, wear, and stable stages. With increasing temperature, the wear mechanism of 316L ASS changed from adhesive and abrasive wear to adhesive wear, accompanied by plastic deformation, fatigue peeling, and oxidative wear. The carburized layer had an adhesive wear, plastic deformation, fatigue peeling, and oxidative wear mechanism. As the frequency increased, 316L ASS showed an adhesive wear, fatigue peeling, and oxidative wear mechanism. With increasing frequency, the wear mechanism of PC changed from abrasive and adhesive wear to abrasive wear, adhesive wear, and fatigue peeling, accompanied by oxidative wear. The carburized layer generally showed lower frictional energy dissipation coefficients and wear rates than 316L ASS. This work demonstrated that plasma carburization could improve the fretting wear stability and resistance of 316L ASS. The rise in frictional temperature, the tribo-chemical reaction time, and the evolution of debris collectively influenced the wear mechanisms and wear morphologies of 316L ASS before and after plasma carburization. This could provide theoretical support for the fretting damage behaviors of ball valves under severe service conditions. Full article
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Figure 1
<p>The schematic diagram of the fretting wear test.</p>
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<p>(<b>a</b>) Friction coefficient of 316L ASS under different temperatures, (<b>b</b>) friction coefficient of carburized layer under different temperatures, (<b>c</b>) friction coefficient of 316L ASS under different frequencies, (<b>d</b>) friction coefficient of carburized layer under different frequencies, (<b>e</b>) average friction coefficient of 316L ASS and carburized layer under different temperatures, and (<b>f</b>) average friction coefficient of 316L ASS and carburized layer under different frequencies.</p>
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<p>Effects of friction coefficient of 316L ASS and carburized layer under different temperatures and frequencies.</p>
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<p>Wear scar morphologies of 316L ASS at (<b>a1</b>) 50 °C, (<b>b1</b>) 75 °C, (<b>c1</b>) 100 °C, (<b>d1</b>) 150 °C, (<b>e1</b>) 200 °C, (<b>f1</b>) 250 °C, and (<b>g1</b>) 300 °C. Wear scar morphologies of the carburized layer at (<b>a2</b>) 50 °C, (<b>b2</b>) 75 °C, (<b>c2</b>) 100 °C, (<b>d2</b>) 150 °C, (<b>e2</b>) 200 °C, (<b>f2</b>) 250 °C, and (<b>g2</b>) 300 °C.</p>
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<p>Wear scar morphologies of 316L ASS at (<b>a1</b>) 50 °C, (<b>b1</b>) 75 °C, (<b>c1</b>) 100 °C, (<b>d1</b>) 150 °C, (<b>e1</b>) 200 °C, (<b>f1</b>) 250 °C, and (<b>g1</b>) 300 °C. Wear scar morphologies of the carburized layer at (<b>a2</b>) 50 °C, (<b>b2</b>) 75 °C, (<b>c2</b>) 100 °C, (<b>d2</b>) 150 °C, (<b>e2</b>) 200 °C, (<b>f2</b>) 250 °C, and (<b>g2</b>) 300 °C.</p>
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<p>Wear scar morphologies of 316L ASS at (<b>a1</b>) 10 Hz, (<b>b1</b>) 50 Hz, (<b>c1</b>) 75 Hz, and (<b>d1</b>) 100 Hz. Wear scar morphologies of the carburized layer at (<b>a2</b>) 10 Hz, (<b>b2</b>) 50 Hz, (<b>c2</b>) 75 Hz, and (<b>d2</b>) 100 Hz.</p>
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<p>Wear scar morphologies of 316L ASS at (<b>a1</b>) 10 Hz, (<b>b1</b>) 50 Hz, (<b>c1</b>) 75 Hz, and (<b>d1</b>) 100 Hz. Wear scar morphologies of the carburized layer at (<b>a2</b>) 10 Hz, (<b>b2</b>) 50 Hz, (<b>c2</b>) 75 Hz, and (<b>d2</b>) 100 Hz.</p>
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<p>Oxygen element distribution of 316L ASS at (<b>a1</b>) 50 °C, (<b>b1</b>) 75 °C, (<b>c1</b>) 100 °C, (<b>d1</b>) 150 °C, (<b>e1</b>) 200 °C, (<b>f1</b>) 250 °C, and (<b>g1</b>) 300 °C. Oxygen element distribution of carburized layer at (<b>a2</b>) 50 °C, (<b>b2</b>) 75 °C, (<b>c2</b>) 100 °C, (<b>d2</b>) 150 °C, (<b>e2</b>) 200 °C, (<b>f2</b>) 250 °C, and (<b>g2</b>) 300 °C.</p>
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<p>Oxygen element distribution of 316L ASS at (<b>a1</b>) 10 Hz, (<b>b1</b>) 50 Hz, (<b>c1</b>) 75 Hz, and (<b>d1</b>) 100 Hz. Oxygen element distribution of carburized layer at (<b>a2</b>) 10 Hz, (<b>b2</b>) 50 Hz, (<b>c2</b>) 75 Hz, and (<b>d2</b>) 100 Hz.</p>
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<p>OM images of wear marks of the GCr15 ball from Gcr15/316L at (<b>a1</b>) 50 °C, (<b>b1</b>) 75 °C, (<b>c1</b>) 100 °C, (<b>d1</b>) 150 °C, (<b>e1</b>) 200 °C, (<b>f1</b>) 250 °C, and (<b>g1</b>) 300 °C. OM images of wear marks of the GCr15 ball from Gcr15/PC at (<b>a2</b>) 50 °C, (<b>b2</b>) 75 °C, (<b>c2</b>) 100 °C, (<b>d2</b>) 150 °C, (<b>e2</b>) 200 °C, (<b>f2</b>) 250 °C, and (<b>g2</b>) 300 °C.</p>
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<p>OM images of wear marks of the GCr15 ball from Gcr15/316L at (<b>a1</b>) 50 °C, (<b>b1</b>) 75 °C, (<b>c1</b>) 100 °C, (<b>d1</b>) 150 °C, (<b>e1</b>) 200 °C, (<b>f1</b>) 250 °C, and (<b>g1</b>) 300 °C. OM images of wear marks of the GCr15 ball from Gcr15/PC at (<b>a2</b>) 50 °C, (<b>b2</b>) 75 °C, (<b>c2</b>) 100 °C, (<b>d2</b>) 150 °C, (<b>e2</b>) 200 °C, (<b>f2</b>) 250 °C, and (<b>g2</b>) 300 °C.</p>
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<p>OM images of wear marks of the GCr15 ball from GCr15/316L at (<b>a1</b>) 10 Hz, (<b>b1</b>) 50 Hz, (<b>c1</b>) 75 Hz, and (<b>d1</b>) 100 Hz. OM images of wear marks of the GCr15 ball from GCr15/PC at (<b>a2</b>) 10 Hz, (<b>b2</b>) 50 Hz, (<b>c2</b>) 75 Hz, and (<b>d2</b>) 100 Hz.</p>
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<p>Wear profiles of 316L ASS and carburized layer under different temperatures of (<b>a</b>) 50 °C, (<b>b</b>) 75 °C, (<b>c</b>) 100 °C, (<b>d</b>) 150 °C, (<b>e</b>) 200 °C, (<b>f</b>) 250 °C, and (<b>g</b>) 300 °C.</p>
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<p>Wear profiles of 316L ASS and carburized layer under different frequencies of (<b>a</b>) 10 Hz, (<b>b</b>) 50 Hz, (<b>c</b>) 75 Hz, and (<b>d</b>) 100 Hz.</p>
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<p>Wear volumes and wear rates of 316L ASS and carburized layer under different (<b>a</b>) temperatures and (<b>b</b>) frequencies.</p>
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<p>Fretting wear process at (<b>a1</b>) initial friction stage of 316L, (<b>a2</b>) initial friction stage of PC, (<b>b1</b>) debris formation stage of 316L, (<b>b2</b>) debris formation stage of PC, (<b>c1</b>) three-body contact stage of 316L, (<b>c2</b>) three-body contact stage of PC, (<b>d1</b>) oxide film formation and action stage of 316L, and (<b>d2</b>) oxide film formation and action stage of PC.</p>
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<p>(<b>a</b>) Schematic diagram of frictional dissipated energy and (<b>b</b>) frictional dissipation energy coefficient of 316L and carburized layer under different temperatures and frequencies.</p>
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31 pages, 5958 KiB  
Article
Biogas Production from a Solar-Heated Temperature-Controlled Biogas Digester
by Francis Makamure, Patrick Mukumba and Golden Makaka
Sustainability 2024, 16(22), 9894; https://doi.org/10.3390/su16229894 - 13 Nov 2024
Viewed by 980
Abstract
This research paper explores biogas production in an underground temperature-controlled fixed dome digester and compares it with a similar uncontrolled digester. Two underground fixed-dome digesters, one fitted with a solar heating system and a stirrer and the other one with an identical stirrer [...] Read more.
This research paper explores biogas production in an underground temperature-controlled fixed dome digester and compares it with a similar uncontrolled digester. Two underground fixed-dome digesters, one fitted with a solar heating system and a stirrer and the other one with an identical stirrer only, were batch-fed with cow dung slurry collected from the University of Fort Hare farm and mixed with water in a ratio of 1:1. The solar heating system consisted of a solar geyser, pex-al-pex tubing, an electric ball valve, a water circulation pump, an Arduino aided temperature control system, and a heat exchanger located at the centre of the digester. Both the digesters were intermittently stirred for 10 min every 4 h. The digester without a heating system was used as a control. Biogas production in the two digesters was compared to assess the effect of solar heating on biogas production. The total solids, volatile solids, and the chemical oxygen demand of the cow dung used as substrate were determined before and after digestion. These were compared together with the cumulative biogas produced and the methane content for the controlled and uncontrolled digesters. It was observed that the temperature control system kept the slurry temperature in the controlled digester within the required range for 82.76% of the retention period, showing an efficiency of 82.76%. Some maximum temperature gradients of 7.0 °C were observed in both the controlled and uncontrolled digesters, showing that the stirrer speed of 30 rpm was not fast enough to create the needed vortex for a uniform mix in the slurry. It was further observed that the heat from the solar geyser and the ground insulation were sufficient to keep the digester temperature within the required temperature range without any additional heat source even at night. Biogas yield was observed to depend on the pH with a strong coefficient of determination of 0.788 and 0.755 for the controlled and uncontrolled digesters, respectively. The cumulative biogas was 26.77 m3 and 18.05 m3 for controlled and uncontrolled digesters, respectively, which was an increase of 33%. The methane content increased by 14% while carbon dioxide decreased by 10% from the uncontrolled to the controlled scenario. The percentage removal of the TS, VS, and COD was 66.26%, 76.81%, and 74.69%, respectively, compared to 47.01%, 60.37%, and 57.86% for the uncontrolled situation. Thus, the percentage removal of TS, VS, and COD increased by 19.25%, 16.44%, and 16.89%, respectively. Full article
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<p>Fixed dome biodigester (adapted from [<a href="#B24-sustainability-16-09894" class="html-bibr">24</a>].</p>
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<p>Floating drum biodigester (Adapted from [<a href="#B28-sustainability-16-09894" class="html-bibr">28</a>].</p>
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<p>Balloon digester (Adapted from [<a href="#B31-sustainability-16-09894" class="html-bibr">31</a>]).</p>
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<p>Structure of evacuated tube collector (adapted from [<a href="#B80-sustainability-16-09894" class="html-bibr">80</a>].</p>
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<p>Positions of temperature sensors in the digester (own diagram).</p>
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<p>Gas flow metre with digital display.</p>
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<p>Bosean gas Analyzer.</p>
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<p>Schematic diagram of temperature control and automation circuit.</p>
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<p>The experimental setup.</p>
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<p>The inside of the power and control house.</p>
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<p>Slurry and Ambient temperatures versus retention time.</p>
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<p>Volume of biogas produced versus retention time.</p>
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<p>Cumulative volume of biogas versus retention time.</p>
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<p>Comparison of biogas composition by percentage concentrations.</p>
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<p>Percentage removals in the heated digester.</p>
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<p>Percentage removals in unheated digester.</p>
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<p>pH versus retention time for heated and unheated digesters.</p>
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<p>Biogas yield versus pH for heated and unheated digesters.</p>
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25 pages, 13135 KiB  
Article
Research on Hydraulic Characteristics of Water Leakage Phenomenon of Waterproof Hammer Air Valve in Water Supply Pressure Pipeline Based on Sustainable Utilization of Water Resources in Irrigation Areas
by Yixiong Cheng, Yuan Tang, Jianhua Wu, Hua Jin, Lixia Shen and Zhiyong Sun
Sustainability 2024, 16(22), 9868; https://doi.org/10.3390/su16229868 - 12 Nov 2024
Viewed by 639
Abstract
To investigate the causes of water leakage in the waterproof hammer air valve and its impact on sustainable water resource management, the DN100 waterproof hammer air valve was taken as the research object. By using the overset grid solution method of ANSYS Fluent [...] Read more.
To investigate the causes of water leakage in the waterproof hammer air valve and its impact on sustainable water resource management, the DN100 waterproof hammer air valve was taken as the research object. By using the overset grid solution method of ANSYS Fluent 2021 R1 software, the flow field simulation of the waterproof hammer air valve was carried out. The transient action during the ascent phase of the key structural component floating ball, and the velocity and pressure distribution of the flow field inside the air valve are analyzed. The results showed that by giving different inlet flow velocities, the normal flow velocity range for the floating ball to float up was below 35 m/s and above 50 m/s. When the inlet flow velocity was between 35 m/s and 50 m/s, the growth rate of the pressure difference above and below the floating ball increased from 1.48% to 5.79% and then decreased to 0.4%. The floating ball would not be able to float up due to excessive outlet pressure above, which would cause the DN100 waterproof hammer air valve to leak water and fail to provide water hammer protection. When the inlet flow rate is 5 m/s, the velocity and pressure inside the valve body increase with time during the upward movement of the floating ball inside the waterproof hammer air valve and tend to stabilize at 400 ms. Through the generated pressure and velocity cloud maps, it can be observed that the location of maximum pressure is at the bottom of the buoy, directly below the floating ball, and at the narrow channels on both sides of the outflow domain. The location of the maximum velocity is at the small inlet of the bottom of the buoy. When the inlet speed of the valve is constant, a large amount of water flow is blocked by the floating ball, reducing the flow velocity and forming partial backflow below the floating ball, with an obvious vortex phenomenon. A small portion of the water flow passes through the air valve at a high velocity from both ends of the channel, and the water flow below the floating ball is in an extremely unstable state under the impact of high-speed water flow, resulting in a large gradient of water flow velocity passing through the valve. The research results not only help to improve the operational efficiency of water resource management systems but also reduce unnecessary water resource waste, thereby supporting the goal of sustainable water resource management. Full article
(This article belongs to the Section Sustainable Water Management)
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Figure 1
<p>Schematic diagram of water supply from a pumping station in an irrigation district.</p>
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<p>Structural diagram of the waterproof hammer air valve.</p>
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<p>Schematic diagram of the operation phase division of the waterproof hammer air valve.</p>
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<p>Geometric models of (<b>a</b>) the floating ball, (<b>b</b>) the bonnet, (<b>c</b>) the buoy, and (<b>d</b>) the assembled body.</p>
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<p>A diagram of the assembled waterproof hammer air valve.</p>
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<p>A diagram of the fluid domain.</p>
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<p>A diagram of the overset grid.</p>
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<p>A diagram of the boundary layer.</p>
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<p>A diagram of the grid section.</p>
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<p>The grid quality cloud map.</p>
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<p>A preview of the converted grid.</p>
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<p>Diagrams of the grid trial calculation process.</p>
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<p>Internal pressure nephogram.</p>
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<p>Internal velocity nephogram.</p>
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<p>Internal streamline nephogram.</p>
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<p>Graph of maximum pressure and maximum speed inside the waterproof hammer air valve with time.</p>
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<p>Cloud map of internal pressure of air valve under different inlet flow rates.</p>
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<p>Cloud map of internal pressure of air valve under different inlet flow rates.</p>
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<p>Cloud map of internal velocity of air valve under different inlet flow rates.</p>
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<p>Cloud map of internal velocity of air valve under different inlet flow rates.</p>
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<p>Graph of maximum pressure and maximum speed inside air valve with inlet velocity.</p>
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<p>Pressure changes above and below the floating ball.</p>
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<p>Initial state flow field pressure nephogram at an inlet velocity of 35 m/s.</p>
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<p>Initial state flow field pressure nephogram at an inlet velocity of 50 m/s.</p>
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25 pages, 8051 KiB  
Article
Dexterous Manipulation Based on Object Recognition and Accurate Pose Estimation Using RGB-D Data
by Udaka A. Manawadu and Naruse Keitaro
Sensors 2024, 24(21), 6823; https://doi.org/10.3390/s24216823 - 24 Oct 2024
Viewed by 948
Abstract
This study presents an integrated system for object recognition, six-degrees-of-freedom pose estimation, and dexterous manipulation using a JACO robotic arm with an Intel RealSense D435 camera. This system is designed to automate the manipulation of industrial valves by capturing point clouds (PCs) from [...] Read more.
This study presents an integrated system for object recognition, six-degrees-of-freedom pose estimation, and dexterous manipulation using a JACO robotic arm with an Intel RealSense D435 camera. This system is designed to automate the manipulation of industrial valves by capturing point clouds (PCs) from multiple perspectives to improve the accuracy of pose estimation. The object recognition module includes scene segmentation, geometric primitives recognition, model recognition, and a color-based clustering and integration approach enhanced by a dynamic cluster merging algorithm. Pose estimation is achieved using the random sample consensus algorithm, which predicts position and orientation. The system was tested within a 60° field of view, which extended in all directions in front of the object. The experimental results show that the system performs reliably within acceptable error thresholds for both position and orientation when the objects are within a ±15° range of the camera’s direct view. However, errors increased with more extreme object orientations and distances, particularly when estimating the orientation of ball valves. A zone-based dexterous manipulation strategy was developed to overcome these challenges, where the system adjusts the camera position for optimal conditions. This approach mitigates larger errors in difficult scenarios, enhancing overall system reliability. The key contributions of this research include a novel method for improving object recognition and pose estimation, a technique for increasing the accuracy of pose estimation, and the development of a robot motion model for dexterous manipulation in industrial settings. Full article
(This article belongs to the Section Intelligent Sensors)
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<p>A simple schematic diagram of integrated systems used in previous research.</p>
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<p>System architecture for the proposed system for object recognition, pose estimation, and dexterous manipulation. The methodology for preprocessing is described in detail in <a href="#sec3-sensors-24-06823" class="html-sec">Section 3</a>, object recognition is discussed in <a href="#sec5-sensors-24-06823" class="html-sec">Section 5</a>, pose estimation is covered in <a href="#sec5dot1-sensors-24-06823" class="html-sec">Section 5.1</a>, and information about the yellow and green zones is provided in <a href="#sec5dot2-sensors-24-06823" class="html-sec">Section 5.2</a>.</p>
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<p>Geometric abstractions of valve types. The globe valve (<b>left</b>) is represented by a combination of a cylinder and a disc, and the ball valve (<b>right</b>) is depicted as a cylinder and a plane.</p>
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<p>Output of the object recognition module.</p>
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<p>Position and orientation prediction using a RANSAC circle. Yellow points are inliers that are used for the RANSAC algorithm. In (<b>a</b>–<b>e</b>), images are depicted at a 30-degree interval on the yaw axis. (<b>a</b>) Pitch 0, yaw -60; (<b>b</b>) pitch 0, yaw -30; (<b>c</b>) pitch 0, yaw 0; (<b>d</b>) pitch 0, yaw 30; and (<b>e</b>) pitch 0, yaw 60.</p>
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<p>The “yellow” and “green” zones in the testing environment are shown in a schematic diagram of transitioning from the initial position in the yellow zone to the green zone’s final position. The range for the green zone is tested in this research.</p>
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<p>(<b>a</b>) Manipulation of the globe valve. (<b>b</b>) Manipulation of ball valve.</p>
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<p>Depiction of pitch and yaw terminology: (<b>a</b>) yaw and (<b>b</b>) pitch axis changes.</p>
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<p>Experimental results of the 3D object recognition (sub-figures a2–e2) and pose estimation (sub-figures a3–e3) of a globe valve at different yaw angles in the pitch 000 axis.</p>
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<p>Experimental results of the 3D object recognition (sub-figures a2–e2) and pose estimation (sub-figures a3–e3) of a ball valve at different yaw angles in the pitch 000 axis.</p>
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<p>Surface plot for <a href="#sensors-24-06823-t002" class="html-table">Table 2</a> and <a href="#sensors-24-06823-t003" class="html-table">Table 3</a> for the globe valve. The left plot represents position errors, while the right plot represents orientation errors at different yaw angles and distances from the object. A blue-colored surface in the plot indicates the accepted threshold range.</p>
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<p>SD surface plot for the globe valve given by <a href="#sensors-24-06823-t004" class="html-table">Table 4</a>. A blue-colored surface in the plot indicates the accepted threshold range.</p>
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<p>Experimental results for the 3D object recognition (sub-figures a2–e2) and pose estimation (sub-figures a3–e3) of the ball valve from different yaw and pitch axes.</p>
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<p>Surface plot for <a href="#sensors-24-06823-t005" class="html-table">Table 5</a> and <a href="#sensors-24-06823-t006" class="html-table">Table 6</a> for the ball valve. The left plot represents position error, while the right plot represents the orientation error at different yaw angles and distances from the object. A blue-colored surface in the plot indicates the accepted threshold range.</p>
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<p>Surface plot for <a href="#sensors-24-06823-t007" class="html-table">Table 7</a> showing the position errors of the ball valve results at different pitch and yaw angles. A blue-colored surface indicates the accepted threshold range.</p>
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<p>Steps for globe valve manipulation. (<b>a</b>) starting point, (<b>b</b>) moving to the green zone, (<b>c</b>) standby position, (<b>d</b>,<b>e</b>) manipulation of the valves, and (<b>f</b>) final position.</p>
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<p>Steps for ball valve manipulation. (<b>a</b>) starting point, (<b>b</b>) moving to the green zone, (<b>c</b>) standby position, (<b>d</b>,<b>e</b>) manipulation of the valves, and (<b>f</b>) final position.</p>
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27 pages, 8016 KiB  
Article
Carbon Emission Accounting Model of Three-Stage Mechanical Products for Manufacturing Process
by Minjie Wang, Yuanbo Wu and Bin Wang
Sustainability 2024, 16(18), 8101; https://doi.org/10.3390/su16188101 - 17 Sep 2024
Viewed by 1307
Abstract
Carbon accounting is critical to manufacturing and achieving a low-carbon transition and lean carbon management. A comprehensive understanding of carbon emissions in manufacturing is essential to calculate a product’s carbon footprint accurately. Based on the life cycle assessment (LCA) method, this study divides [...] Read more.
Carbon accounting is critical to manufacturing and achieving a low-carbon transition and lean carbon management. A comprehensive understanding of carbon emissions in manufacturing is essential to calculate a product’s carbon footprint accurately. Based on the life cycle assessment (LCA) method, this study divides the whole process of mechanical products from parts to finished products into three stages: parts (P), assembly (A), and testing (T). By decomposing each stage’s carbon emission sources and combining each stage’s characteristics, a series of corresponding carbon emission accounting models is established. Finally, the three-stage carbon emission model of the manufacturing process of a three-piece ball valve is established, and the validity and feasibility of the proposed model are verified. The results show that raw material consumption, energy consumption, and transportation are the primary sources of carbon emissions in the manufacturing process of three-piece ball valves, accounting for 35.6%, 38.8%, and 17.6%, respectively. The corresponding carbon emissions were 17.854 kgCO2e, 19.405 kgCO2e, and 8.8 kgCO2e, respectively. Through these results, we can provide some theoretical and data support for the low-carbon transformation of manufacturing enterprises as well as some research ideas for realizing low-carbon production through process planning and shop scheduling. Full article
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<p>Assessment boundaries of product carbon emissions.</p>
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<p>Carbon emission structure analysis of parts.</p>
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<p>Product carbon emission accounting process.</p>
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<p>Three-piece fixed ball valve structure diagram. ① valve body; ② valve bonnet; ③ valve stem; ④ connection disc; ⑤ guide bushing; ⑥ anchor block; ⑦ valve ball; ⑧ valve seat ring.</p>
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<p>Machining process of P-HP.</p>
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<p>Assembly process schematic diagram for ball valve.</p>
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<p>Distribution of carbon emissions from materials and electricity consumption of P-PP.</p>
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<p>Distribution of carbon emission sources in P-HP machining processes (unit: kgCO<sub>2</sub>e). (<b>a</b>) Distribution of carbon emission sources in valve body machining processes; (<b>b</b>) distribution of carbon emission sources in valve bonnet machining processes; (<b>c</b>) distribution of carbon emission sources in valve stem machining processes; (<b>d</b>) distribution of carbon emission sources in valve ball machining processes.</p>
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<p>Distribution of carbon emission sources in P-HP machining processes (unit: kgCO<sub>2</sub>e). (<b>a</b>) Distribution of carbon emission sources in valve body machining processes; (<b>b</b>) distribution of carbon emission sources in valve bonnet machining processes; (<b>c</b>) distribution of carbon emission sources in valve stem machining processes; (<b>d</b>) distribution of carbon emission sources in valve ball machining processes.</p>
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<p>Proportional emissions of various carbon sources in the production process of ball valves.</p>
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16 pages, 15164 KiB  
Communication
Study on Traction Characteristics of Point Contact State under Oil–Air Lubrication
by Bing Su, Han Li, Jiongli Ren and Zeyu Gong
Lubricants 2024, 12(9), 299; https://doi.org/10.3390/lubricants12090299 - 25 Aug 2024
Viewed by 1234
Abstract
Oil–air lubrication technology is commonly utilized in the lubrication design of traditional components to reduce friction between contact pairs. This study focuses on testing the point-contact friction pairs of two quantitative valves using a self-made oil–air lubrication traction force machine with a G95Cr18 [...] Read more.
Oil–air lubrication technology is commonly utilized in the lubrication design of traditional components to reduce friction between contact pairs. This study focuses on testing the point-contact friction pairs of two quantitative valves using a self-made oil–air lubrication traction force machine with a G95Cr18 disk and ball as the friction pairs. The test data are analyzed using a four-parameter exponential model. Additionally, a calculation model of the oil–air lubrication flow field is established, defining boundary conditions and conducting flow field simulation analysis. The results of the ball and disk test show that the traction coefficient increases with load and decreases with entrainment speed. Furthermore, when the air-speed is 12 m/s, the traction coefficient is lower for the oil supply of 6 mL/min than for the oil supply of 1.5 mL/min. According to CFD analysis, the volume fraction of the oil phase in the contact area increases with the increase of entrainment speed when the slip–roll ratio is 0.1. The theoretical values from the four-parameter exponential model align well with the experimental results, and the fitting accuracy is higher than 0.95. Full article
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<p>Diagram of the traction ball disk testing machine.</p>
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<p>Diagram of the traction ball disk testing machine.</p>
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<p>Schematic diagram of point contact model.</p>
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<p>The mesh of the computational model.</p>
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<p>Variation of coefficient of traction with slip-to-roll ratio. (<b>a</b>) Changes in traction coefficient with the slip–roll ratio under different loads. (<b>b</b>) Changes in traction coefficient with the slip–roll ratio at different entrainment speeds.</p>
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<p>At injection speed of 0.05 mL/min, oil phase volume distribution of simulation results at different entrainment speeds with a slip–roll ratio of 0.1.</p>
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<p>At injection speed of 0.05 mL/min, oil phase volume distribution of simulation results at different entrainment speeds with a slip–roll ratio of 0.1.</p>
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<p>Variation of coefficient of traction with slip–roll ratio. (<b>a</b>) Changes in traction coefficient with the slip–roll ratio under different loads. (<b>b</b>) Changes in traction coefficient with the slip–roll ratio at different entrainment speeds.</p>
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<p>At injection speed of 0.2 mL/min, oil phase volume distribution of simulation results at different entrainment speeds with a slip–roll ratio of 0.1.</p>
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<p>At injection speed of 0.2 mL/min, oil phase volume distribution of simulation results at different entrainment speeds with a slip–roll ratio of 0.1.</p>
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<p>Traction coefficient curve changes with different oil supplies.</p>
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<p>Simulation and test comparison of different oil supplies.</p>
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<p>Fitting results of the four-parameter exponential model. (<b>a</b>) The quantitative valve is 0.05 mL/time, and the load is different. (<b>b</b>) The quantitative valve is 0.05 mL/time, and the entrainment speed is different. (<b>c</b>) The quantitative valve is 0.2 mL/time, and the load is different. (<b>d</b>) The quantitative valve is 0.2 mL/time, and the entrainment speed is different.</p>
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<p>Fitting results of the four-parameter exponential model. (<b>a</b>) The quantitative valve is 0.05 mL/time, and the load is different. (<b>b</b>) The quantitative valve is 0.05 mL/time, and the entrainment speed is different. (<b>c</b>) The quantitative valve is 0.2 mL/time, and the load is different. (<b>d</b>) The quantitative valve is 0.2 mL/time, and the entrainment speed is different.</p>
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30 pages, 9516 KiB  
Article
Numerical Simulation Study on Hydraulic Characteristics and Wear of Eccentric Semi-Ball Valve under Sediment Laden Water Flow
by Yixiong Cheng, Yuan Tang, Jianhua Wu, Hua Jin and Lixia Shen
Sustainability 2024, 16(17), 7266; https://doi.org/10.3390/su16177266 - 23 Aug 2024
Viewed by 886
Abstract
To investigate the variation laws of various hydraulic parameters and internal fluid flow patterns of eccentric semi-ball valves under different boundary conditions, the DPM model was used to numerically simulate the eccentric semi-ball valve based on Fluent 2021 R1 software. The flow velocity, [...] Read more.
To investigate the variation laws of various hydraulic parameters and internal fluid flow patterns of eccentric semi-ball valves under different boundary conditions, the DPM model was used to numerically simulate the eccentric semi-ball valve based on Fluent 2021 R1 software. The flow velocity, pressure distribution, and erosion wear rate on the valve wall were simulated under different combinations of opening, inlet flow velocity, and sediment concentration conditions, and hydraulic parameters such as drag coefficient, flow coefficient, and cavitation coefficient were calculated. The results show that as the opening of the eccentric semi-ball valve increases, the valve drag coefficient decreases, the flow coefficient increases, the cavitation coefficient increases, and the degree of cavitation decreases. The flow velocity in the high-velocity zone at both ends of the valve plate decreases, and the gradient of water flow velocity passing through the valve decreases. The area of the low-velocity zone at the rear of the valve plate decreases, and the vortex phenomenon gradually weakens; as the sediment content in the water increases, the valve drag coefficient increases, the flow coefficient decreases, and the cavitation coefficient first increases and then decreases. The maximum flow velocity of the pipeline decreases faster and faster, causing an increase in pressure gradient in the flow area and drastic changes. This results in higher pressure on the pipe wall near the valve plate, especially a significant increase in negative pressure; As the inlet flow rate increases, the valve drag coefficient decreases, the flow coefficient increases, and the cavitation coefficient gradually decreases. The flow velocity of the water passing through the valve increases, and the low-pressure area downstream of the valve plate increases. The pressure gradient at both ends of the valve port increases significantly from small to large, and the positive pressure upstream of the valve plate gradually increases. The force of the water flow on the valve plate is large, causing friction between the valve stem and the valve body, which is not conducive to long-term operation. With the increase in inlet flow rate, the maximum wear amount and wear range of the valve plate have significantly increased, and erosion wear is mainly distributed in point blocks at the edge of the valve plate. This study can provide certain references and solutions for the key technology research of eccentric semi-ball valves and assess the performance indicators of the operation being maintained. Full article
(This article belongs to the Section Sustainable Water Management)
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<p>The drag coefficient testing device diagram for the eccentric semi-ball valve.</p>
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<p>Simplified structure diagram of eccentric semi-ball valve.</p>
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<p>Mathematical model of eccentric semi-ball valve.</p>
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<p>Grid partition of eccentric semi-ball valve and fluid domain. They should be listed as follows: (<b>a</b>) Fluid domain grid. (<b>b</b>) Pipeline entrance grid. (<b>c</b>) Eccentric semi-ball valve grid.</p>
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<p>Changes in various coefficients at different openings. They should be listed as follows: (<b>a</b>) Import and export pressure difference. (<b>b</b>) Drag coefficient. (<b>c</b>) Flow coefficient. (<b>d</b>) Cavitation coefficient.</p>
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<p>Changes in various coefficients under different sediment concentrations. They should be listed as follows: (<b>a</b>) Import and export pressure difference. (<b>b</b>) Drag coefficient. (<b>c</b>) Flow coefficient. (<b>d</b>) Cavitation coefficient.</p>
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<p>Changes in various coefficients at different inlet velocities. They should be listed as follows: (<b>a</b>) Import and export pressure difference. (<b>b</b>) Drag coefficient. (<b>c</b>) Flow coefficient. (<b>d</b>) Cavitation coefficient.</p>
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<p>Variation in pipe velocity at different openings.</p>
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<p>Diagram of the maximum flow velocity of the pipe at different openings.</p>
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<p>Variation in pipe pressure at different openings.</p>
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<p>The change in the maximum and minimum pressure of the pipe under different openings.</p>
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<p>Distribution diagram of valve wall erosion rates at different openings.</p>
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<p>Distribution diagram of valve wall erosion rates at different openings.</p>
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<p>Velocity variation diagram in pipelines under different sediment concentrations.</p>
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<p>Maximum flow velocity diagrams in the pipeline under different sediment concentrations.</p>
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<p>Pressure variation in pipelines under different sediment concentrations.</p>
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<p>Graph showing variations in maximum and minimum pipeline pressures under different sediment concentrations.</p>
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<p>Distribution of valve wall erosion rates at different sediment concentrations.</p>
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<p>Velocity variation diagrams in the pipeline under different inlet flow velocities.</p>
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<p>Maximum velocity diagrams in the pipeline under different inlet flow velocities.</p>
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<p>Pressure variation in pipelines under different inlet velocities.</p>
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<p>Pressure variation diagrams in pipelines under different inlet velocities show maximum and minimum pressures.</p>
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<p>Distribution maps of valve wall erosion rate at different inlet velocities.</p>
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18 pages, 14879 KiB  
Article
Numerical Analysis of the Sediment Erosion of the Balance Valve in a Buoyancy Regulation System
by Hao Liu, Shenshen Yang, Lei Wang, Yulong Li, Lei Mi, Fangyang Yuan and Cong Ye
J. Mar. Sci. Eng. 2024, 12(8), 1344; https://doi.org/10.3390/jmse12081344 - 7 Aug 2024
Viewed by 841
Abstract
Numerical analysis of the sediment erosion of the balance valve in a buoyancy regulation system was performed. A numerical model for the two-phase flow inside the balance valve was constructed based on the discrete phase model. The sediment erosion rate on the balance [...] Read more.
Numerical analysis of the sediment erosion of the balance valve in a buoyancy regulation system was performed. A numerical model for the two-phase flow inside the balance valve was constructed based on the discrete phase model. The sediment erosion rate on the balance valve was discussed, and the effects of five parameters were considered. The effects of the sediment concentration and valve opening were found to be significant, while the effects of the pressure difference, sediment density, and size were found to be moderate. The erosion rate, according to the numerical results, increased linearly with the sediment concentration, so long-term operation of a buoyancy regulation system in high-concentration areas should be avoided. The erosion rate was the highest when the valve opening was 46.3%, so half-open operating conditions are not recommended. The erosion rate was proportional to the square root of the pressure difference. However, adjusting the pressure difference may not be an effective method for regulating the total erosion. The superposition of the secondary flow and the main stream caused particles to spiral along with the fluid, resulting in asymmetric erosion at the working edge. The erosion rate on the working edge decreased with the increase in the sediment size. Conversely, the erosion rate on the valve ball surface increased with the sixth power of the sediment size. Considering that large particles are more likely to cause a blockage, it is recommended to install a seawater pretreatment device at the inlet to prevent large sediments from entering the valve and to improve the working life of the buoyancy regulation system. Full article
(This article belongs to the Section Ocean Engineering)
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Figure 1
<p>Structure of the balance valve: (<b>a</b>) sectional view and key dimensions, 1—valve seat, 2—guide sleeve, 3—valve core, 4—valve stem, 5—valve body. and (<b>b</b>) inside flow channel.</p>
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<p>Pressure evolution for different grid schemes.</p>
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<p>Working edge and its circumferential angle.</p>
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<p>Erosion rate contours at different pressure differences (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> <mo> </mo> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 7.6 × 10<sup>−5</sup> kg/s, (<b>b</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 10 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.087 × 10<sup>−4</sup> kg/s, (<b>c</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 15 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.335 × 10<sup>−4</sup> kg/s, (<b>d</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 20 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.544 × 10<sup>−4</sup> kg/s.</p>
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<p>Erosion rate contours at different pressure differences (<math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> <mo> </mo> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 7.6 × 10<sup>−5</sup> kg/s, (<b>b</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 10 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.087 × 10<sup>−4</sup> kg/s, (<b>c</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 15 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.335 × 10<sup>−4</sup> kg/s, (<b>d</b>) <math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 20 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.544 × 10<sup>−4</sup> kg/s.</p>
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<p>Erosion rates at the working edge and surface of the valve ball at different pressure differences: (<b>a</b>) working edge distribution and (<b>b</b>) valve ball surface.</p>
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<p>Flow field and its secondary flow: (<b>a</b>) vortex at the section near the outlet and (<b>b</b>) typical particle trajectories.</p>
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<p>Erosion rate contours at different valve openings (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> <mo> </mo> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>). (<b>a</b>) valve opening = 27.8%, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.2 × 10<sup>−5</sup> kg/s, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>u</mi> </mrow> <mrow> <mi>i</mi> <mi>n</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 5.61 m/s, (<b>b</b>) valve opening = 46.3%, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 3.51 × 10<sup>−5</sup> kg/s, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>u</mi> </mrow> <mrow> <mi>i</mi> <mi>n</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 8.95 m/s, (<b>c</b>) valve opening = 64.8%, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 4.74 × 10<sup>−5</sup> kg/s, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>u</mi> </mrow> <mrow> <mi>i</mi> <mi>n</mi> </mrow> </msub> </mrow> </semantics></math> = 12.06 m/s, (<b>d</b>) valve opening = 83.3%, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 6.05 × 10<sup>−5</sup> kg/s, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>u</mi> </mrow> <mrow> <mi>i</mi> <mi>n</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 15.4 m/s, (<b>e</b>) valve opening = 100%, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 7.57 × 10<sup>−5</sup> kg/s, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>u</mi> </mrow> <mrow> <mi>i</mi> <mi>n</mi> </mrow> </msub> <mo>=</mo> </mrow> </semantics></math> 19.29 m/s.</p>
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<p>Erosion rates at the working edge and surface of the valve ball at different valve openings: (<b>a</b>) working edge distribution and (<b>b</b>) valve ball surface.</p>
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<p>Erosion rate contours with different sediment densities (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.2 g/cm<sup>3</sup>, (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.6 g/cm<sup>3</sup>, (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 3.0 g/cm<sup>3</sup>.</p>
Full article ">Figure 9 Cont.
<p>Erosion rate contours with different sediment densities (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.2 g/cm<sup>3</sup>, (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.6 g/cm<sup>3</sup>, (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 3.0 g/cm<sup>3</sup>.</p>
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<p>Erosion rates at the working edge and surface of the valve ball with different sediment densities: (<b>a</b>) working edge distribution and (<b>b</b>) valve ball surface.</p>
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<p>Erosion rate contours with different sediment diameters (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20<math display="inline"><semantics> <mrow> <mo> </mo> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> </mrow> </semantics></math> (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 30<math display="inline"><semantics> <mrow> <mo> </mo> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> </mrow> </semantics></math> (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 40<math display="inline"><semantics> <mrow> <mo> </mo> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> <mo>,</mo> </mrow> </semantics></math> (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50<math display="inline"><semantics> <mrow> <mo> </mo> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>.</p>
Full article ">Figure 12
<p>Erosion rates at the working edge and surface of the valve ball with different sediment diameters: (<b>a</b>) working edge distribution and (<b>b</b>) valve ball surface.</p>
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<p>Erosion rate contours with different sediment concentrations (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 7.6 × 10<sup>−5</sup> kg/s, (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 150 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.28 × 10<sup>−4</sup> kg/s, (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 250 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 3.8 × 10<sup>−4</sup> kg/s, (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 350 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 5.32 × 10<sup>−4</sup> kg/s.</p>
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<p>Erosion rate contours with different sediment concentrations (<math display="inline"><semantics> <mrow> <mo>∆</mo> <mi>p</mi> </mrow> </semantics></math> = 5 MPa, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>ρ</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 1.8 g/cm<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>d</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 20 <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">μ</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>, valve opening = 100%). (<b>a</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 50 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 7.6 × 10<sup>−5</sup> kg/s, (<b>b</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 150 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 2.28 × 10<sup>−4</sup> kg/s, (<b>c</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 250 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 3.8 × 10<sup>−4</sup> kg/s, (<b>d</b>) <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>c</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 350 g/m<sup>3</sup>, <math display="inline"><semantics> <mrow> <msub> <mrow> <mi>Q</mi> </mrow> <mrow> <mi>s</mi> </mrow> </msub> </mrow> </semantics></math> = 5.32 × 10<sup>−4</sup> kg/s.</p>
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<p>Erosion rates at the working edge and surface of the valve ball with different sediment concentrations: (<b>a</b>) working edge distribution and (<b>b</b>) valve ball surface.</p>
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18 pages, 17404 KiB  
Article
Numerical Study of Solid–Gas Two-Phase Flow and Erosion Distribution in Glass Fiber-Reinforced Polymer Ball Valves
by Qi Chen, Yazhong Xia, Jiuyang Yu, Yaonan Dai, Kang Peng, Tianyi Zhang and Bowen Liu
Machines 2024, 12(8), 541; https://doi.org/10.3390/machines12080541 - 7 Aug 2024
Viewed by 676
Abstract
The use of glass fiber-reinforced polymer (GFRP) composites in fluid transport systems can effectively reduce corrosion damage caused by corrosive media. However, collisions between solid particles and the surfaces of ball valve flow passages can cause erosion damage and lead to safety issues. [...] Read more.
The use of glass fiber-reinforced polymer (GFRP) composites in fluid transport systems can effectively reduce corrosion damage caused by corrosive media. However, collisions between solid particles and the surfaces of ball valve flow passages can cause erosion damage and lead to safety issues. The two-phase flow and erosion characteristics of ball valves manufactured from resin-based fiber-reinforced composite materials were studied under different openings and particle sizes using the CFD-DPM method. The results indicate that both smaller and larger relative openings are prone to erosion damage at the thin edges of the valve ball. As the relative opening increases, the average erosion amount in the flow passage first increases and then decreases. The maximum average erosion amount is 0.0051 kg/m2·s when the relative opening is Cv = 40. At Cv = 40, erosion damage in the flow channel mainly occurs at the bottom of the inlet flow channel and the valve seat position. With increasing particle size, both the average and maximum erosion amounts in the flow channel increase. Larger particle sizes in the inlet flow channel significantly raise the erosion rate nearby, while at other locations, larger particle sizes mainly increase the erosion rate in the same area. During the use of GFRP valves, it is important to avoid introducing large-sized particles into the medium. Keeping the valve’s relative opening greater than 40 and using more erosion-resistant materials for the valve seat can effectively reduce the erosion of the composite ball valve and extend its service life. Full article
(This article belongs to the Section Machine Design and Theory)
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<p>Internal structure of GFRP ball valve.</p>
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<p>Flow passage structure.</p>
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<p>Simulation and experimental comparison of erosion rates.</p>
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<p>Grid unrelated validation. (<b>a</b>) Grid and outlet path; (<b>b</b>) comparison of velocity on line AB for different grid numbers.</p>
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<p>Velocity and relative total pressure distributions under different relative openings.</p>
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<p>Erosion rate distribution under different relative openings.</p>
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<p>Erosion rates under different relative openings.</p>
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<p>Erosion distribution on inlet side spool surface.</p>
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<p>Erosion rate distributions under different particle diameters.</p>
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<p>Schematic of extraction locations of erosion rate data.</p>
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<p>Erosion rate distribution of extraction location A.</p>
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<p>Erosion rate distribution of extraction location B.</p>
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<p>Erosion rate distribution of extraction location C.</p>
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<p>Erosion rate distribution of extraction location D.</p>
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<p>Erosion rate under different particle diameters.</p>
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16 pages, 6627 KiB  
Article
The Design and Application of a New Wireline Pressure Coring System for the Guangzhou Marine Geological Survey Methane Hydrate Expedition in the South China Sea
by Qiuping Lu, Rulei Qin, Yanjiang Yu, Liqiang Qi, Wenwei Xie, Hongfeng Lu, Benchong Xu, Haoxian Shi, Chenlu Xu and Xingchen Li
Appl. Sci. 2024, 14(15), 6753; https://doi.org/10.3390/app14156753 - 2 Aug 2024
Viewed by 1051
Abstract
Natural gas hydrate is widely distributed, shallow-buried, clean, and pollution-free and has enormous reserves, it is regarded as the alternative clean energy source in the oil and gas field with the most potential. Pressure coring is the only way to drill for gas [...] Read more.
Natural gas hydrate is widely distributed, shallow-buried, clean, and pollution-free and has enormous reserves, it is regarded as the alternative clean energy source in the oil and gas field with the most potential. Pressure coring is the only way to drill for gas hydrate core on the surface under in situ conditions, which is of great value for analyzing its occurrence conditions and reserves comprehensively. Based on this, a new wireline pressure coring system (WPCS) with a ball valve seal was designed and developed in this paper; it was applied in the deep sea for the first time in the South China Sea hydrate survey voyage of the Guangzhou Marine Geological Survey (GMGS). A total of 15 runs of deep-sea gas hydrate drilling and coring applications were carried out, and they tested well. The experimental water depth was 1700–1800 m, and the coring depth below the seafloor was about 100–150 m. The formation consisted of sandy hydrate and argillaceous hydrate. The results showed the following. (1) The success rate of ball valve turn-over could reach almost 100% in the argillaceous hydrate reservoir, although there are some isolated cases of pressure relief. Meanwhile, drilling in the sandy hydrate reservoir, the success rate was only 54.55%. (2) When drilling in the argillaceous hydrate reservoir, the core recovery rate could reach 80%, while in the sandy hydrate reservoir, it was almost 0%. In practice, the sandy formation with gas hydrate is stiff to drill compared to the performance in argillaceous formations. After our analysis, it was believed that the ball valve and core tube could be easily plugged by sand debris during the sampling of sandy hydrate formation. Moreover, the sandy core is easily plugged into the core liner because of the high friction of sand grains in clearance. (3) The pressure-holding effect of the core drilling tool was related to the formation of hydrate, the sealing form of the ball valve, and the environmental pressure. Sandy hydrate formations often caused the ball valve to jam, while the muddy hydrate formation did not. The research results of this paper have reference value for the further optimization of the WPCS structure, the optimization of drilling parameters, and the design parameters of the ball valve structure, which could be better used for the pressure coring of gas hydrate and subsequent research work in the future. Full article
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<p>The structure of WPCS.</p>
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<p>The position and schematic diagram of the ball valve: (<b>a</b>) the comparison of ball valve before and after turning; (<b>b</b>) the process of turn-over sealing of the downward motion unit.</p>
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<p>The physical diagram of section connection of the WPCS: (<b>a</b>) the upper barrel assembly of WPCS; (<b>b</b>) the lower barrel assembly of WPCS.</p>
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<p>The Pressure Core Analysis Transfer System: (<b>a</b>) the main part of the Pressure Core Analysis Transfer System; (<b>b</b>) pressure measurement of the hydrate core inside the autoclave before transfer; (<b>c</b>) transfer of the hydrate core inside the core tube with pressure holding.</p>
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<p>X wave and P wave scanning picture of several typical runs.</p>
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<p>The temperature and pressure curve of the WPCS in run 13 (the critical line is the phase equilibrium curve of gas hydrate). ① Lowered through the drill string to latch in the BHA; ② coring; ③ retrieved; ④ pressure core transferred.</p>
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<p>The temperature and pressure curve of the WPCS recorded over time during the whole coring process: (<b>a</b>) run 8; (<b>b</b>) run 9; (<b>c</b>) run 13. ① Lowered through the drill string to latch in the BHA; ② coring; ③ retrieved; ④ pressure core transferred.</p>
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<p>The temperature and pressure curve of the WPCS recorded over time during the whole coring process: (<b>a</b>) run 8; (<b>b</b>) run 9; (<b>c</b>) run 13. ① Lowered through the drill string to latch in the BHA; ② coring; ③ retrieved; ④ pressure core transferred.</p>
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<p>The physical picture of WPCS: (<b>a</b>) pressure-retaining core bit and BHA; (<b>b</b>) the water tunnels of core bit plugged by sand; (<b>c</b>) pressure-retaining ball valve turned over with sand.</p>
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<p>Force analysis near DMU.</p>
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<p>Several cases of ball valve turn-over sealing: (<b>a</b>) the unsuccessful case with no ball valve turn-over; (<b>b</b>) the successful turn-over sealing case of the ball valve.</p>
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13 pages, 2092 KiB  
Article
Multi-Parameter Complex Control of Metal Coatings on Ball Plugs of Pipeline Shut-Off Valves
by Varvara Alekhnovich, Vladimir Syasko and Alexander Umanskii
Inventions 2024, 9(4), 78; https://doi.org/10.3390/inventions9040078 - 15 Jul 2024
Cited by 3 | Viewed by 1414
Abstract
The greatest losses during gas transportation occur in the elements of shut-off valves, the operating parameters of which, among other things, depend on the thickness and hardness of the protective coating of the ball plugs. The study of the parameters of nickel–phosphorus and [...] Read more.
The greatest losses during gas transportation occur in the elements of shut-off valves, the operating parameters of which, among other things, depend on the thickness and hardness of the protective coating of the ball plugs. The study of the parameters of nickel–phosphorus and chrome coatings on ball plugs of serially produced shut-off valves, including control of their thickness and hardness, was carried out. Based on the test results, deviations in the actual parameters of coatings from the requirements of technological documentation were revealed, the necessity of their complex control was substantiated, recommendations on the choice of methods and equipment were formulated, and the main provisions of the test methodology were developed. Full article
(This article belongs to the Section Inventions and Innovation in Biotechnology and Materials)
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<p>Dependence of coercive force of Ni-P alloy material comprising an increasing concentration of P [<a href="#B22-inventions-09-00078" class="html-bibr">22</a>].</p>
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<p>Microhardness (Vickers) of Ni-P coatings directly after deposition (1) and after heat treatment under optimal conditions (2) depending on the phosphorus content in the coating. The arrows show the increase in microhardness with heat treatment.</p>
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<p>Measurement of hardness (by Knoop) after heat treatment at different temperatures for one hour. Phosphorus content in the coating: 1–4%, 2–9% [<a href="#B22-inventions-09-00078" class="html-bibr">22</a>].</p>
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<p>Dependence of hardness of chromium coatings on the temperature of heat treatment [<a href="#B25-inventions-09-00078" class="html-bibr">25</a>].</p>
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<p>Sample No. 1 AD-136 2” for measurements and calibration.</p>
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<p>(<b>a</b>) One of a set of chrome plating thicknesses (matte); (<b>b</b>) Drawing of the part to be electroplated with chrome plating.</p>
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<p>Dependence of the obtained ADC code on the thickness of chrome coatings.</p>
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15 pages, 1872 KiB  
Article
Performance Assessment of Pneumatic-Driven Automatic Valves to Improve Pipeline Fault Detection Procedure by Fast Transient Tests
by Francesco Castellani, Caterina Capponi, Bruno Brunone, Matteo Vedovelli and Silvia Meniconi
Sensors 2024, 24(6), 1825; https://doi.org/10.3390/s24061825 - 12 Mar 2024
Cited by 1 | Viewed by 972
Abstract
The use of fast transients for fault detection in long transmission networks makes the generation of controlled transients crucial. In order to maximise the information that can be extracted from the measured pressure time history (pressure signal), the transients must meet certain requirements. [...] Read more.
The use of fast transients for fault detection in long transmission networks makes the generation of controlled transients crucial. In order to maximise the information that can be extracted from the measured pressure time history (pressure signal), the transients must meet certain requirements. In particular, the manoeuvre that generates the transient must be fast and repeatable, and must produce a pressure wave that is as sharp as possible, without spurious pressure oscillations. This implies the use of small-diameter valves and often pneumatically operated automatic valves. In the present work, experimental transient tests are carried out at the Water Engineering Laboratory (WEL) of the University of Perugia using a butterfly valve and a ball pneumatic-driven valve to generate pressure waves in a pressurised copper pipe. A camera is used to monitor the valve displacement, while the pressure is measured by a pressure transducer close to the downstream end of the pipe where the pneumatic valve is installed. The experimental data are analysed to characterise the valve performance and to compare the two geometries in terms of valve closing dynamics, the sharpness of the generated pressure wave and the stability of the pressure time history. The present work demonstrates how the proposed approach can be very effective in easily characterising the transient dynamics. Full article
(This article belongs to the Special Issue Sensors and Methods for Diagnostics and Early Fault Detection)
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<p>Sketch of the experimental setup (R = reservoir, PV = automatic pneumatic-driven valve (manoeuvre valve), MV = manual valve (regulation valve), C = air compressor, PT = pressure transducer and FIC = Fast Industrial Camera).</p>
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<p>Automatic pneumatic-driven butterfly valve (by FESTO Group, Esslingen, Germany) with the reference system in the open configuration.</p>
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<p>Schematic representation of the frames corresponding to the conditions before and at the end of the manoeuvre: (<b>a</b>) open position and (<b>b</b>) closed position.</p>
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<p>Schematic representation of the frames during the manoeuvre.</p>
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<p>Schematic representation of the overall closing process.</p>
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<p>Effect of the discharge, <math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math>, on the closing manoeuvre time history (<math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math> = 8 bar): (<b>a</b>) butterfly valve and (<b>b</b>) ball valve.</p>
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<p>Effect of the air pressure, <math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math>, on the closing manoeuvre time history (<math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math> = 0.09 L/s): (<b>a</b>) butterfly valve and (<b>b</b>) ball valve.</p>
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<p>Comparison of the time history of the valve opening degree for the two PVs (<math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math> = 0.09 L/s and <math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math> = 8 bar).</p>
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<p>Pressure signals acquired during transient tests carried out with the butterfly PV for the three chosen values of <math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math> and two values of <math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math>.</p>
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<p>Pressure signals acquired during transient tests carried out with the ball PV for the three chosen values of <math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math> and two values of <math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math>.</p>
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<p>Standard deviation, <math display="inline"><semantics> <mi>σ</mi> </semantics></math>, of the pressure signal during the copper pipe’s first characteristic time for manoeuvres made by (<b>a</b>) the butterfly PV and (<b>b</b>) the ball PV for the three chosen values of <math display="inline"><semantics> <msub> <mi>Q</mi> <mn>0</mn> </msub> </semantics></math> and two values of <math display="inline"><semantics> <msub> <mi>p</mi> <mrow> <mi>a</mi> <mi>i</mi> <mi>r</mi> </mrow> </msub> </semantics></math>.</p>
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21 pages, 17164 KiB  
Article
Transient and Dynamic Simulation of the Fluid Flow through Five-Way Electric Coolant Control Valve of a 100 kW Fuel Cell Vehicle by CFD with Moving Grid Technique
by Soo-Jin Jeong, Ji-hoon Kang, Seong-Joon Moon and Gum-su Lee
Actuators 2024, 13(3), 110; https://doi.org/10.3390/act13030110 - 11 Mar 2024
Cited by 1 | Viewed by 1814
Abstract
In order to maintain the performance of a fuel cell vehicle, it is essential to maintain a constant temperature of the stack. Therefore, it is very important to distribute the optimal coolant flow rate to each major component under very diverse and rapidly [...] Read more.
In order to maintain the performance of a fuel cell vehicle, it is essential to maintain a constant temperature of the stack. Therefore, it is very important to distribute the optimal coolant flow rate to each major component under very diverse and rapidly changing dynamic operating conditions. The part responsible for this is a five-way electric coolant valve. Therefore, this study aims to investigate transient dynamic flow characteristics of the fluid flow through a five-way electric coolant valve (PCCV: Penta-Control Coolant Valve). To achieve this goal, this paper attempts a three-dimensional dynamic simulation of the fluid flow through the valve using a commercial CFD solver with moving mesh technique to consider flow inertia and dynamic flow in the opening and closing stages of the ball valve rotating motion. The dynamic flow characteristics and the thermal mixing inside the PCCV ball valve during the opening and closing stages are analyzed. It was found that the discrepancies between dynamic and steady-state simulations are remarkable when fluxes with different levels of enthalpy and momentum flow into the PCCV, leading to strong flow interference and flow inertia, while the discrepancies are relatively small at low rotation speed and weak flow interference. Subsequently, the effect of the dynamic flow characteristics of the valve on the dynamic thermal mixing characteristics at two different ball valve rotation speeds and rotation directions are investigated. It was found that the dynamic flow and thermal mixing characteristics inside the PCCV are greatly affected by the rotation speed, rotation direction, and degree of flow interference between fluxes. It also helps design better coolant control strategies and improves the FCEV thermal management system. Full article
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<p>An example of a thermal management system for a fuel cell vehicle.</p>
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<p>Illustration of five-way electric coolant control valve concept for an integrated module cooling strategy. (<b>a</b>) Three-way valve cooling circuit; (<b>b</b>) five-way valve cooling circuit.</p>
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<p>Exploded view of five-way electric coolant control valve.</p>
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<p>Geometrical details of five-way electric coolant control valve and internal flow paths.</p>
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<p>CAD surface data and computational grid system of the PCCV. (<b>a</b>) CAD surface data; (<b>b</b>) computational grid system.</p>
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<p>The variable opening area of each port with respect to the ball valve rotating angle (deg).</p>
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<p>Temporal variation of the mass flow rate at the inlet face of the stack port for various rotation speeds and averaged discrepancies between transient dynamic flow analysis and steady-state analysis.</p>
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<p>Temporal variation of the mass flow rate at the inlet face of the COD heater port for various rotation speeds and averaged discrepancies between transient dynamic flow analysis and steady-state analysis.</p>
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<p>Temporal variation of the mass flow rate at the inlet face of the ion-filter port for various rotation speeds and averaged discrepancies between transient dynamic flow analysis and steady-state analysis.</p>
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<p>Temporal variation of the mass flow rate at the inlet face of the radiator port for various rotation speeds and averaged discrepancies between transient dynamic flow analysis and steady-state analysis.</p>
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<p>Cross-sectional view (@115 mm from bottom) of velocity distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 40 deg.</p>
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<p>Cross-sectional view (@50.6 mm from bottom) of velocity distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 40 deg.</p>
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<p>Cross-sectional view (@115 mm from bottom) of velocity distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 85 deg.</p>
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<p>Cross-sectional view (@50.6 mm from bottom) of velocity distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 85 deg.</p>
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<p>Temporal sequential isometric-views of particle streak lines in PCCV at ω = ±94 deg/s (Color was used to distinguish flux flowing from each port).</p>
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<p>Temporal variation of velocity in PCCV (<b>a</b>) stack port; (<b>b</b>) COD heater port; (<b>c</b>) ion-filter port; (<b>d</b>) radiator port.</p>
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<p>Cross-sectional view (@25.6 mm from bottom) of temperature distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 40 deg.</p>
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<p>Cross-sectional view (@25.6 mm from bottom) of temperature distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 85 deg.</p>
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<p>Cross-sectional view (@115 mm from bottom) of temperature distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 40 deg.</p>
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<p>Cross-sectional view (@115 mm from bottom) of temperature distribution at ω = ±94 deg/s and <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 85 deg.</p>
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<p>Comparison of temperature at the outlet between dynamic and steady-flow simulations for two different rotation speeds and angles at <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 40 deg.</p>
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<p>Comparison of temperature at the outlet between dynamic and steady-flow simulations for two different rotation speeds and angles at <math display="inline"><semantics> <mrow> <mi mathvariant="sans-serif">θ</mi> <mo>=</mo> </mrow> </semantics></math> 85 deg.</p>
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20 pages, 18484 KiB  
Article
Effect of Low-Temperature Plasma Carburization on Fretting Wear Behavior of AISI 316L Stainless Steel
by Lu Sun, Yuandong Li, Chi Cao, Guangli Bi and Xiaomei Luo
Coatings 2024, 14(2), 158; https://doi.org/10.3390/coatings14020158 - 25 Jan 2024
Cited by 3 | Viewed by 1465
Abstract
AISI 316L stainless steel has received considerable attention as a common material for key ball valve components; however, its properties cannot be improved through traditional phase transformation, and fretting wears the contact interface between valve parts. A carburized layer was prepared on the [...] Read more.
AISI 316L stainless steel has received considerable attention as a common material for key ball valve components; however, its properties cannot be improved through traditional phase transformation, and fretting wears the contact interface between valve parts. A carburized layer was prepared on the surface of AISI 316L stainless steel by using double-glow low-temperature plasma carburization technology. This study reveals the effect of double-glow low-temperature plasma carburization technology on the fretting wear mechanism of AISI 316L steel under different normal loads and displacements. The fretting wear behavior and energy dissipation of the AISI 316L steel and the carburized layer were studied on an SRV-V fretting friction and wear machine with ball–plane contact. The wear mark morphology was analyzed by using scanning electron microscopy (SEM), the phase structure of the carburized layer was characterized with X-ray diffractometry (XRD), and the wear profile and wear volume were evaluated with laser confocal microscopy. The carburized layer contains a single Sc phase, a uniform and dense structure, and a metallurgically combined matrix. After plasma carburizing, the sample exhibited a maximum surface hardness of 897 ± 18 HV0.2, which is approximately four times higher than that of the matrix (273 ± 33 HV0.2). Moreover, the surface roughness was approximately doubled. The wear depth, wear rate, and frictional dissipation energy coefficient of the carburized layer were significantly reduced by up to approximately an order of magnitude compared with the matrix, while the wear resistance and fretting wear stability of the carburized layer were significantly improved. Under different load conditions, the wear mechanism of the AISI 316L steel changed from adhesive wear and abrasive wear to adhesive wear, fatigue delamination, and abrasive wear. Meanwhile, the wear mechanism of the carburized layer changed from adhesive wear to adhesive wear and fatigue delamination, accompanied by a furrowing effect. Under variable displacement conditions, both the AISI 316L steel and carburized layer mainly exhibited adhesive wear and fatigue peeling. Oxygen elements accumulated in the wear marks of the AISI 316L steel and carburized layer, indicating oxidative wear. The fretting wear properties of the AISI 316L steel and carburized layer were determined using the coupled competition between mechanical factors and thermochemical factors. Low-temperature plasma carburization technology improved the stability of the fretting wear process and changed the fretting regime of the AISI 316L steel and could be considered as anti-wearing coatings of ball valves. Full article
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Figure 1
<p>(<b>a</b>) Cross-sectional SEM microstructure of the carburized layer, (<b>b</b>) cross-sectional metallographic microstructure of the carburized layer, (<b>c</b>) EDS patterns of the carburized layer, and (<b>d</b>) XRD patterns of plasma-carburized AISI 316L steel.</p>
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<p>Friction coefficient curves of AISI 316L steel and carburized layer under different (<b>a</b>) loads and (<b>b</b>) displacements.</p>
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<p>SEM images of wear marks of AISI 316L steel at (<b>a</b>) 30 N, (<b>c</b>) 50 N, and (<b>e</b>) 70 N. SEM images of wear marks of the carburized layer at (<b>b</b>) 30N, (<b>d</b>) 50N, and (<b>f</b>) 70N.</p>
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<p>SEM images of wear marks of AISI 316L steel under displacement of (<b>a</b>) 50 μm, (<b>c</b>) 75 μm, and (<b>e</b>) 100 μm. SEM images of wear marks of the carburized layer under displacement of (<b>b</b>) 50 μm, (<b>d</b>) 75 μm, and (<b>f</b>) 100 μm.</p>
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<p>Oxygen element distribution of AISI 316L steel under loads of (<b>a1</b>) 30 N, (<b>a2</b>) 50 N, and (<b>a3</b>) 70 N and displacements of (<b>c1</b>) 50 μm, (<b>c2</b>) 75 μm, and (<b>c3</b>) 100 μm. Oxygen element distribution of the carburized layer under loads of (<b>b1</b>) 30 N, (<b>b2</b>) 50 N, and (<b>b3</b>) 70 N and displacements of (<b>d1</b>) 50 μm, (<b>d2</b>) 75 μm, and (<b>d3</b>) 100 μm.</p>
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<p>OM images of wear marks of the GCr15 ball under loads of (<b>a1</b>) 30 N, (<b>a2</b>) 50 N, and (<b>a3</b>) 70 N and displacements of (<b>c1</b>) 50 μm, (<b>c2</b>) 75 μm, and (<b>c3</b>) 100 μm. OM images of wear marks of the GCr15 ball under loads of (<b>b1</b>) 30 N, (<b>b2</b>) 50 N, and (<b>b3</b>) 70 N and displacements of (<b>d1</b>) 50 μm, (<b>d2</b>) 75 μm, and (<b>d3</b>) 100 μm.</p>
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<p>Wear profiles of the AISI 316L steel and carburized layer under loads of (<b>a</b>) 30 N, (<b>b</b>) 50 N, and (<b>c</b>) 70 N and displacements of (<b>d</b>) 50 μm, (<b>e</b>) 75 μm, and (<b>f</b>) 100 μm.</p>
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<p>Wear profiles of the AISI 316L steel and carburized layer under loads of (<b>a</b>) 30 N, (<b>b</b>) 50 N, and (<b>c</b>) 70 N and displacements of (<b>d</b>) 50 μm, (<b>e</b>) 75 μm, and (<b>f</b>) 100 μm.</p>
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<p>Wear volume and wear rate of the untreated and carburized AISI 316L steel under different (<b>a</b>) loads and (<b>b</b>) displacements.</p>
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<p>Fretting wear process and mechanism of GCr15/PC and GCr15/316L at (<b>a</b>) initial stage, (<b>b</b>) wear stage, and (<b>c</b>) stability stage.</p>
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<p>(<b>a</b>) Simplified wear contours and (<b>b</b>) cutting plasticity ratios of AISI 316L steel and carburized layer.</p>
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<p>Frictional dissipative energy and friction dissipation energy coefficients of the untreated and carburized AISI 316L steel under different loads and displacements.</p>
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21 pages, 13554 KiB  
Article
A Bimodal Hydrostatic Actuator for Robotic Legs with Compliant Fast Motion and High Lifting Force
by Alex Lecavalier, Jeff Denis, Jean-Sébastien Plante and Alexandre Girard
Actuators 2023, 12(12), 452; https://doi.org/10.3390/act12120452 - 7 Dec 2023
Viewed by 2032
Abstract
Robotic legs, such as for lower-limb exoskeletons and prostheses, have bimodal operation: (1) within a task, like for walking (high speed and low force for the swing phase and low speed and higher force when the leg bears the weight of the system); [...] Read more.
Robotic legs, such as for lower-limb exoskeletons and prostheses, have bimodal operation: (1) within a task, like for walking (high speed and low force for the swing phase and low speed and higher force when the leg bears the weight of the system); (2) between tasks, like between walking and sit–stand motions. Sizing a traditional single-ratio actuation system for such extremum operations leads to oversized heavy electric motor and poor energy efficiency at low speeds. This paper explores a bimodal actuation concept where a hydrostatic transmission is dynamically reconfigured using custom motorized ball valves to suit the requirements of a robotic leg with a smaller and more efficient actuation system. First, this paper presents an analysis of the mass and efficiency advantages of the bimodal solution over a baseline solution, for three operating points: high-speed, high-force, and braking modes. Second, an experimental demonstration with a custom-built actuation system and a robotic leg test bench is presented. Control challenges regarding dynamic transition between modes are discussed and a control scheme solution is proposed and tested. The results show the following findings: (1) The actuator prototype can meet the requirements of a leg bimodal operation in terms of force, speed, and compliance while using smaller motors than a baseline solution. (2) The proposed operating principle and control schemes allow for smooth and fast mode transitions. (3) Motorized ball valves exhibit a good trade-off between size, speed, and flow restriction. (4) Motorized ball valves are a promising way to dynamically reconfigure a hydrostatic transmission while allowing energy to be dissipated. Full article
(This article belongs to the Special Issue Actuation Solutions for Wearable Robots)
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<p>Trade-offs of geared motors with a fixed reduction ratio: direct drive and lightly geared motors on the left and highly geared motors on the right.</p>
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<p>The three targeted operating points of the proposed multimodal design.</p>
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<p>Bimodal actuation principle of the proposed hydrostatic architecture. (<b>a</b>) High-speed mode; (<b>b</b>) high-force mode.</p>
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<p>Bimodal demonstration on a robotic knee: swing phase (high-speed phase), stance phase (high-force phase).</p>
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<p>Model of the proposed hydrostatic architecture.</p>
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<p>The baseline configuration used for analytical comparison.</p>
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<p>Predicted mass of the baseline (solid lines) and the two-speed (dashed lines) concepts. The middle curves are the analysis based on the nominal specifications. The left and right curves show the sensitivity of the mass when the high-speed mode specifications are changed.</p>
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<p>Efficiency comparison of the baseline configuration (solid black) with the proposed two-speed solution (dashed black). (<b>a</b>) High-speed mode; (<b>b</b>) high-force mode; (<b>c</b>) high-force mode.</p>
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<p>Mass mapping for aluminum motorized ball valves as a function of the bore diameter and 90° cycle time: (<b>a</b>) 3D view of the map; (<b>b</b>) 2D view of the map.</p>
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<p>Motorized valve unit prototype built with two commercial three-way ball valves and servo motors. (<b>a</b>) Actual prototype overview; (<b>b</b>) top and bottom cut views; (<b>c</b>) mass distribution.</p>
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<p>Hydrostatic actuator components layout.</p>
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<p>Bimodal system operating regions in terms of force and speed.</p>
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<p>Actuator control structure based on state machine and PID controllers.</p>
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<p>Contribution of leader cylinder (L1) on the total output speed (top) and theoretical dissipative force (bottom) when closing the valves.</p>
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<p>Comparison of three switching strategies for a downshift.</p>
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<p>State machine of the controller.</p>
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<p>Motion sequence for the downshift and upshift transition test. The labels (a) to (e) are described in the text.</p>
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<p>Results for the downshift and upshift transition test under load. The labels (a) to (e) are described in the text.</p>
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<p>Motion sequence for the landing test. The labels (a) to (c) are described in the text.</p>
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<p>Drop test sequence showcasing the brake capacity of the valve when positioned at 45°. The labels (a) to (c) are described in the text.</p>
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<p>Scaling laws found for the TQ Systems motor family used with extrapolation up to 100 <math display="inline"><semantics> <mrow> <mi mathvariant="normal">N</mi> <mi mathvariant="normal">m</mi> </mrow> </semantics></math>: mass (<math display="inline"><semantics> <mrow> <mi mathvariant="normal">k</mi> <mi mathvariant="normal">g</mi> </mrow> </semantics></math>) in black, nominal speed (<math display="inline"><semantics> <mrow> <msup> <mi mathvariant="normal">s</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>) in blue, rotor inertia (<math display="inline"><semantics> <mrow> <mi mathvariant="normal">k</mi> <mi mathvariant="normal">g</mi> <msup> <mi mathvariant="normal">m</mi> <mn>2</mn> </msup> </mrow> </semantics></math>) in red, Joule’s coefficient (<math display="inline"><semantics> <mrow> <mi mathvariant="normal">W</mi> <mo>/</mo> <mrow> <mi mathvariant="normal">N</mi> <msup> <mi mathvariant="normal">m</mi> <mn>2</mn> </msup> </mrow> </mrow> </semantics></math>) in green, and outside diameter (<math display="inline"><semantics> <mi mathvariant="normal">m</mi> </semantics></math>) in yellow.</p>
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