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Search Results (1,261)

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29 pages, 19650 KiB  
Article
A Comparative Study on Corrosion and Tribocorrosion Behaviors of NiCoCrAlY High-Entropy Alloy Coatings and M50 Steel
by Qunfeng Zeng, Jiahe Wang, Wei Liu and Naiming Lin
Coatings 2025, 15(1), 26; https://doi.org/10.3390/coatings15010026 (registering DOI) - 1 Jan 2025
Viewed by 240
Abstract
High-entropy alloy (HEA) coatings have attracted wide scientific attention in academic research and industrial innovation. In the present paper, the NiCoCrAlY HEA coatings are successfully synthesized on the surface of M50 steel to improve the corrosion resistance and tribocorrosion resistance of M50 steel [...] Read more.
High-entropy alloy (HEA) coatings have attracted wide scientific attention in academic research and industrial innovation. In the present paper, the NiCoCrAlY HEA coatings are successfully synthesized on the surface of M50 steel to improve the corrosion resistance and tribocorrosion resistance of M50 steel in salt-contaminated lubricating oil. The corrosion and tribocorrosion behaviors of M50 steel and NiCoCrAlY coatings are studied systemically under the same conditions. The experimental results show that NiCoCrAlY coatings have good, densified microstructures and improve effectively the corrosion resistance and tribocorrosion resistance of M50 steel because the protective passivation films and oxide films are formed on the surface of NiCoCrAlY coatings. NiCoCrAlY coatings have high corrosion potential, a low corrosion current density, and a corrosion rate that is comparable with M50 steel. The corrosion potential of M50 steel decreases and the corrosion current density increases with the increase in load due to wear-induced corrosion. The corrosion and tribocorrosion mechanisms of M50 steel and coatings are discussed in light of the experimental results. The wear mechanism of M50 steel is abrasive wear. It is accompanied by corrosion wear for M50 steel and oxidative wear for NiCoCrAlY coatings. Full article
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Figure 1
<p>XRD pattern of NiCoCrAlY coatings.</p>
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<p>Surface morphology and EDS of NiCoCrAlY coatings. (<b>a</b>) Surface topography of NiCoCrAlY coatings. (<b>b</b>) EDS of NiCoCrAlY coatings.</p>
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<p>SEM image of the cross-section and element distribution maps of NiCoCrAlY coatings.</p>
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<p>Surface morphology of the coatings under different conditions: (<b>a</b>) 1% emulsion, (<b>b</b>) 1% free water, (<b>c</b>) 2.5% emulsion, (<b>d</b>) 2.5% free water.</p>
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<p>CoF of HEA coatings under different experimental conditions: (<b>a</b>) 1% emulsion; (<b>b</b>) 2.5% emulsion.</p>
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<p>The wear rate of NiCoCrAlY under different experimental conditions.</p>
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<p>Polarization curves of M50 steel under different loads in artificial seawater.</p>
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<p>Electrochemical impedance spectroscopy of M50 steel in artificial seawater. (<b>a</b>) Nyquist. (<b>b</b>) Bode.</p>
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<p>Electrochemical impedance spectroscopy of M50 steel in artificial seawater. (<b>a</b>) Nyquist. (<b>b</b>) Bode.</p>
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<p>Equivalent circuit diagram.</p>
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<p>Polarization curve in artificial seawater of M50 steel and NiCoCrAlY coatings.</p>
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<p>The OCP and CoF of M50 steel and NiCoCrAlY coatings. (<b>a</b>) OCP. (<b>b</b>) CoF.</p>
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<p>The OCP and CoF of M50 steel and NiCoCrAlY coatings. (<b>a</b>) OCP. (<b>b</b>) CoF.</p>
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<p>The CoF and OCP of M50 steel and NiCoCrAlY coatings.</p>
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<p>Surface morphology after the polarization test. (<b>a</b>) NiCoCrAlY coatings. (<b>b</b>) M50 steel.</p>
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<p>Pitting pits of M50 steel. (<b>a</b>) M50 steel. (<b>b</b>) High multiples.</p>
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<p>Element distribution on the surface of the coatings after the static polarization test.</p>
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<p>Content of elements on M50 steel surface after the static polarization test.</p>
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<p>Surface images of M50 and NiCoCrAlY coatings after friction and wear. (<b>a</b>) M50 steel. (<b>b</b>) NiCoCrAlY coatings (low resolution).</p>
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<p>Surface images of M50 and NiCoCrAlY coatings after friction and wear. (<b>a</b>) M50 steel. (<b>b</b>) NiCoCrAlY coatings (high resolution).</p>
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<p>Surface element distribution at the wear mark on M50 steel.</p>
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<p>Surface element content in the abrasion mark on NiCoCrAlY coatings.</p>
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<p>Schematic diagram of the corrosion wear mechanism of NiCoCrAlY coatings.</p>
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13 pages, 1425 KiB  
Article
Design and Detection Performance of Metal Contaminant Sensor with Triple Coil Structure
by Changzhi Gu, Zuo Zhang, Shaoxuan Zhang, Hongliang Zhao, Shukui Hu, Wenbo Zhang, Chenzhao Bai, Hongpeng Zhang and Chenyong Wang
J. Mar. Sci. Eng. 2025, 13(1), 59; https://doi.org/10.3390/jmse13010059 - 31 Dec 2024
Viewed by 250
Abstract
In marine engineering, the daily management of mechanical equipment needs to ensure that the oil is normal. Oil plays the role of sealing, cooling, lubrication, and other functions in the equipment, and can also be used as hydraulic fluid to transfer energy. By [...] Read more.
In marine engineering, the daily management of mechanical equipment needs to ensure that the oil is normal. Oil plays the role of sealing, cooling, lubrication, and other functions in the equipment, and can also be used as hydraulic fluid to transfer energy. By analyzing the state of the oil, it is possible to obtain information about the operation of the equipment, such as judging the wear or failure of the equipment by detecting impurities in the oil. This paper proposes and designs a wireless triple-coil structure oil detection sensor for detecting metal particles in the oil circuit. The sensor consists of three coils placed concentrically with the same parameters. When the sensor detects metal particles in the oil, the ferromagnetic and non-ferromagnetic particles flowing through the sensor produce magnetization and eddy current effects, resulting in variable inductive signals that complete the detection of metal particles. This paper firstly explains the sensing principle of this triple coil sensor detection by formula derivation. Secondly, the simulation model of the sensor was established by using COMSOL 6.0 simulation software according to the scale of 1:1, and the magnetic field strength distribution law inside the coil of the triple-coil sensor was simulated. The experimental results showed that the sensor was able to detect iron particles at 73 µm and copper particles at 220 µm, moreover the obtained signal characteristics are obvious, with high detection sensitivity. The sensor is wireless and performs contactless detection of metal particles. This is important for the detection of metal particle contaminants in oil. Full article
(This article belongs to the Special Issue Advances in Recent Marine Engineering Technology)
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<p>Simulated sensor structure diagram.</p>
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<p>Equivalent circuit diagram of the oil condition monitoring sensor.</p>
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<p>Sensor simulation model.</p>
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<p>Simulation of the magnetic susceptibility of the three coils.</p>
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<p>Images of metal particles used in the experiment.</p>
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<p>Sensor detection system image.</p>
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<p>Inductance signal curve of iron particles at 0.835–0.86 MHZ frequency.</p>
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<p>Inductance signal curve of copper particles at 0.835–0.86 MHZ frequency.</p>
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<p>Simulation schematic of the three paths: (<b>a</b>) Path 1; (<b>b</b>) Path 2; (<b>c</b>) Path 3.</p>
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<p>Simulation schematic of the three paths: (<b>a</b>) Path 1; (<b>b</b>) Path 2; (<b>c</b>) Path 3.</p>
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<p>Signal of 600 μm iron particles.</p>
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<p>Signal of 600 μm copper particles.</p>
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<p>Signal curves of iron particles with particle sizes ranging from 73 μm to 700 μm.</p>
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<p>Signal curves of copper particles with particle sizes ranging from 220 μm to 800 μm.</p>
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22 pages, 19802 KiB  
Article
Analysis and Research on Oil Injection Lubrication of Variable Tooth Thickness Gear Based on CFD Method
by Huicheng Zhang, Yongping Liu and Qi Chen
Appl. Sci. 2025, 15(1), 297; https://doi.org/10.3390/app15010297 - 31 Dec 2024
Viewed by 229
Abstract
Variable tooth thickness gears have significant effects on the characteristics of the flow field inside the gearbox and the lubrication efficiency under high-speed operating conditions due to their complex parameters, such as tooth profile, cone angle, rotational speed, and oil injection speed. To [...] Read more.
Variable tooth thickness gears have significant effects on the characteristics of the flow field inside the gearbox and the lubrication efficiency under high-speed operating conditions due to their complex parameters, such as tooth profile, cone angle, rotational speed, and oil injection speed. To investigate the impact mechanism of oil injection velocity on the working flow field of high-speed variable tooth thickness gears under varying parameters, this paper establishes an oil injection lubrication model under high rotational speeds of variable tooth thickness gears, based on computational fluid dynamics (CFD) methods and the Volume of Fluid (VOF) model, combined with the dynamic mesh technique. This paper analyzes the lubrication issues at the initial oil injection moment of involute variable tooth thickness gears. By computing the lubricant distribution state at 0.1 s after the oil injection onset based on the stabilized flow field under no-oil-injection condition, discussions are conducted on the single-phase and two-phase flow fields within the gear casing at different cone angles and rotational speeds separately examining the flow states near the oil nozzle and the distribution patterns of lubricant at the meshing portions. The results indicate that, without oil injection, the pressure near the oil nozzle gradually increases with an increase in rotational speed and decreases with an increase in cone angle; at the initial oil injection moment, the lubricant volume fraction at the gear meshing portions gradually increases with an increase in rotational speed and rises with an increase in cone angle. Full article
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Figure 1
<p>Working pitch cone of variable tooth thickness gear.</p>
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<p>Fixed coordinate system.</p>
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<p>Three-dimensional model of involute variable tooth thickness gear: (1) driving wheel and (2) driven wheel.</p>
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<p>Internal structure of gearbox: (1) driving wheel, (2) fuel injector, (3) gear box, (4) driven wheel, and (5) oil outlet.</p>
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<p>Time step independence verification.</p>
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<p>Internal monitoring points of the gearbox: (1) middle section and (2) monitoring point.</p>
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<p>Pressure and velocity data under five different grid numbers.</p>
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<p>Final mesh model inside the gearbox.</p>
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<p>Gear-machining process.</p>
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<p>Optimized point cloud data model and 3D digital testing model.</p>
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<p>Three-dimensional comparison of involute variable tooth thickness gears.</p>
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<p>Involute variable tooth thickness gear transmission test bench.</p>
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<p>Transmission error at n = 10 rpm and T = 5 N·m.</p>
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<p>Transmission error at n = 10 rpm and T = 15 N·m.</p>
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<p>Observation surface schematic diagram: (1) observation plane 1, (2) observation plane 2, (3) point 1, (4) point 2, and (5) point 3.</p>
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<p>Cloud maps of gas field velocity at observation surface 1 and observation surface 2 under different gear pitch angles and rotational speeds.</p>
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<p>Cloud maps of gas field velocity at observation surface 1 and observation surface 2 under different gear pitch angles and rotational speeds.</p>
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<p>Gas field pressure cloud maps at observation surface 1 and observation surface 2 under different gear pitch cone angles and speed conditions.</p>
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<p>Gas field pressure cloud maps at observation surface 1 and observation surface 2 under different gear pitch cone angles and speed conditions.</p>
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<p>The law of the variation in meshing area pressure with gear speed under different gear pitch cone angle conditions.</p>
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<p>Distribution of volume fraction of gear lubricating oil under different cone angles and rotational speeds.</p>
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<p>Distribution of volume fraction of gear lubricating oil under different cone angles and rotational speeds.</p>
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<p>Curve graph of the variation in oil volume fraction with gear speed under different cone angle conditions.</p>
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<p>The relationship between oil volume fraction and injection speed at different gear speeds and cone angles.</p>
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10 pages, 1706 KiB  
Article
Wettability of Polar and Apolar Liquids on Metal Surfaces
by Mohanad Khairi, Zoltán Erdélyi and Peter Baumli
Metals 2025, 15(1), 23; https://doi.org/10.3390/met15010023 - 31 Dec 2024
Viewed by 230
Abstract
The wettability of metal surfaces by different oils and water is a multifaceted phenomenon with significant implications for industrial processes, including lubrication, corrosion protection, and fluid transport; an understanding of the process is essential for optimizing the performance and durability of metallic components. [...] Read more.
The wettability of metal surfaces by different oils and water is a multifaceted phenomenon with significant implications for industrial processes, including lubrication, corrosion protection, and fluid transport; an understanding of the process is essential for optimizing the performance and durability of metallic components. The intermolecular interactions between oil molecules and the metal surface primarily influence the wetting of a metal surface by different types of oil. This paper introduces the concept of oil wetting on metal surfaces, exploring the factors influencing wetting behavior, the characterization techniques employed to assess wetting properties, and the implications for different industrial processes. This work aims to ascertain the contact angle of oil on various metal surfaces and subsequently establish a relationship between this contact angle and the attributes of the substrate. This is achieved through using the sessile drop technique. The results indicate that the wettability of petroleum was better than the hydraulic oil we used on all types of substrates (for example, on Ag surface, Θ-petroleum = 11°, but Θ-hydraulic oil = 20°). Also, we observed that the cosine of the oil/metal contact angle increases with the increase in the atomic radius of the pure metal substrate, and Becker’s broken bond model proved this linear relation. We then contrast this behavior with the wetting characteristics of water and glycerin on the same metals using the same conditions. Full article
(This article belongs to the Special Issue Surface Modification and Coatings of Metallic Materials)
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<p>Measurement process.</p>
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<p>The silhouette of the droplets on the silver substrate ((<b>a</b>): glycerin droplet, (<b>b</b>): hydraulic oil droplet).</p>
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<p>Measured contact angles of the liquid (oil types and distilled water) and atomic radius of the substrate as a function of the substrate atomic number.</p>
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<p>Cosine of the contact angle of liquids as a function of the atomic radius parameter of the substrate.</p>
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22 pages, 3247 KiB  
Article
Experimental Identification of the Void Fraction in a Large Hydrodynamic Offset Halves Bearing
by Alexander Engels, Sören Wettmarshausen, Michael Stottrop, Thomas Hagemann, Christoph Weißbacher, Hubert Schwarze and Beate Bender
Lubricants 2025, 13(1), 7; https://doi.org/10.3390/lubricants13010007 (registering DOI) - 29 Dec 2024
Viewed by 314
Abstract
A common approach to optimising hydrodynamic journal bearings for power loss is to reduce the lubricant supply and direct the oil to specific bearing areas where it is needed to guarantee safe operation. This requires information on the processes in the gap and [...] Read more.
A common approach to optimising hydrodynamic journal bearings for power loss is to reduce the lubricant supply and direct the oil to specific bearing areas where it is needed to guarantee safe operation. This requires information on the processes in the gap and the surrounding pocket areas for both pre-design and simulation. In this paper, a system consisting of a total of eight cameras is used to determine the void fraction in deep grooves outside the lubricant film. The void fraction in the lubrication gap is determined using a novel method for the evaluation of two proximity measurements. While the variation of the deep groove void fraction is realised by a special oil supply and radially adjustable deep groove elements, the gap void fraction is adjusted by the oil supply in the lube oil pockets at the pad leading edges. On the one hand, the experimental investigations show that the void fraction of the deep groove areas has hardly any influence on the general operating behaviour. On the other hand, the void fraction in the lubrication gap can be measured quantitatively for the first time, and the operating point-dependent gas fractions can be visualised. It is also shown that gaseous cavitation is the main mechanism in partially filled regions of the lubrication gap. Full article
(This article belongs to the Special Issue Advances in Lubricated Bearings, 2nd Edition)
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Figure 1
<p>Test bearing design of OHB; (<b>a</b>): OHB in isometric view; (<b>b</b>): OHB in axial section from drive direction at <math display="inline"><semantics> <mrow> <msub> <mi>b</mi> <mi mathvariant="normal">b</mi> </msub> <mo>=</mo> <mn>97.5</mn> </mrow> </semantics></math> mm; (<b>c</b>): OHB in radial section.</p>
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<p>Test rig for large hydrodynamic journal bearings (side view); (<b>a</b>): test rig in radial half section; (<b>b</b>): enlarged view of the test bearing with measurement technology (radial section in the measuring plane of the distance sensors).</p>
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<p>Schematic view: radial section of the shaft in the sensor plane.</p>
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<p>Radially adjustable deep groove elements, which can be fed with lubricant; (<b>a</b>): initial design; (<b>b</b>): recessed deep groove; (<b>c</b>): recessed deep groove with deep groove element.</p>
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<p>Camera system for identifying the lower deep groove and ring groove void fraction; <span class="html-italic">1,4</span>: radial cameras in deep groove element; <span class="html-italic">2,3</span>: axial cameras for the ring groove void fraction.</p>
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<p>Comparison of the models for determining the void fraction.</p>
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<p>Comparison and dependencies of the distance sensors.</p>
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<p>Calibration functions of the capacitive distance sensor and the eddy current distance sensor.</p>
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<p>Relative permittivity as a function of temperature of different VG 32 lubricants.</p>
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<p>Deep groove void fraction @ <span class="html-italic">n</span> <math display="inline"><semantics> <mrow> <mo>=</mo> <mn>1500</mn> <mspace width="3.33333pt"/> <msup> <mi>min</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> <mo>,</mo> <mo> </mo> <mover> <mi>p</mi> <mo>¯</mo> </mover> <mo>=</mo> <mn>1.00</mn> <mspace width="3.33333pt"/> <mi>MPa</mi> <mo>,</mo> <mo> </mo> <msub> <mi>h</mi> <mi mathvariant="normal">P</mi> </msub> <mo>=</mo> <mn>45</mn> <mspace width="3.33333pt"/> <mi>mm</mi> <mo>,</mo> <mo> </mo> <msub> <mover accent="true"> <mi>V</mi> <mo>˙</mo> </mover> <mi mathvariant="normal">L</mi> </msub> <mo>=</mo> <mn>7.5</mn> <mspace width="3.33333pt"/> <mi mathvariant="normal">L</mi> <mspace width="0.166667em"/> <mi>·</mi> <mspace width="0.166667em"/> <msup> <mi mathvariant="normal">s</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>.</p>
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<p>Deep groove depth influence on <math display="inline"><semantics> <msub> <mi>h</mi> <mi>min</mi> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>P</mi> <mi>fric</mi> </msub> </semantics></math> at different operating points.</p>
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<p>Deep groove depth influence on operational safety and power loss at different operating points.</p>
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<p>Lubrication gap void fraction at low rotational speed and load (<b>a</b>) and high rotational speed and load (<b>b</b>) under standard oil supply and fully opened deep grooves.</p>
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<p>Lubrication gap pressure distribution (<b>a</b>) and void fraction (<b>b</b>) under standard oil supply and fully opened deep grooves.</p>
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<p>Lubrication gap void fraction @ <span class="html-italic">n</span> <math display="inline"><semantics> <mrow> <mo>=</mo> <mn>3000</mn> <mspace width="3.33333pt"/> <msup> <mi>min</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mover> <mi>p</mi> <mo>¯</mo> </mover> <mo>=</mo> <mn>1.00</mn> <mo>.</mo> <mo>.</mo> <mo>.</mo> <mn>4.50</mn> <mspace width="3.33333pt"/> <mi>MPa</mi> </mrow> </semantics></math> with standard oil supply and fully opened deep grooves.</p>
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<p>Lubrication gap void fraction @ <span class="html-italic">n</span> <math display="inline"><semantics> <mrow> <mo>=</mo> <mn>1000</mn> <mo>.</mo> <mo>.</mo> <mn>3600</mn> <mspace width="3.33333pt"/> <msup> <mi>min</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mover> <mi>p</mi> <mo>¯</mo> </mover> <mo>=</mo> <mn>1.00</mn> <mspace width="3.33333pt"/> <mi>MPa</mi> </mrow> </semantics></math> with standard oil supply at maximum deep groove depth.</p>
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<p>Lubrication gap void fraction @ <span class="html-italic">n</span> <math display="inline"><semantics> <mrow> <mo>=</mo> <mn>1500</mn> <mspace width="3.33333pt"/> <msup> <mi>min</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mover> <mi>p</mi> <mo>¯</mo> </mover> <mo>=</mo> <mn>1.00</mn> <mspace width="3.33333pt"/> <mi>MPa</mi> </mrow> </semantics></math> with varying <math display="inline"><semantics> <msub> <mover accent="true"> <mi>V</mi> <mo>˙</mo> </mover> <mi mathvariant="normal">P</mi> </msub> </semantics></math>.</p>
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<p>Lubrication gap void fraction @ <span class="html-italic">n</span> <math display="inline"><semantics> <mrow> <mo>=</mo> <mn>3000</mn> <mspace width="3.33333pt"/> <msup> <mi>min</mi> <mrow> <mo>−</mo> <mn>1</mn> </mrow> </msup> </mrow> </semantics></math>, <math display="inline"><semantics> <mrow> <mover> <mi>p</mi> <mo>¯</mo> </mover> <mo>=</mo> <mn>2.0</mn> <mspace width="3.33333pt"/> <mi>MPa</mi> </mrow> </semantics></math> with varying <math display="inline"><semantics> <msub> <mover accent="true"> <mi>V</mi> <mo>˙</mo> </mover> <mi mathvariant="normal">P</mi> </msub> </semantics></math>.</p>
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<p>Deep groove volume flow influence on <math display="inline"><semantics> <msub> <mi>h</mi> <mi>min</mi> </msub> </semantics></math> and <math display="inline"><semantics> <msub> <mi>P</mi> <mi>fric</mi> </msub> </semantics></math> at different operating points.</p>
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<p>Deep groove flow rate influence on maximum film pressure and temperature at different operating points.</p>
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24 pages, 7920 KiB  
Article
Investigation of the Tribological Effects of Nano-Sized Transition Metal Oxides on a Base Oil Containing Pour Point Depressant and Viscosity Modifier
by Ádám István Szabó, Kevin Szabó and Hajnalka Hargitai
ChemEngineering 2025, 9(1), 1; https://doi.org/10.3390/chemengineering9010001 - 27 Dec 2024
Viewed by 237
Abstract
This study investigates the tribological effects of nano-sized metal oxides (ZrO2, CuO, Y2O3 and TiO2) in Group III type base oil containing 0.3% pour point depressant (PPD) and 5% viscosity modifier (VM) to enhance friction and [...] Read more.
This study investigates the tribological effects of nano-sized metal oxides (ZrO2, CuO, Y2O3 and TiO2) in Group III type base oil containing 0.3% pour point depressant (PPD) and 5% viscosity modifier (VM) to enhance friction and wear performance. The homogenized lubricant samples with varying concentrations of oxide nanoparticles (0.1–0.5 wt%) on a linear oscillating tribometer performed static and dynamic frictional tests. Optical and confocal microscopy surface analysis evaluated the wear of the specimen, and SEM and EDX analyses characterized the wear tracks, nanoparticle distributions, and quantification. The cooperation between PPD and nanoparticles significantly improved friction and wear values; however, the worn surface suffered extensively from fatigue wear. The collaboration between VM and nanoparticles resulted in a nanoparticle-rich tribofilm on the contact surface, providing excellent wear resistance that protects the component while also favorably impacting friction reduction. This study found CuO reduced wear volume by 85% with PPD and 43% with VM at 0.5 wt%, while ZrO2 achieved 80% and 63% reductions, respectively. Y2O3 reduced wear volume by 82% with PPD, and TiO2 reduced friction by 20% with VM. These nanoparticles enhanced tribological performance at optimal concentrations, but high concentrations caused tribofilm instability, highlighting the need for precise optimization. Full article
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Figure 1
<p>Measurement of the dimensions required to determine the wear scar diameter of a worn ball according to the ISO 19291:2016 standard.</p>
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<p>3D scan of wear scar using a confocal microscope to calculate wear volume.</p>
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<p>The friction absolute integral results of the tested oxide nanoparticles are shown with a dashed line for the lubricant sample containing 5% viscosity modifier and a solid line for the lubricant sample containing 0.3% pour point depressant. All y-axes are truncated at 0.1.</p>
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<p>The static friction results of the tested oxide nanoparticles are shown with a dashed line for the lubricant sample containing a 5% viscosity modifier and a solid line for the lubricant sample containing 0.3% pour point depressant. All y-axes are truncated at 0.12.</p>
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<p>The mean wear scar diameter results of the balls tested with oxide nanoparticles are shown with a dashed line for the lubricant sample containing a 5% viscosity modifier and a solid line for the lubricant sample containing 0.3% pour point depressant. All y-axes are truncated at 400 µm.</p>
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<p>The wear volume results of the disks tested with oxide nanoparticles are shown with a dashed line for the lubricant sample containing a 5% viscosity modifier and a solid line for the lubricant sample containing 0.3% pour point depressant.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 0.3% pour point depressant + 0.5 wt% zirconia nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the zirconium element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 5% viscosity modifier + 0.5 wt% zirconia nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the zirconium element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 0.3% pour point depressant + 0.5 wt% cupric oxide nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the copper element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 5% viscosity modifier + 0.5 wt% cupric oxide nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the copper element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 0.3% pour point depressant + 0.5 wt% yttria nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the yttrium element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 5% viscosity modifier + 0.3 wt% yttria nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the yttrium element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 0.3% pour point depressant + 0.3 wt% titania nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the titanium element highlighted in yellow.</p>
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<p>SEM and EDX images of the worn surface of the disc specimens tribotested with Group III + 5% viscosity modifier + 0.3 wt% titania nanoadditive. The photos were taken from the wear track dead center (<b>left</b>) and stroke-middle section (<b>right</b>) areas with the horizontal sliding direction. In the <b>bottom</b> row are the results of the EDX analysis of the same images, with the location of the titanium element highlighted in yellow.</p>
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17 pages, 19581 KiB  
Article
Investigation of Anti-Friction Properties of MoS2 and SiO2 Nanolubricants Based on the Friction Pairs of Inconel 718 Superalloy and YG6 Carbide
by Lijie Ma, Fengnan Li, Shijie Ba, Zunyan Ma, Xinhui Mao, Qigao Feng and Kang Yang
Lubricants 2025, 13(1), 4; https://doi.org/10.3390/lubricants13010004 - 27 Dec 2024
Viewed by 275
Abstract
In order to improve the anti-friction property of common mineral oil and develop a high-performance lubricant, MoS2 and SiO2 nano-additives were individually dispersed into the 350SN mineral oil at various weight percentages to prepare nanolubricants. Then, the viscosity, wettability, and tribological [...] Read more.
In order to improve the anti-friction property of common mineral oil and develop a high-performance lubricant, MoS2 and SiO2 nano-additives were individually dispersed into the 350SN mineral oil at various weight percentages to prepare nanolubricants. Then, the viscosity, wettability, and tribological properties of the nanolubricants were measured and analyzed with a rotary viscometer, a contact angle measuring instrument, and a friction tester. Finally, the action mechanism of two nano-additives was explained based on the energy spectrum test results of the abrasion surface. The results show that MoS2 and SiO2 nano-additives could improve the viscosity of the base fluid and change its wettability, giving nanolubricants better anti-friction performance than the base fluid. Due to the difference in physical properties, SiO2 and MoS2 nanolubricants presented different friction reduction rules with the increase in nano-additive percentage. Under experimental conditions, SiO2 nanolubricants showed better anti-friction effects than MoS2 nanolubricants. When the SiO2 percentage was 10 wt% and 15 wt%, the maximum friction coefficient was reduced to 0.06, which was about 1/3 of that with the base fluid. In this case, the abrasion surface quality was significantly improved, and the abrasion trace size was about half that of the base fluid. The energy spectrum test results show that the action mechanism of the MoS2 nano-additive is the adsorption film effect and mending effect of nanoparticles, while the main action mechanism of the SiO2 nano-additive should be the polishing effect and rolling effect of nanoparticles. Full article
(This article belongs to the Special Issue Mechanical Tribology and Surface Technology)
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<p>SEM images of nano-additives: (<b>a</b>) SiO<sub>2</sub> (<b>b</b>) MoS<sub>2</sub>.</p>
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<p>Nanolubricants: (<b>a</b>) MoS<sub>2</sub>; (<b>b</b>) SiO<sub>2</sub>.</p>
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<p>Viscosity and wettability test equipment: (<b>a</b>) NDJ-5s rotary viscometer; (<b>b</b>) SDC-100 contact angle measuring instrument.</p>
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<p>Friction tester and the specimens: (<b>a</b>) MWF-500 friction tester; (<b>b</b>) lower and upper specimens.</p>
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<p>Friction surface of Inconel 718 specimen before and after polishing: (<b>a</b>) before polishing; (<b>b</b>) after polishing.</p>
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<p>Viscosities of nanolubricants. (<b>a</b>) MoS<sub>2</sub>; (<b>b</b>) SiO<sub>2</sub>.</p>
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<p>Contact angles of base fluid and nanolubricants.</p>
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<p>Friction coefficient curve under the lubrication of the base fluid.</p>
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<p>Friction coefficient curves under different nanolubricants: (<b>a</b>) MoS<sub>2</sub>; (<b>b</b>) SiO<sub>2</sub>.</p>
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<p>Abrasion surface of the lower specimen under the lubrication of the base fluid: (<b>a</b>) edge of the abrasion trace; (<b>b</b>) overall view of the abrasion trace; (<b>c</b>) middle of the abrasion trace.</p>
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<p>Abrasion surfaces of the Inconel 718 specimen under MoS<sub>2</sub> nanolubricants: (<b>a</b>) 5 wt%; (<b>b</b>) 10 wt%; (<b>c</b>) 15 wt%; (<b>d</b>) 20 wt%.</p>
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<p>Abrasion surfaces of the lower specimen under SiO<sub>2</sub> nanolubricants: (<b>a</b>) 5 wt%; (<b>b</b>) 10 wt%; (<b>c</b>) 15 wt%; (<b>d</b>) 20 wt%.</p>
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<p>Morphologies of abrasion traces under different lubricants: (<b>a</b>) base fluid; (<b>b</b>) 5 wt% MoS<sub>2</sub>; (<b>c</b>) 10 wt% MoS<sub>2</sub>; (<b>d</b>) 15 wt% MoS<sub>2</sub>; (<b>e</b>) 20 wt% MoS<sub>2</sub>; (<b>f</b>) 5 wt% SiO<sub>2</sub>; (<b>g</b>) 10 wt% SiO<sub>2</sub>; (<b>h</b>) 15 wt% SiO<sub>2</sub>; (<b>i</b>) 20 wt% SiO<sub>2</sub>.</p>
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<p>Measurement method and result of abrasion trace size: (<b>a</b>) measurement method; (<b>b</b>) abrasion trace size.</p>
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<p>Action mechanism of nano-additives: (<b>a</b>) adsorption film effect; (<b>b</b>) mending effect; (<b>c</b>) polishing effect; (<b>d</b>) rolling effect.</p>
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<p>Element content on the original surface and abrasion surfaces of the Inconel 718 specimen: (<b>a</b>) original surface; (<b>b</b>) abrasion surface under the base fluid; (<b>c</b>) smooth area of abrasion surface under 5 wt% MoS<sub>2</sub> nanolubricant; (<b>d</b>) severe wear area of abrasion surface under 5 wt% MoS<sub>2</sub> nanolubricant; (<b>e</b>) smooth area of abrasion surface under 5 wt% SiO<sub>2</sub> nanolubricant; (<b>f</b>) severe wear area of abrasion surface under 5 wt% SiO<sub>2</sub> nanolubricant.</p>
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20 pages, 15697 KiB  
Article
The Effect of the Addition of Silicon Dioxide Particles on the Tribological Performance of Vegetable Oils in HCT600X+Z/145Cr46 Steel Contacts in the Deep-Drawing Process
by Tomasz Trzepieciński, Krzysztof Szwajka, Marek Szewczyk, Joanna Zielińska-Szwajka, Ján Slota and Ľuboš Kaščák
Materials 2025, 18(1), 73; https://doi.org/10.3390/ma18010073 - 27 Dec 2024
Viewed by 296
Abstract
Friction is an unfavourable phenomenon in deep-drawing forming processes because it hinders the deformation processes and causes deterioration of the surface quality of drawpieces. One way to reduce the unfavourable effect of friction in deep-drawing processes is to use lubricants with the addition [...] Read more.
Friction is an unfavourable phenomenon in deep-drawing forming processes because it hinders the deformation processes and causes deterioration of the surface quality of drawpieces. One way to reduce the unfavourable effect of friction in deep-drawing processes is to use lubricants with the addition of hard particles. For this reason, this article presents the results of friction tests of dual-phase HCT600X+Z steel sheets using the flat die strip drawing test. Sunflower oil and rapeseed oil with the addition of 1, 5 and 10 wt.% of silicon dioxide (SiO2) particles were used as lubricants. Tests were also carried out in dry friction conditions and lubricated conditions using SiO2-modified oils and oils without the addition of particles, as a reference. Tests were carried out at different pressure values between 2 and 8 MPa. The effect of friction on the change in sheet surface roughness was also examined. For the entire range of pressures analysed, pure sunflower oil showed lower efficiency in reducing the coefficient of friction compared to pure rapeseed oil. In the pressure range of 4–8 MPa, the lubricants with 5 wt.% and 10 wt.% of particles were more effective in reducing friction than the biolubricant with the addition of 1 wt.% of SiO2. The lowest average roughness was observed for lubrication with sunflower oil containing 5 wt.% of particles. In relation to rapeseed oil, the addition of 10 wt.% of SiO2 provided a sheet surface with the lowest average roughness. Full article
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<p>(<b>a</b>) Surface topography and (<b>b</b>) material ratio curve of an HCT600X+Z steel sheet.</p>
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<p>(<b>a</b>) Scheme of the SDT, (<b>b</b>) model and (<b>c</b>) photograph of the SDT tribometer.</p>
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<p>Surface topography of countersamples and their basic surface roughness parameters.</p>
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<p>Schematic diagram of the test stand.</p>
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<p>The variation in the force parameters and CoF during testing of HCT600X+Z sheet metal under the following conditions: lubrication with sunflower oil, contact pressure of 4 MPa.</p>
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<p>SEM micrograph of SiO<sub>2</sub> particles.</p>
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<p>Effect of contact pressure on the CoF of HCT600X+Z steel sheets lubricated with sunflower oil.</p>
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<p>Effect of contact pressure on the CoF of HCT600X+Z steel sheets lubricated with rapeseed oil.</p>
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<p>Effect of the type of non-modified lubricant on the effectiveness of the lubrication.</p>
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<p>Effect of the addition of SiO<sub>2</sub> on the effectiveness of lubrication with sunflower oil.</p>
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<p>Effect of the addition of SiO<sub>2</sub> on the effectiveness of lubrication with rapeseed oil.</p>
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<p>Effect of lubrication conditions on the average roughness Sa for (<b>a</b>) sunflower and (<b>b</b>) rapeseed oil.</p>
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<p>SEM micrographs of the sheet surfaces after the friction tests under the following lubricated conditions: sunflower oil + SiO<sub>2</sub> (10 wt.%) and contact pressure (<b>a</b>) 4 MPa and (<b>b</b>) 8 MPa.</p>
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<p>Effect of lubrication conditions on the skewness Ssk for (<b>a</b>) sunflower and (<b>b</b>) rapeseed oils.</p>
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<p>SEM micrographs of the sheet surface after the friction tests under the following lubricated conditions: (<b>a</b>) dry friction, contact pressure 8 MPa and (<b>b</b>) rape seed oil (unmodified), contact pressure 8 MPa.</p>
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<p>SEM micrographs of the sheet surface after the friction tests under the following lubricated conditions: (<b>a</b>) rape seed oil + SiO<sub>2</sub> (1 wt.%), contact pressure 8 MPa and (<b>b</b>) rape seed oil + SiO<sub>2</sub> (5 wt.%), contact pressure 6 MPa.</p>
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<p>Effect of lubrication conditions on the kurtosis Sku for (<b>a</b>) sunflower and (<b>b</b>) rapeseed oils.</p>
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17 pages, 3930 KiB  
Article
Impact of Soil Type and Moisture Content on Microwave-Assisted Remediation of Hydrocarbon-Contaminated Soil
by Jun Xu, Songtao Liu and Chuanmin Chen
Sustainability 2025, 17(1), 101; https://doi.org/10.3390/su17010101 - 27 Dec 2024
Viewed by 348
Abstract
Volatile and semi-volatile compounds, such as petroleum hydrocarbons and equipment lubricating oils, often contaminate soil due to accidents, posing significant ecological and health risks. Traditional soil remediation methods, such as thermal desorption and bioremediation, are time-consuming and resource-intensive, prompting researchers to explore more [...] Read more.
Volatile and semi-volatile compounds, such as petroleum hydrocarbons and equipment lubricating oils, often contaminate soil due to accidents, posing significant ecological and health risks. Traditional soil remediation methods, such as thermal desorption and bioremediation, are time-consuming and resource-intensive, prompting researchers to explore more efficient alternatives. This study investigates the effectiveness of an in situ reactor for microwave-assisted soil remediation, specifically focusing on the impact of soil type and moisture content on pollutant removal efficiency. The reactor, designed to operate within a modified household microwave oven, provides direct microwave irradiation to the soil surface, enabling precise control of heating conditions. Experiments were conducted using soil samples of varying particle sizes and moisture levels under standardized conditions (1000 W microwave power, 2.45 GHz frequency). The results show that moisture content plays a critical role in pollutant removal efficiency, with an optimal moisture content of 10 wt % enhancing microwave absorption and energy transfer, thus improving pollutant recovery. In comparison with traditional resistive heating, microwave heating achieved a faster temperature rise and higher final temperatures, significantly improving pollutant removal efficiency in a shorter time frame. This study highlights the advantages of microwave heating, including its superior energy efficiency, faster pollutant volatilization, and the potential for optimized soil remediation in real-world applications. These findings provide valuable insights for the development of more sustainable and efficient soil remediation technologies. Full article
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<p>Schematic of microwave heating experimental setup.</p>
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<p>Soil temperature variation during microwave heating: (<b>a</b>) Temperature variations at different distances from the microwave source. (<b>b</b>) Temperature variation at 5 cm distance from the microwave source.</p>
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<p>Temperature variation during microwave heating of soils with different moisture contents.</p>
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<p>Relationship between soil moisture content and distance from the microwave heat source at different heating times. Subfigures: (<b>a</b>) 5 min, 6 cm; (<b>b</b>) 170 min, 6 cm; (<b>c</b>) 5 min, 30 cm; (<b>d</b>) 170 min, 30 cm.</p>
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<p>The relationship between the removal rate of soil pollutants with different moisture contents and heating times.</p>
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<p>Temperature variation during microwave heating of soils with different soil sizes.</p>
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<p>Relationship between soil size and distance from the microwave heat source at different heating times. Subfigures: (<b>a</b>) 5 min, 6 cm; (<b>b</b>) 170 min, 6 cm; (<b>c</b>) 5 min, 30 cm; (<b>d</b>) 170 min, 30 cm.</p>
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<p>Liquid recovery rate of soils of different sizes.</p>
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<p>Removal efficiency of medium sand-contaminated soil with different moisture contents after heating for 170 min.</p>
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<p>(<b>a</b>) Temperature variations at different heating methods. (<b>b</b>) Removal efficiency of soil contaminated with different heating methods after heating for 170 min.</p>
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17 pages, 4437 KiB  
Article
Fabrication of Polytetrafluoroethylene-Reinforced Fluorocarbon Composite Coatings and Tribological Properties Under Multi-Environment Working Conditions
by Changqing Xi, Bochao Zhang, Xiangdong Ye and Honghua Yan
Polymers 2024, 16(24), 3595; https://doi.org/10.3390/polym16243595 - 22 Dec 2024
Viewed by 478
Abstract
Currently, few studies have been conducted on the use of fluorocarbon resin (FEVE) and polytetrafluoroethylene (PTFE) as adhesive substrates and lubricating and anti-corrosion fillers, respectively, for the fabrication of PTFE-reinforced fluorocarbon composite coatings. In this paper, the tribological properties of polytetrafluoroethylene-reinforced fluorocarbon composite [...] Read more.
Currently, few studies have been conducted on the use of fluorocarbon resin (FEVE) and polytetrafluoroethylene (PTFE) as adhesive substrates and lubricating and anti-corrosion fillers, respectively, for the fabrication of PTFE-reinforced fluorocarbon composite coatings. In this paper, the tribological properties of polytetrafluoroethylene-reinforced fluorocarbon composite coatings were investigated through orthogonal tests under various operating conditions. The optimal configuration for coating preparation under dry friction and aqueous lubrication was thus obtained: the optimal filler particle size, mass ratio of FEVE to PTFE, spraying pressure, and curing agent content were 50 μm, 3:4.5, 0.3 MPa, and 0.3, respectively. Under oil lubrication, the corresponding optimal values were 5 μm, 3:4.5, 0.3 MPa, and 0.3, respectively. Tribological tests revealed that the best overall performance of the FEVE/PTFE coating was obtained when the mass ratio of FEVE to PTFE was 3:4.5, and the filler particle size also significantly affected the tribological properties under different environments, including the friction coefficients of the FEVE/50 μm-PTFE coating under both dry friction and aqueous lubrication, as well as the friction coefficient of the FEVE/5 μm-PTFE coating under oil lubrication. These coefficients were 0.067, 0.062, and 0.055, representing decreases of 86%, 92%, and 56%, respectively, compared to those of the pure FEVE coating under the same working conditions. This research was conducted with the goal of expanding the application of fluorocarbon coatings in the field of tribology. Full article
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<p>Molecular structure of FEVE.</p>
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<p>PTFE molecular structure.</p>
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<p>Multifunctional friction and wear tester.</p>
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<p>Schematic representation of the friction test principle.</p>
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<p>Adhesion topographies of different orthogonal test specimens. (<b>a</b>) Specimen no. 1. (<b>b</b>) Specimen no. 2. (<b>c</b>) Specimen no. 3. (<b>d</b>) Specimen no. 4. (<b>e</b>) Specimen no. 5. (<b>f</b>) Specimen no. 6. (<b>g</b>) Specimen no. 7. (<b>h</b>) Specimen no. 8. (<b>i</b>) Specimen no. 9.</p>
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<p>Variations in the coefficient of friction curves of different orthogonal test specimens. (<b>a</b>) Specimen no. 1. (<b>b</b>) Specimen no. 2. (<b>c</b>) Specimen no. 3. (<b>d</b>) Specimen no. 4. (<b>e</b>) Specimen no. 5. (<b>f</b>) Specimen no. 6. (<b>g</b>) Specimen no. 7. (<b>h</b>) Specimen no. 8. (<b>i</b>) Specimen no. 9.</p>
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<p>Variations in the coefficient of friction curves of different orthogonal test specimens. (<b>a</b>) Specimen no. 1. (<b>b</b>) Specimen no. 2. (<b>c</b>) Specimen no. 3. (<b>d</b>) Specimen no. 4. (<b>e</b>) Specimen no. 5. (<b>f</b>) Specimen no. 6. (<b>g</b>) Specimen no. 7. (<b>h</b>) Specimen no. 8. (<b>i</b>) Specimen no. 9.</p>
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<p>Plot of the mean values of levels for adhesion factors.</p>
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<p>Plot of the mean values of levels for friction factors.</p>
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<p>Friction coefficient variation curves of the composite coatings with different FEVE/PTFE mass ratios under dry friction.</p>
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<p>Friction coefficient variation curves of the composite coatings with different FEVE/PTFE mass ratios under water lubrication.</p>
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<p>Friction coefficient variation curves of the composite coatings with different FEVE/PTFE mass ratios under oil lubrication.</p>
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<p>Friction coefficient variation curves of the FEVE/5 μm-PTFE composite coating under different working conditions.</p>
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17 pages, 5039 KiB  
Article
Optimization of Parameters and Comparison of Detection Signals for Planar Coil Particle Detection Sensors with Different Core Materials
by Changzhi Gu, Chao Liu, Bo Liu, Wenbo Zhang, Chenzhao Bai, Chenyong Wang, Yuqing Sun and Hongpeng Zhang
Micromachines 2024, 15(12), 1520; https://doi.org/10.3390/mi15121520 - 20 Dec 2024
Viewed by 407
Abstract
The cleanliness of lubricating oil plays a key role in determining the operational health of mechanical systems, serving as a critical metric that delineates the extent of equipment wear. In this study, we present a magnetic-core-type planar coil particle detection sensor. The detection [...] Read more.
The cleanliness of lubricating oil plays a key role in determining the operational health of mechanical systems, serving as a critical metric that delineates the extent of equipment wear. In this study, we present a magnetic-core-type planar coil particle detection sensor. The detection accuracy and detection limit are improved by optimizing the magnetic field inside the sensor. The optimization of the magnetic field is achieved through the finite element simulation analysis of the coil and the magnetic core. First, the finite element simulation software COMSOL 6.0 is used to model the sensor in three dimensions (3D). Then, we study the distribution of the magnetic field under different coil radii, core conductivity levels, and other parameters. We obtain the sensor structure after optimizing the magnetic field. The sensor is made using experimental methods, and the iron particles and copper particles are detected. The results show that the lower limit of detection of iron particles can reach 46 μm, and the lower limit of detection of copper particles can reach 110 μm. Full article
(This article belongs to the Special Issue Micro/Nanostructures in Sensors and Actuators, 2nd Edition)
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<p>The coil’s magnetic core sensor.</p>
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<p>Schematic diagram of the eddy current effect.</p>
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<p>(<b>a</b>) 3D model of the sensor detection unit and (<b>b</b>) grid of the sensor detection unit.</p>
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<p>(<b>a</b>) Magnetic induction intensity distribution in the coil with magnetic cores of different lengths. (<b>b</b>) Comparison of flux density in the direction of channel length under different coil turns. (<b>c</b>) The change law for the coil inductance value with the size of the coil turns.</p>
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<p>(<b>a</b>) Comparison of flux density in the direction of channel length for different inner diameters of the coil. (<b>b</b>) Variation in coil inductance with the size of the coil’s inner diameter. (<b>c</b>) Comparison of flux density in the direction of channel length for different coil outer diameter sizes. (<b>d</b>) Variation in the coil inductance value with the coil outer diameter size. (<b>e</b>) Comparison of flux density in the direction of channel length under different coil thicknesses. (<b>f</b>) Variation in coil inductance with coil thickness.</p>
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<p>(<b>a</b>) Spatial magnetic field distribution of a single planar coil in a magnetic core with different conductivity levels. (<b>b</b>) Magnetic induction intensity distribution in the detection area under different conductivity levels in the magnetic core. (<b>c</b>) Spatial magnetic field distribution of a single planar coil in a magnetic core with different relative permeability levels. (<b>d</b>) Magnetic induction intensity distribution in the detection area under different relative permeability levels of the magnetic core.</p>
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<p>Oil metal particle detection system.</p>
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<p>(<b>a</b>) Comparison of 70 μm iron particle inductance detection results of magnetic core sensors of different materials. (<b>b</b>) Comparison of 130 μm copper particle inductance detection results of magnetic core sensors of different materials. (<b>c</b>) Comparison of 70 μm iron particle resistance detection results of magnetic core sensors of different materials. (<b>d</b>) Comparison of 130 μm copper particle resistance detection results of magnetic core sensors of different materials.</p>
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<p>Peak heights of inductance signal with different particle size; (<b>a</b>) iron particles; (<b>b</b>) copper particles.</p>
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<p>Lower detection limit of the inductance signal for (<b>a</b>) 46 µm iron particles; (<b>b</b>) 125 µm copper particles. The resistance detection floor level: (<b>c</b>) 59 µm iron particles and (<b>d</b>) 110 µm copper particles.</p>
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39 pages, 22737 KiB  
Article
Comparative Research in the Field of the Parametric Effect of Lubricant Cavitation Initiation and Development on Friction and Wear in Piston Ring and Cylinder Liner Assemblies
by Polychronis Dellis
Lubricants 2024, 12(12), 460; https://doi.org/10.3390/lubricants12120460 - 20 Dec 2024
Viewed by 522
Abstract
This research follows closely previous findings in flow characteristics and phenomena that take place in the piston ring and cylinder liner interface during motoring and firing engine operation, and also compares results between different optical engine set-ups. Cavitation visualisation in a simulating lubrication [...] Read more.
This research follows closely previous findings in flow characteristics and phenomena that take place in the piston ring and cylinder liner interface during motoring and firing engine operation, and also compares results between different optical engine set-ups. Cavitation visualisation in a simulating lubrication single-ring test rig and oil transport and cavitation visualisation in custom made cylinder assemblies of optical engines are the tools used to quantify the transport process under the piston ring and cylinder liner. Simplification of the interface is an essential technique that enhances the researcher’s confidence in results interpretation. Engine complexity and severe oil starvation are impeding the analysis of the experimental results. Visualisation experiments constitute an effective way to test various lubricant types and assess their overall performance characteristics, including their properties and cavitation behaviour. The repeatability of the visualisation method establishes the parametric study effects and offers valuable experimental results. As a further step towards the lubricant composition effect, a link between the lubricant formulation and the operating conditions could be established as the oil performance is assessed with a view to its transport behaviour. Image processing is used to quantify the impact of cavitation on piston ring lubrication in conjunction with varied operating and lubricant parameters. The characteristics of the lubricant and the working environment have an impact on these types of cavities. Viscosity, cavitation, oil film thickness (OFT), lubricant shear-thinning characteristics and friction are all linked. Full article
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<p>Simulating single-ring test rig: (<b>a</b>) schematic; (<b>b</b>) the capacitance sensor used for MOFT measurements; (<b>c</b>) the capacitance, friction sensors, piston specimen and the oil jets that flood the piston ring and liner interface with lubricant; (<b>d</b>) schematic of the miniature pressure transducer as fitted on the liner specimen.</p>
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<p>Modified Kubota engine block with fitted window section [<a href="#B13-lubricants-12-00460" class="html-bibr">13</a>].</p>
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<p>PSA spark ignition engine: (<b>a</b>) side view; (<b>b</b>) top view [<a href="#B13-lubricants-12-00460" class="html-bibr">13</a>].</p>
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<p>Toyota engine—window layout [<a href="#B17-lubricants-12-00460" class="html-bibr">17</a>].</p>
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<p>Lubricant transport mechanisms in the piston assembly of a fired automotive engine [<a href="#B35-lubricants-12-00460" class="html-bibr">35</a>].</p>
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<p>Lister–Petter engine modifications, experimental set-up and drawings: (<b>a</b>) Lister–Petter engine with modified block on the dynamometer; (<b>b</b>) liner drawing details; (<b>c</b>) liner and block 3-D drawings; (<b>d</b>) Lister–Petter piston; (<b>e</b>) window drawing details; (<b>f</b>) modified engine drawing details; (<b>g</b>) photo of fitted windows; (<b>h</b>) engine visualisation experimental set-up; (<b>i</b>) camera visualisation set-up; (<b>j</b>) viewing windows, optical fibre probe and pressure transducer fittings in the modified liner [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>,<a href="#B25-lubricants-12-00460" class="html-bibr">25</a>].</p>
Full article ">Figure 6 Cont.
<p>Lister–Petter engine modifications, experimental set-up and drawings: (<b>a</b>) Lister–Petter engine with modified block on the dynamometer; (<b>b</b>) liner drawing details; (<b>c</b>) liner and block 3-D drawings; (<b>d</b>) Lister–Petter piston; (<b>e</b>) window drawing details; (<b>f</b>) modified engine drawing details; (<b>g</b>) photo of fitted windows; (<b>h</b>) engine visualisation experimental set-up; (<b>i</b>) camera visualisation set-up; (<b>j</b>) viewing windows, optical fibre probe and pressure transducer fittings in the modified liner [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>,<a href="#B25-lubricants-12-00460" class="html-bibr">25</a>].</p>
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<p>Piston ring pack details for Lister–Petter PHW1 single-cylinder engine [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>The Ricardo HYDRA optical engine: (<b>a</b>) new cylinder design and cooling details; (<b>b</b>) cut-out; (<b>c</b>) custom made quartz visualisation windows; (<b>d</b>) engine side view [<a href="#B9-lubricants-12-00460" class="html-bibr">9</a>].</p>
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<p>Upstroke cavitation images from (<b>a</b>–<b>l</b>) 15° crank angle (CA) to 28.2° CA [<a href="#B23-lubricants-12-00460" class="html-bibr">23</a>].</p>
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<p>Downstroke cavitation images from 0° crank angle (CA) to 360° CA [<a href="#B23-lubricants-12-00460" class="html-bibr">23</a>].</p>
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<p>Imaging at different CAs for the simulating test rig with the respective oil film pressure readings and different speed tests at 1159 N/m load [<a href="#B4-lubricants-12-00460" class="html-bibr">4</a>,<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Imaging at different CAs for the simulating test rig with the respective oil film pressure readings and different load tests at 400 rpm [<a href="#B4-lubricants-12-00460" class="html-bibr">4</a>,<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>(<b>a</b>) Vaporous oil film pressure difference between upstroke and downstroke; (<b>b</b>) ring profile as measured by Talysurf surface profilometry [<a href="#B4-lubricants-12-00460" class="html-bibr">4</a>].</p>
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<p>Peak oil film pressure signals: (<b>a</b>) offset at different speeds; (<b>b</b>) different cavitation areas at different speeds; (<b>c</b>) cavitation reformation at different loads [<a href="#B27-lubricants-12-00460" class="html-bibr">27</a>].</p>
Full article ">Figure 14 Cont.
<p>Peak oil film pressure signals: (<b>a</b>) offset at different speeds; (<b>b</b>) different cavitation areas at different speeds; (<b>c</b>) cavitation reformation at different loads [<a href="#B27-lubricants-12-00460" class="html-bibr">27</a>].</p>
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<p>Effect of varying speed and load on (<b>a</b>) cavitation initiation points, different CAs; (<b>b</b>) number of string cavities at mid-stroke [<a href="#B7-lubricants-12-00460" class="html-bibr">7</a>].</p>
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<p>Possible cavitation stages for different test cases and location of fibre probe as it travels on top of the piston ring specimen and the cavities: (<b>a</b>) over a lubricant striation at cycle No 1 at 90° CA; (<b>b</b>) over a cavity at cycle No 2 at 90° CA; (<b>c</b>) over a mixed lubricant string cavity region at cycle No 3 at 90° CA [<a href="#B7-lubricants-12-00460" class="html-bibr">7</a>].</p>
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<p>The effect of different lubricants’ properties on friction force peaks at 300 r/min, 971 N/m load, 70 °C at TDC [<a href="#B26-lubricants-12-00460" class="html-bibr">26</a>].</p>
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<p>Focus on BDC MOFT measurements and squeeze film shift: (<b>a</b>) for different temperatures, oil 6E, 400 r/min and 1159 N/m load; (<b>b</b>) for different lubricants at 600 r/min, 1159 N/m load and high temperature of 70 °C [<a href="#B26-lubricants-12-00460" class="html-bibr">26</a>].</p>
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<p>Images taken from the top window at various crank angles. Forms of string cavities are strongly supported by the findings. Camera is fitted 11.17cm from TDC: (<b>a</b>) 576° CA exhaust stroke, cycle A; (<b>b</b>) 576° CA exhaust stroke, cycle B; (<b>c</b>) 576° CA exhaust stroke, cycle C; (<b>d</b>) 576° CA exhaust stroke, cycle D; (<b>e</b>) 576° CA exhaust stroke, cycle E [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Image taken from the top window at 608.40° CA, exhaust stroke, camera fitted 9.17 cm from top edge, showing (<b>a</b>) oil starvation and surface change on the piston ring; (<b>b</b>) oil spouts extending the second piston land [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Image of 475.20° CA expansion stroke, camera at 9.17 cm from top edge, string cavities’ formation on top compression ring [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Images of 615.24° CA exhaust stroke, camera at 9.17 cm from top edge, second compression ring at two different engine cycles: (<b>a</b>) cycle A; (<b>b</b>) cycle B [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Top window anti-thrust side at 255.24° CA compression stroke, camera at 8.67 cm from top edge: (<b>a</b>) irregular string-shaped cavities, cycle A; (<b>b</b>) appearance of oil droplets on piston ring bottom side clearance, cycle B; (<b>c</b>) more irregular cavitation shapes, cycle C; and (<b>d</b>) another irregular cavity shape, cycle D [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Top window anti-thrust side: (<b>a</b>) 218.34° CA compression stroke, camera at 11.67 cm from top edge—second compression ring; (<b>b</b>) 218.34° CA compression stroke, camera at 8.67 cm from top edge—top compression ring [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Images of 124.20° CA induction stroke, camera at 16.07 cm from top edge; (<b>a</b>–<b>c</b>) bubbles on the side clearance of the piston ring; (<b>d</b>) shapes resembling string cavity [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Oil mist on the piston skirt, using the highest magnification lens: (<b>a</b>) 18° CA induction stroke, camera at 9.07 cm from top edge; (<b>b</b>) 48.60° CA induction stroke, camera at 9.07 cm from top edge; (<b>c</b>) 142.20° CA induction stroke, camera at 16.07 cm from top edge [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Schematic of the possible cavitation stages on the Lister–Petter engine: (<b>A</b>) fern-shaped cavities; (<b>B</b>) irregular fern growth; (<b>C</b>) string cavities [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Window–liner profile measurements, Lister liner anti-thrust side: (<b>a</b>) upper window, upper side (TDC); (<b>b</b>) upper side of lower window and liner limit; (<b>c</b>) lower side of upper window; and (<b>d</b>) lower side of lower window (BDC) [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Window–liner profile measurements, Lister liner anti-thrust side: (<b>a</b>) upper window, upper side (TDC); (<b>b</b>) upper side of lower window and liner limit; (<b>c</b>) lower side of upper window; and (<b>d</b>) lower side of lower window (BDC) [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Cavitation string measurements, length and width as derived from imaging: (<b>a</b>) single-ring simulating test rig and (<b>b</b>) single-cylinder motored Lister–Petter engine [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>]. Orange measurements are the piston ring width and compression ring groove width, blue measurements are the strings’ length and green measurements the strings’ width.</p>
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<p>Oil mist appearance on the surface of the top compression ring: (<b>a</b>) 44.28° CA, induction stroke 3.67 cm from top (no sign); (<b>b</b>) 403.92° CA, expansion stroke 3.67 cm from top edge; (<b>c</b>) 403.92° CA, expansion stroke 3.67 cm from top edge; and (<b>d</b>) 403.92° CA, expansion stroke 3.67 cm from top edge [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>].</p>
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<p>Image of 254.88° CA compression stroke camera at 8.67 cm from top edge.</p>
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<p>Image of 255.24° CA compression stroke, camera at 8.67 cm from top edge, cycle A.</p>
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<p>Image of 255.24° CA compression stroke, camera at 8.67 cm from top edge, cycle B.</p>
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<p>Image of 255.24° CA compression stroke, camera at 8.67 cm from top edge, cycle C.</p>
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<p>Cavities on compression ring upstroke: (<b>a</b>) at 30 °C and (<b>b</b>) at 40 °C, 800 rpm [<a href="#B9-lubricants-12-00460" class="html-bibr">9</a>]. Red highlighted area shows the cavitation area that covers the piston-ring and is calculated by the algorithm. Blue arrow shows upstroke piston movement.</p>
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<p>Cavitation images on top compression ring of the HYDRA engine motored tests during compression stroke, upstroke at 70 °C, at different speeds; (<b>a</b>) 208 r/min, (<b>b</b>) 800 r/min, (<b>c</b>) 1000 r/min; (<b>d</b>) 2000 r/min [<a href="#B9-lubricants-12-00460" class="html-bibr">9</a>]. Red highlighted area shows the cavitation area that covers the piston-ring and is calculated by the algorithm.</p>
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<p>High-pressure gasses act as a medium of the lubricant transport through the ring gaps towards the engine sump during motored tests: (<b>a</b>) 1000 rpm, 70 °C, 6° CA after TDC; (<b>b</b>) 1000 rpm, 70 °C, 6° CA after TDC; (<b>c</b>) 1000 rpm, 70 °C, 12° CA after TDC, higher magnification [<a href="#B8-lubricants-12-00460" class="html-bibr">8</a>]. Blue arrow shows downstroke piston movement and dotted red arrows show lubricant transport pathways towards the engine sump.</p>
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<p>Oil pumping at the second land [<a href="#B5-lubricants-12-00460" class="html-bibr">5</a>]. Black arrows show lubricant pumping process from ring side clearances in the top image as piston moves upstroke and in the bottom image as piston moves downstroke. The orange arrow shows transition from upstroke to downstroke.</p>
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14 pages, 11976 KiB  
Article
Tribological Characteristics of Biolubricant Obtained by Transesterification of Grape Seed Oil
by Thawan Fonseca Silva, Maria Marliete Fernandes de Melo Neta, Paulo Roberto Campos Flexa Ribeiro Filho, Francisco Murilo Tavares de Luna and Célio Loureiro Cavalcante
Lubricants 2024, 12(12), 459; https://doi.org/10.3390/lubricants12120459 - 20 Dec 2024
Viewed by 461
Abstract
Research on and the development of bio-based lubricants as alternatives to mineral-based lubricants have been encouraged worldwide owing to environmental concerns and the possible depletion of oil reserves. This study explored the use of grape seed oil (GSO), a byproduct of wine production, [...] Read more.
Research on and the development of bio-based lubricants as alternatives to mineral-based lubricants have been encouraged worldwide owing to environmental concerns and the possible depletion of oil reserves. This study explored the use of grape seed oil (GSO), a byproduct of wine production, as a raw material for biolubricant synthesis. GSO contains a triglyceride molecule rich in unsaturated fatty acids, which is ideal for obtaining biolubricants. This study addresses the technical challenges of converting GSO into a lubricant by synthesizing methyl esters (FAME) via transesterification with 2-ethylhexanol to produce a biolubricant (BL) sample. The obtained products were characterized using Fourier-transform infrared spectroscopy and nuclear magnetic resonance spectroscopy to confirm the conversion of the molecules. The density, kinematic viscosity, and viscosity index were determined using the parameters established by ASTM. The tribological characteristics of BL were evaluated using a four-ball tribometer configuration. BL exhibited physicochemical characteristics comparable with those of an ISO VG 10 lubricant, a friction coefficient (FC) 40.82% lower than that of a hydrotreated mineral oil sample, and a smoother wear surface. These results indicate that the polarity of the ester functional group was efficient in producing a protective film on metal surfaces. Full article
(This article belongs to the Special Issue Tribological Properties of Biolubricants)
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<p>Synthetic route used to obtain methyl esters (FAME) from grape seed oil (GSO).</p>
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<p>Experimental setup for synthesis of bio-based lubricants.</p>
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<p>Synthetic route to obtain biolubricants (BL) from transesterification of FAME.</p>
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<p>Four-ball test configuration.</p>
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<p>FTIR spectra of GSO, FAME, and BL samples.</p>
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<p><sup>1</sup>H NMR spectra of (<b>a</b>) GSO, (<b>b</b>) FAME, and (<b>c</b>) BL samples.</p>
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<p>FC and WSD values of FAME, BL, and HMO after tribological test. <span class="html-italic">p</span> &lt; 0.05. Different letters indicate significant differences between WSDs.</p>
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<p>Sketches of the lubrication mechanisms of FAME, BL, and HMO at the friction interface. (<b>a</b>) The initial formation of the lubricating film of the bio-based samples (FAME and BL). (<b>b</b>) The rupture of unsaturated bonds of the bio-based samples (FAME and BL) and (<b>c</b>) HMO lubricating film.</p>
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27 pages, 3744 KiB  
Article
A Comprehensive Study on Physicochemical Properties of Fatty Acid Esters Derived from Different Vegetable Oils and Alcohols and Their Potential Application
by Anton L. Esipovich, Evgeny A. Kanakov, Tatyana A. Charykova, Ksenia V. Otopkova, Mikhail A. Smirnov, Yulia A. Mityukova and Artem S. Belousov
Energies 2024, 17(24), 6407; https://doi.org/10.3390/en17246407 - 19 Dec 2024
Viewed by 434
Abstract
This study is related to producing a set of fatty acid esters from different vegetable oils and C1–C12 alcohols. A total of 66 products were synthesized. The obtained esters were characterized by fatty acid composition, density, viscosity, saponification value, acid value, iodine value, [...] Read more.
This study is related to producing a set of fatty acid esters from different vegetable oils and C1–C12 alcohols. A total of 66 products were synthesized. The obtained esters were characterized by fatty acid composition, density, viscosity, saponification value, acid value, iodine value, low-temperature properties, and oxidative stability. It was established that the fatty acid composition, as well as alcohol, used has a significant impact on esters properties. Comparing physicochemical properties of fatty acid esters with existing standards and specifications, it was proposed to use esters for different industrial applications. In particular, rapeseed oil fatty acid methyl esters are an ideal candidate for application as biodiesel, while transesterification of soybean oil, sunflower oil, rapeseed oil, and coconut oil with higher alcohols led to products with promising properties as bio-lubricants. Castor oil alkyl esters could potentially be utilized as base oils due to their excellent viscosity and low-temperature properties. Full article
(This article belongs to the Section I1: Fuel)
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<p>Density of FAEs at 15 °C.</p>
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<p>Kinematic viscosity of FAEs at (<b>a</b>) 40 °C and (<b>b</b>) 100 °C.</p>
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<p>Cold filter plugging point (<b>a</b>) and cloud point (<b>b</b>) of FAEs.</p>
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<p>Effect of the amount of C16–C18 saturated esters on pour point of (<b>a</b>) methyl esters, (<b>b</b>) ethyl esters, (<b>c</b>) <span class="html-italic">n</span>-propyl esters, and (<b>d</b>) <span class="html-italic">n</span>-butyl esters.</p>
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<p>Effect of the amount of C16–C18 saturated esters on pour point of (<b>a</b>) <span class="html-italic">n</span>-hexyl esters, (<b>b</b>) <span class="html-italic">n</span>-octyl esters, (<b>c</b>) <span class="html-italic">n</span>-decyl esters, and (<b>d</b>) <span class="html-italic">n</span>-dodecyl esters.</p>
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<p>Effect of the amount of C16–C18 saturated esters on pour point of (<b>a</b>) isopropyl esters, (<b>b</b>) isobutyl esters, and (<b>c</b>) 2-ethylhexyl esters.</p>
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<p>Effect of saponification value on (<b>a</b>) flash point and (<b>b</b>) fire point of FAEs (data from <a href="#energies-17-06407-t003" class="html-table">Table 3</a>, <a href="#energies-17-06407-t007" class="html-table">Table 7</a>, and <a href="#energies-17-06407-t008" class="html-table">Table 8</a>).</p>
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<p>Relationship between oxidative stability and iodine value for (<b>a</b>) methyl esters and (<b>b</b>) ethyl esters (data from <a href="#energies-17-06407-t003" class="html-table">Table 3</a> and <a href="#energies-17-06407-t010" class="html-table">Table 10</a>).</p>
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20 pages, 18907 KiB  
Article
From Experimentation to Optimization: Surface Micro-Texturing for Low-Friction and Durable PTFE–Steel Interfaces Under Full Film Lubrication
by Risheng Long, Jincheng Hou, Yimin Zhang, Qingyu Shang, Chi Ma, Florian Pape and Max Marian
Polymers 2024, 16(24), 3505; https://doi.org/10.3390/polym16243505 - 17 Dec 2024
Viewed by 511
Abstract
To enhance the sliding tribological performance between PTFE and 40#steel (AISI 1040) under full film lubrication conditions, laser surface texturing (LST) technology was employed to prepare micro-dimples on the contact surfaces of 40# steel discs. The Box–Behnken design response surface methodology (BBD-RSM) was [...] Read more.
To enhance the sliding tribological performance between PTFE and 40#steel (AISI 1040) under full film lubrication conditions, laser surface texturing (LST) technology was employed to prepare micro-dimples on the contact surfaces of 40# steel discs. The Box–Behnken design response surface methodology (BBD-RSM) was applied to optimize the micro-dimple parameters. Coefficients of friction (COFs), wear losses and worn contact surfaces of the PTFE–40# steel tribo-pairs were researched through repeated wear tests, as lubricated with sufficient anti-wear hydraulic oil. The influencing mechanism of micro-dimples on the tribological behavior of tribo-pairs was also discussed. The results proved that micro-dimples can significantly improve the tribological properties of PTFE–40#steel tribo-pairs. The deviation between the final obtained average COF and the prediction by the BBD-RSM regression model was only 0.0023. Following optimization, the average COF of the PTFE–40# steel tribo-pair was reduced by 39.34% compared to the smooth reference. The wear losses of the PTFE ring and 40# steel disc decreased by 91.8% and 30.3%, respectively. This study would offer a valuable reference for the optimal design of key seals used in hydraulic cylinders. Full article
(This article belongs to the Section Polymer Applications)
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<p>PTFE–40# steel tribo-pair and laser marking system. (<b>a</b>) Photos of the steel disc and upper counter rings (PTFE); (<b>b</b>) Section view of the lower sample (40# steel disc); (<b>c</b>) Photo of laser marking machine; (<b>d</b>) Section view of the upper sample (PTFE ring); (<b>e</b>) Textured surface of the 40#steel disc before re-polishing and the angle between two adjacent sets of micro-dimples in circumference.</p>
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<p>Vertical universal tribological test rig. (<b>a</b>) Photo of the MMW-1A vertical universal tribo-meter; (<b>b</b>) Photo of the fixtures used; (<b>c</b>) Section view of the fixtures: ① upper fixture; ② upper sample (PTFE ring); ③ lower sample (40# steel disc); ④ oil deflector; ⑤ lower fixture; ⑥ loading flange.</p>
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<p>COF data of different groups as the PTFE rings were tested against the 40# steel discs: (<b>a</b>) COF curves of T1–T4; (<b>b</b>) COF curves of R1–R4; (<b>c</b>) COF curves of X1–X4; (<b>d</b>) COF curves of X5-1 to X5-5; (<b>e</b>) Average COFs of 17 groups.</p>
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<p>Representative worn surfaces of the PTFE rings and wear losses of different groups after wear tests. (<b>a</b>) Worn surfaces of the PTFE rings after ultrasonic cleaning. (<b>b</b>) Mass losses of the PTFE rings and 40# steel discs: (<b>b1</b>) mass losses of T1–T4; (<b>b2</b>) mass losses of R1–R4; (<b>b3</b>) mass losses of X1–X4; (<b>b4</b>) mass losses of X5-1–X5-5.</p>
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<p>Representative worn surfaces of the 40# steel discs of different groups after wear tests and the FTIR curve of the PTFE transfer film. (<b>a</b>) Worn surfaces of the 40# steel discs after ultrasonic cleaning. (<b>b</b>) Typical infrared spectral characteristics of the PTFE debris collected from the transfer film on the contact surface of the 40# steel disc. (<b>c</b>) Section view of one black spot on the worn surface of the steel disc of the CT group.</p>
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<p>Representative 3D worn morphologies (with an enlargement of 2000% in the height direction) of the PTFE–40# steel tribo-pairs (T1, T3, T4, R1, X3, X5-4) after ultrasonic cleaning. (<b>a</b>) PTFE rings; (<b>b</b>) 40# steel discs.</p>
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<p>Response surfaces of the interaction among three factors (<span class="html-italic">D</span>, <span class="html-italic">P</span>, <span class="html-italic">H</span>) on the average COFs of the PTFE–40# steel tribo-pairs. (<b>a</b>) Response surface among average COF, <span class="html-italic">P</span> and <span class="html-italic">H</span>; (<b>b</b>) Response surface among average COF, <span class="html-italic">D</span> and <span class="html-italic">P</span>; (<b>c</b>) Response surface among average COF, <span class="html-italic">D</span> and <span class="html-italic">H</span>.</p>
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<p>COF curves and wear losses of three groups (OT, LT and CT). (<b>a</b>) COF curves and average COF lines of OT, LT and CT; (<b>b</b>) Wear losses of OT, LT and CT.</p>
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<p>Representative worn surfaces and 3D morphologies of the PTFE rings of OT, LT and CT after ultrasonic cleaning. (<b>a</b>) OT; (<b>b</b>) LT; (<b>c</b>) CT.</p>
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<p>Representative worn surfaces and 3D morphologies of the 40# steel discs of OT, LT and CT after ultrasonic cleaning. (<b>a</b>) OT; (<b>b</b>) LT; (<b>c</b>) CT.</p>
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<p>Influence mechanism of micro-dimples on the tribological performance of the PTFE–40# steel tribo-pair as lubricated with sufficient anti-wear hydraulic oil. (<b>a</b>) PTFE–40# steel tribo-pair and transfer film: (<b>a1</b>) section view of PTFE–40# steel tribo-pair; (<b>a2</b>) top view of PTFE–40# steel tribo-pair; (<b>a3</b>) transfer film left on the surface. (<b>b</b>) Micro-eddies in micro-dimples and the debris migration: (<b>b1</b>) influence of micro-eddies on the load-carrying capacity along the circumference; (<b>b2</b>) migration of wear debris along the radius direction. (<b>c</b>) Cavitation phenomenon and its formation mechanism: (<b>c1</b>) image of black spots; (<b>c2</b>) formation mechanism of cavitation.</p>
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