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13 pages, 4907 KiB  
Article
Tribological Comparison of Coatings Produced by PVD Sputtering for Application on Combustion Piston Rings
by Ney Francisco Ferreira, Filipe Fernandes, Patric Daniel Neis, Jean Carlos Poletto, Talha Bin Yaqub, Albano Cavaleiro, Luis Vilhena and Amilcar Ramalho
Coatings 2024, 14(9), 1109; https://doi.org/10.3390/coatings14091109 - 2 Sep 2024
Viewed by 457
Abstract
This article compares the tribological performance of coatings produced by PVD sputtering. Transition metal dichalcogenide (TMD) coatings doped with carbon (WSC and MoSeC) and nitrogen (WSN and MoSeN) and a conventional diamond-like carbon (DLC) coating are compared. The tribological evaluation was oriented towards [...] Read more.
This article compares the tribological performance of coatings produced by PVD sputtering. Transition metal dichalcogenide (TMD) coatings doped with carbon (WSC and MoSeC) and nitrogen (WSN and MoSeN) and a conventional diamond-like carbon (DLC) coating are compared. The tribological evaluation was oriented towards the use of coatings on piston rings. Block-on-ring tests in a condition lubricated with an additive-free polyalphaolefin (PAO 8) and at temperatures of 30, 60, and 100 °C were carried out to evaluate the coatings in boundary lubrication conditions. A load scanner test was used to evaluate dry friction and scuffing propensity. In addition to WSN, all other TMD coatings (WSC, MoSeC, and MoSeN) exhibited lower friction than DLC in dry and lubricated conditions. The study reveals that WSC, among TMD coatings, offers promising results, with significantly lower friction levels than DLC, while demonstrating reduced wear and a lower risk of metal adhesion. These findings suggest that WSC may be a viable alternative to DLC in piston rings, with potential benefits for reducing fuel consumption and increasing engine durability. Full article
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Figure 1

Figure 1
<p>Representative schemes/illustrations of the (<b>a</b>) load scanner (LS) and (<b>b</b>) block-on-ring (BoR) tests.</p>
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<p>Illustration of the methodology used to estimate the average volume loss V (in mm<sup>3</sup>) in the wear scars: (<b>a</b>) each wear scar is captured under an optical microscope; (<b>b</b>) the image is binarized to a black and white image using code 1; (<b>c</b>) code 2 determines the width of the wear scar along the length of the wear mark and calculates the volume (this figure shows a wear mark in MoSeN, tested at 20 °C).</p>
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<p>Friction coefficient measured in the LS tests for all coatings. (<b>a</b>) Friction coefficient as a function of sliding distance and applied normal force; (<b>b</b>) average value between 2 and 8 mm (normal load: 11 to 45 N; average contact pressure: 1.02 to 1.65 GPa).</p>
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<p>Detail of friction coefficient and wear obtained for the DLC coating in the LS test. (<b>a</b>) Coefficient of friction as a function of distance; (<b>b</b>) worn track seen via scanning electron microscopy (SEM); (<b>c</b>) worn track seen via digital optical microscopy; (<b>d</b>) wear scar on the steel ball.</p>
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<p>Wear analysis of DLC coating. (<b>a</b>) Scanning electron microscopy; (<b>b</b>) detail emphasizing adhered material; (<b>c</b>) chromium map derived from energy-dispersive spectroscopy (EDS); (<b>d</b>) iron map derived from EDS.</p>
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<p>Coefficients of friction obtained in the BoR tests. (<b>a</b>) Coefficients of friction at 20, 60, and 100 °C; (<b>b</b>) mean CoF, considering all three temperatures.</p>
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<p>Wear rate results measured in the BoR tests. (<b>a</b>) Wear rates at 20, 60, and 100 °C, (<b>b</b>) mean wear rate.</p>
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<p>Wear analysis showing the rupture of the MoSeN coating (test condition: 100 °C). (<b>a</b>) Image acquired using scanning electron microscopy (SEM), showing the region analyzed by energy dispersive spectroscopy (EDS). (<b>b</b>) Main elements of the coating (Mo and Se) identified by EDS. (<b>c</b>) Substrate and interlayer elements (Fe and Cr) identified by EDS. (<b>d</b>) Spectrum of elements identified by EDS.</p>
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<p>Wear analysis showing the rupture of the MoSeC coating (test condition: 100 °C). (<b>a</b>) Image acquired using scanning electron microscopy (SEM), showing the region analyzed by energy dispersive spectroscopy (EDS). (<b>b</b>) Main elements of the coating (Mo and Se) identified by EDS. (<b>c</b>) Substrate and interlayer elements (Fe and Cr) identified by EDS. (<b>d</b>) Spectrum of elements identified by EDS.</p>
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<p>Wear and coefficient of friction obtained in the BoR test: (<b>a</b>) all coatings; (<b>b</b>) DLC and WSC.</p>
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23 pages, 5531 KiB  
Article
Effect of Thickener Type on Change the Tribological and Rheological Characteristics of Vegetable Lubricants
by Rafal Kozdrach
Materials 2024, 17(16), 3959; https://doi.org/10.3390/ma17163959 - 9 Aug 2024
Viewed by 596
Abstract
This paper presents the results of a study on the effect of the dispersed phase on the lubricating and rheological properties of selected lubricant compositions. A vegetable oil base (rapeseed oil) was used to prepare vegetable lubricants, which were then thickened with lithium [...] Read more.
This paper presents the results of a study on the effect of the dispersed phase on the lubricating and rheological properties of selected lubricant compositions. A vegetable oil base (rapeseed oil) was used to prepare vegetable lubricants, which were then thickened with lithium stearate, calcium stearate, aluminum stearate, amorphous silica, and montmorillonite. Based on the results of the tribological tests of selected lubricating compositions, it was found that calcium stearate and montmorillonite have the most beneficial effect on the anti-wear properties of the tested lubricating greases, while silica thickeners (amorphous silica and montmorillonite) provide the effective anti-wear protection in compared to the lubricants produced on lithium and aluminum stearate. The lowest structural viscosity was found for grease thickened with montmorillonite. Much higher values of this parameter were observed for composition, where aluminum stearate was the dispersed phase, while the highest value of structural viscosity was observed for composition, where aerosol–amorphous silica was the thickener. The composition thickened with amorphous silica had the highest yield point value, while the composition in which montmorillonite was the dispersed phase had the lowest value. Dynamic viscosity decreases with temperature, which is characteristic of lubricants. No significant differences in dynamic viscosity were found for the lubricating compositions tested at temperatures above 50 [°C]. The most favorable rheological properties were observed for composition, which was produced using calcium stearate, as it allows the lowest dynamic viscosity at −20 [°C]. Lubricants produced with lithium stearate or aluminum stearate were characterized by higher viscosity at low temperatures. For grease, in which the lithium stearate was used as a thickener, the value of the elasticity index determines the weak viscoelastic properties of tested grease and a greater tendency to change structure under the influence of applied forces. For vegetable grease thickened with aluminum stearate, more than 15 times lower values of the MSD function were observed, and the calculated elasticity index value proves the stronger viscoelastic properties of the aluminum stearate grease in relation to grease thickened with the lithium stearate. The elasticity index value for grease thickened with amorphous silica was lower than for greases thickened with lithium and aluminum stearate, indicating its stronger viscoelastic properties in relation to these two greases. For grease composition prepared on the vegetable oil base and thickened with montmorillonite. The value of the elasticity index was lower than most of the tested grease compositions, without the composition, in which the calcium stearate was used as a thickener. Such results testify to moderately strong viscoelastic properties, which leads to the conclusion that the produced lubricant was a stable substance on changes in chemical structure under the influence of variable conditions prevailing during work in tribological joints. Full article
(This article belongs to the Special Issue Advanced Materials for Environmental Applications)
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<p>Welding load of a tribosystem lubricated with compositions based on rapeseed oil with different thickeners.</p>
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<p>Limiting pressure of seizure of tribosystem lubricated with compositions based on rapeseed oil with different thickeners.</p>
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<p>Scuffing load of tribosystem lubricated with compositions based on rapeseed oil with different thickeners.</p>
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<p>The limiting load of scuffing of tribosystem lubricated with compositions based on rapeseed oil with different thickeners.</p>
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<p>Limiting load of wear of tribosystem lubricated with compositions produced on rapeseed oil with different thickeners.</p>
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<p>The dependence of shear stress on shear rate (flow curves) for lubricants produced on different thickeners.</p>
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<p>The dependence of dynamic viscosity from temperature (viscosity curves) for greases produced with different thickeners.</p>
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<p>The dependence of dynamic viscosity from shear rate (viscosity curves) for lubricants produced with different thickeners.</p>
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<p>The dependence of the value of the MSD correlation function on time for a lubricating composition based on rapeseed oil and thickened with lithium stearate.</p>
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<p>The dependence of the value of the MSD correlation function on time for a lubricating composition based on rapeseed oil and thickened with aluminum stearate.</p>
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<p>The dependence of the value of the MSD correlation function on time for a lubricating composition based on rapeseed oil and thickened with calcium stearate.</p>
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<p>The dependence of the value of the MSD correlation function on time for a lubricating composition based on rapeseed oil and thickened with amorphous silica–Aerosil.</p>
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<p>The dependence of the value of the MSD correlation function on time for a lubricating composition based on rapeseed oil and thickened with montmorillonite.</p>
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<p>The dependence of G′ and G″ modulus values on frequency for grease produced on rapeseed oil base and thickened with lithium stearate.</p>
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<p>The dependence of G′ and G″ modulus values on frequency for grease produced on rapeseed oil base and thickened with aluminum stearate.</p>
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<p>The dependence of G′ and G″ modulus values on frequency for grease produced on rapeseed oil base and thickened with calcium stearate.</p>
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<p>The dependence of G′ and G″ modulus values on frequency for grease produced on rapeseed oil base and thickened with amorphous silica–Aerosil.</p>
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<p>The dependence of G′ and G″ modulus values on frequency for grease produced on rapeseed oil base and thickened with montmorillonite.</p>
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13 pages, 57896 KiB  
Article
Wear Mechanisms of the Working Surface of Gears after Scuffing Tests
by Edyta Osuch-Słomka, Remigiusz Michalczewski, Anita Mańkowska-Snopczyńska, Marek Kalbarczyk, Andrzej N. Wieczorek and Emilia Skołek
Materials 2024, 17(14), 3552; https://doi.org/10.3390/ma17143552 - 18 Jul 2024
Viewed by 436
Abstract
Identification of changes occurring on the working surface of lubricated gears using analytical equipment, e.g., an FE-SEM scanning electron microscope with an EDS microanalyzer, a WLI interferometric microscope, or a GDEOS optical discharge spectrometer, enables the characterisation of wear mechanisms of this surface. [...] Read more.
Identification of changes occurring on the working surface of lubricated gears using analytical equipment, e.g., an FE-SEM scanning electron microscope with an EDS microanalyzer, a WLI interferometric microscope, or a GDEOS optical discharge spectrometer, enables the characterisation of wear mechanisms of this surface. Definition of the phenomena occurring on the surface of tribo-couples after scuffing tests enables a comparative analysis of scuffing resistance and surface properties of the micro- and nanostructure, and elemental composition of the tested gears. Recognition and analysis of the wear mechanisms occurring on the working surface of gears will reduce the risk of damage and losses resulting from the need for maintenance and repair. The study concerned the working surfaces of gears made of 17HNM and 35HGSA steels on which a W-DLC/CrN coating was deposited. Shell Omala S4 GX 320 commercial industrial oil with a synthetic PAO (polyalphaolefin) base was selected for the lubrication of the gears. Tribological tests employed an FZG gear scuffing under severe conditions test method and they were carried out on a T-12U test rig for cylindrical gear analysis. Full article
(This article belongs to the Special Issue Friction and Wear of Materials Surfaces (2nd Edition))
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Figure 1
<p>A10 scuffing test gears.</p>
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<p>SEM microscope images: (<b>a</b>) 17HNM steel/W-DLC/CrN coating, (<b>b</b>) 35HGSA steel/W-DLC/CrN coating and GDOES depth profile of W/DLC/CrN coating.</p>
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<p>T-12U face-to-face gear test rig.</p>
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<p>Microhardness profiles.</p>
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<p>Results of working surface tests obtained using an SEM microscope.</p>
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<p>SEM images and maps of the EDS elemental distribution from the working surface of tooth. 17HNM/coating and 35HGSA/coating after scuffing tests at 1500× magnification.</p>
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<p>SEM images and maps of the EDS elemental distribution from the working surface of tooth. 17HNM/coating and 35HGSA/coating after scuffing tests at 1500× magnification.</p>
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<p>Results of working surface tests obtained using an AFM microscope.</p>
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<p>Results of working surface tests obtained using an AFM microscope.</p>
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<p>Results of pre-scuffing tests of the pinion’s working surface obtained using a WLI microscope.</p>
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<p>Results of post-scuffing tests of the pinion’s working surface obtained using a WLI microscope.</p>
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20 pages, 12530 KiB  
Article
Research on Calculation and Optimization Methods for Tooth Flash Temperature and Meshing Power Loss of the Gear System in Drum Shearer
by Bo Bai, Run Mao, Wenchao Guo and Shimin Mao
Appl. Sci. 2024, 14(12), 5222; https://doi.org/10.3390/app14125222 - 16 Jun 2024
Viewed by 567
Abstract
The operating conditions of the drum shearer are very complex, and its ranging arm gear system often suffers from gear scuffing and wear. Gear scuffing is caused by the adhesive wear, which is due to the instantaneous friction and flash temperature of the [...] Read more.
The operating conditions of the drum shearer are very complex, and its ranging arm gear system often suffers from gear scuffing and wear. Gear scuffing is caused by the adhesive wear, which is due to the instantaneous friction and flash temperature of the tooth surface, and the gear meshing power loss is also caused by tooth surface friction. In order to resist tooth scuffing and improve meshing efficiency of the transmission system, an improved semi-analytical tooth surface flash temperature calculation method was used. The tooth flash temperature status under various working conditions were analyzed in detail. Based on the mechanical model of the shearer drum picks, the load condition of the drum was analyzed. Under these load and boundary conditions, the misalignments of each gear pair in the ranging arm were calculated. The tooth surface load distribution was calculated under the gear misalignments, and then the theoretical tooth surface flash temperature and meshing power loss were determined. Next, the tooth micro-geometry was modified to reduce flash temperature and meshing power loss. The flash temperature distribution pattern of the optimized tooth surface was studied under various working conditions, and the meshing power loss was also obtained. Finally, experiments were conducted to verify the effects of the optimized tooth surface on the friction temperature rise and the effectiveness of the modification method. Tooth surface optimization aimed at reducing tooth surface flash temperature can also effectively reduce meshing power loss, which has a significant effect on gear anti-scuffing and energy saving. Full article
(This article belongs to the Topic Research on the Mechanical Wear of Gear-Shaped Parts)
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Figure 1
<p>A drum shearer and its components.</p>
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<p>Force diagram for a cutting tooth (red line) of a cutter drum.</p>
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<p>Force diagram of a cutter drum.</p>
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<p>The external load (forces and torque) and boundary condition on the ranging arm.</p>
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<p>The misalignments of all gear pairs.</p>
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<p>Relative sliding speed and load distribution on the tooth surface of involute cylindrical gears.</p>
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<p>The scheme and evaluation of tooth surface micro-geometry modification. (<b>a</b>) Theory tooth surface contact stress. (<b>b</b>) Modified tooth surface contact stress. (<b>c</b>) Tooth surface modification.</p>
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<p>Colormap of tooth surface flash temperature distribution of gearset-G1735.</p>
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<p>Colormap of tooth surface flash temperature distribution of gearset-G1735.</p>
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<p>Maximum flash temperature of gearsets before and after tooth modification under full load conditions.</p>
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<p>Tooth surface flash temperature of G1735 under load spectrum. (<b>a</b>) Non-modified tooth surface; (<b>b</b>) modified tooth surface.</p>
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<p>Tooth surface flash temperature under various operation conditions. (<b>a</b>) Flash temperature curves with speed variation; (<b>b</b>) flash temperature curves with torque variation.</p>
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<p>Gear meshing power loss under load spectrum. (<b>a</b>) Theory tooth surface of G1735; (<b>b</b>) improved tooth surface of G1735.</p>
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<p>Gear meshing efficiency under load spectrum. (<b>a</b>) Theory tooth surface of G1735; (<b>b</b>) optimized tooth surface of G1735.</p>
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<p>Gears meshing accumulated power loss under various operation conditions. (<b>a</b>) Accumulated power loss with speed variation; (<b>b</b>) accumulated power loss with torque variation.</p>
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<p>Gear meshing efficiency under various operation conditions. (<b>a</b>) Meshing efficiency vs. speed; (<b>b</b>) meshing efficiency vs. torque.</p>
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<p>Modified tooth surface of gears were (<b>a</b>) ground, (<b>b</b>) measured, and (<b>c</b>) tested for load contact pattern.</p>
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<p>Layout position of temperature sensors.</p>
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<p>Measurement results of temperature sensors.</p>
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26 pages, 15536 KiB  
Article
Emergence of Coated Piston Ring Scuffing Behavior on an Application-Oriented Tribological Model Test System
by Thomas Markut, Florian Summer, Michael Pusterhofer and Florian Grün
Lubricants 2024, 12(6), 218; https://doi.org/10.3390/lubricants12060218 - 14 Jun 2024
Viewed by 736
Abstract
A major problem in lubricated piston ring/cylinder liner contact sliding systems is the tribological failure mechanisms known as scuffing. In order to evaluate and better understand this damage phenomenon in these tribological systems, a tilted linear tribometer (TE77) for application-oriented reciprocating model tests [...] Read more.
A major problem in lubricated piston ring/cylinder liner contact sliding systems is the tribological failure mechanisms known as scuffing. In order to evaluate and better understand this damage phenomenon in these tribological systems, a tilted linear tribometer (TE77) for application-oriented reciprocating model tests was developed and validated with scuffed field engine parts. With precise oil lubrication, original engine parts, such as CKS-coated piston rings (chromium-based coating with included aluminum oxides), original liners and fully formulated lubrications, were tested under conditions similar to the most critical part of the internal combustion engines (ICEs), known as fired top dead center (FTDC). Various in situ measurements during the tests allowed for a detailed investigation of the damage processes (crack transformation) on the tribological components. For the coated piston ring, vertical cracks were attributed to residual stresses, while horizontal cracks resulted from shear stresses. The crack transformation and wear results from other studies were confirmed for the liner. The results from FIB (Focused Ion Beam) cuts, along with EDS and SEM analyses, revealed that Fe (deriving from material transfer) acts as a catalyst on the CKS layer for the tribopads and that zinc sulfides are not present everywhere. Full article
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Figure 1
<p>Cut and surface views of piston ring.</p>
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<p>Cut and surface views of cylinder liner.</p>
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<p>Piston ring analysis—field engine part.</p>
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<p>Liner analysis—field engine part.</p>
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<p>Description of the application-oriented model test rig.</p>
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<p>Illustration of the test strategies carried out.</p>
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<p>Test specimen manufacturing areas.</p>
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<p>Test specimen installation and conformity check.</p>
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<p>Test matrix.</p>
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<p>Data analysis from test setup 1.</p>
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<p>Surface, EDS and SEM analysis from a representative test of test setup 1 (left side—piston ring, right side—cylinder liner).</p>
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<p>Data analysis from test setup 2.</p>
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<p>Surface, EDS and SEM analysis from a representative test of test setup 2 (left side—piston ring, right side—cylinder liner).</p>
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<p>Result table—test setup 1 and test setup 2.</p>
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<p>Emergence damage mechanisms of the piston ring until scuffing phenomenon.</p>
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<p>FIB-cut of piston ring with SEM analysis.</p>
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<p>FIB-cut of piston rings with EDS analysis.</p>
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<p>FIB-cut with EDS area analysis.</p>
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<p>Emergence damage mechanisms of the cylinder liner until scuffing phenomenon.</p>
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<p>Heating test—one cycle and ten cycles.</p>
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<p>Surface analysis—piston ring heating tests.</p>
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<p>Tribological damage model.</p>
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33 pages, 17121 KiB  
Review
Mathematical Complexities in Modelling Damage in Spur Gears
by Aselimhe Oreavbiere and Muhammad Khan
Machines 2024, 12(5), 346; https://doi.org/10.3390/machines12050346 - 16 May 2024
Viewed by 784
Abstract
Analytical modelling is an effective approach to obtaining a gear dynamic response or vibration pattern for health monitoring and useful life prediction. Many researchers have modelled this response with various fault conditions commonly observed in gears. The outcome of such models provides a [...] Read more.
Analytical modelling is an effective approach to obtaining a gear dynamic response or vibration pattern for health monitoring and useful life prediction. Many researchers have modelled this response with various fault conditions commonly observed in gears. The outcome of such models provides a good idea about the changes in the dynamic response available between different gear health states. Hence, a catalogue of the responses is currently available, which ought to aid predictions of the health of actual gears by their vibration patterns. However, these analytical models are limited in providing solutions to useful life prediction. This may be because a majority of these models used single fault conditions for modelling and are not valid to predict the remaining life of gears undergoing more than one fault condition. Existing reviews related to gear faults and dynamic modelling can provide an overview of fault modes, methods for modelling and health prediction. However, these reviews are unable to provide the critical similarities and differences in the single-fault dynamic models to ascertain the possibility of developing models under combined fault modes. In this paper, existing analytical models of spur gears are reviewed with their associated challenges to predict the gear health state. Recommendations for establishing more realistic models are made especially in the context of modelling combined faults and their possible impact on gear dynamic response and health prediction. Full article
(This article belongs to the Section Machines Testing and Maintenance)
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Figure 1

Figure 1
<p>(<b>a</b>) tooth breakage, (<b>b</b>) pitting, (<b>c</b>) spalling, (<b>d</b>) abrasive wear, (<b>e</b>) scuffing [<a href="#B22-machines-12-00346" class="html-bibr">22</a>,<a href="#B30-machines-12-00346" class="html-bibr">30</a>,<a href="#B31-machines-12-00346" class="html-bibr">31</a>].</p>
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<p>One-stage gear system with 6 degrees of freedom (Reproduced from original) [<a href="#B36-machines-12-00346" class="html-bibr">36</a>].</p>
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<p>Gear tooth without fault (Reproduced from original) [<a href="#B42-machines-12-00346" class="html-bibr">42</a>].</p>
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<p>Points of single and double tooth engagement on (<b>a</b>) Line of action (<b>b</b>) Gear tooth [<a href="#B36-machines-12-00346" class="html-bibr">36</a>].</p>
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<p>TVMS of a healthy gear pair [<a href="#B44-machines-12-00346" class="html-bibr">44</a>].</p>
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<p>Healthy gear pair time domain response [<a href="#B45-machines-12-00346" class="html-bibr">45</a>].</p>
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<p>Healthy gear pair frequency domain response [<a href="#B45-machines-12-00346" class="html-bibr">45</a>].</p>
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<p>View of a gear tooth with pit [<a href="#B46-machines-12-00346" class="html-bibr">46</a>].</p>
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<p>TVMS for different pitting degrees [<a href="#B44-machines-12-00346" class="html-bibr">44</a>].</p>
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<p>TVMS for different pitting shapes [<a href="#B56-machines-12-00346" class="html-bibr">56</a>].</p>
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<p>Time domain response for different pitting degrees [<a href="#B45-machines-12-00346" class="html-bibr">45</a>].</p>
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<p>Dynamic response of different pitting degrees in the frequency domain [<a href="#B45-machines-12-00346" class="html-bibr">45</a>].</p>
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<p>View of a gear tooth with a rectangular spall [<a href="#B42-machines-12-00346" class="html-bibr">42</a>].</p>
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<p>TVMS showing spalls of increasing length [<a href="#B75-machines-12-00346" class="html-bibr">75</a>].</p>
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<p>Time and freqyency domain dynamic responses for spall defect [<a href="#B70-machines-12-00346" class="html-bibr">70</a>].</p>
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<p>Tooth crack with constant crack depth [<a href="#B39-machines-12-00346" class="html-bibr">39</a>].</p>
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<p>Tooth crack with varying crack depth [<a href="#B82-machines-12-00346" class="html-bibr">82</a>].</p>
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<p>TVMS for different stages of tooth root crack and breakage for [<a href="#B84-machines-12-00346" class="html-bibr">84</a>].</p>
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<p>Time domain signal for root crack [<a href="#B80-machines-12-00346" class="html-bibr">80</a>].</p>
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<p>Frequency domain signal for root crack [<a href="#B80-machines-12-00346" class="html-bibr">80</a>].</p>
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<p>Gear tooth with wear [<a href="#B97-machines-12-00346" class="html-bibr">97</a>].</p>
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<p>(<b>a</b>) TVMS and (<b>b</b>) STE plots for varying wear conditions [<a href="#B96-machines-12-00346" class="html-bibr">96</a>].</p>
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<p>Non-uniform wear [<a href="#B91-machines-12-00346" class="html-bibr">91</a>].</p>
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<p>TVMS due to wear [<a href="#B91-machines-12-00346" class="html-bibr">91</a>].</p>
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<p>Time domain response for (<b>a</b>) 0 mm wear (<b>b</b>) 0.25 mm wear [<a href="#B91-machines-12-00346" class="html-bibr">91</a>].</p>
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<p>Frequency domain response for (<b>a</b>) 0 mm wear (<b>b</b>) 0.25 mm wear [<a href="#B91-machines-12-00346" class="html-bibr">91</a>].</p>
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<p>Temperature variation along the line of action [<a href="#B100-machines-12-00346" class="html-bibr">100</a>].</p>
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<p>Contact temperature along LOA for changes in (<b>a</b>) Tooth Width, (<b>b</b>) Pressure angle, (<b>c</b>) module [<a href="#B100-machines-12-00346" class="html-bibr">100</a>].</p>
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<p>Contact temperature along the LOA for changes in (<b>a</b>) rotational velocity, (<b>b</b>) Torque [<a href="#B100-machines-12-00346" class="html-bibr">100</a>].</p>
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<p>Coupled root crack and pitting model [<a href="#B107-machines-12-00346" class="html-bibr">107</a>].</p>
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<p>TVMS for coupled root crack and pitting [<a href="#B107-machines-12-00346" class="html-bibr">107</a>].</p>
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<p>Time domain response for combined root crack and pitting [<a href="#B107-machines-12-00346" class="html-bibr">107</a>].</p>
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<p>Frequency domain response for combined root crack and pitting [<a href="#B107-machines-12-00346" class="html-bibr">107</a>].</p>
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17 pages, 10275 KiB  
Article
Tribological Behavior of GTL Base Oil Improved by Ni-Fe Layered Double Hydroxide Nanosheets
by Shuo Xiang, Xinghao Zhi, Hebin Bao, Yan He, Qinhui Zhang, Shigang Lin, Bo Hu, Senao Wang, Peng Lu, Xin Yang, Qiang Tian and Xin Du
Lubricants 2024, 12(5), 146; https://doi.org/10.3390/lubricants12050146 - 26 Apr 2024
Viewed by 971
Abstract
The layered double hydroxide (LDH) has been practically applied in the field of tribology and materials science due to its unique physicochemical properties, weak bonding, flexible structural composition, and adjustable interlayer space. In this work, a series of ultrathin and flexible composition of [...] Read more.
The layered double hydroxide (LDH) has been practically applied in the field of tribology and materials science due to its unique physicochemical properties, weak bonding, flexible structural composition, and adjustable interlayer space. In this work, a series of ultrathin and flexible composition of Ni-Fe LDH samples were prepared via a cost-effective room-temperature co-precipitation process. Then, they were mechanically dispersed into GTL base oil and their lubricating performance were tested by a four-ball tribometer. It is found that the variation of Ni-Fe ratio of Ni-Fe LDH has a great influence on the improvement of lubricating performance of GTL base oil. At the same concentration (0.3 mg/mL), the Ni-Fe LDH with Ni/Fe ratio of 6 was demonstrated to exhibit the best lubricating performance and the AFC, WSD, the wear volume, surface roughness and average wear scar depth decreased 51.3%, 30.8%, 78.4%, 6.7% and 50.0%, respectively. SEM-EDS and X-ray photoelectron spectra illustrated that the tribo-chemical film consisting of iron oxides and NiO with better mechanical properties formed and slowly replaced the physical film, which resists scuffing and protect solid surface from severe collisions. Full article
(This article belongs to the Special Issue Tribology of 2D Nanomaterials)
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<p>The powder X-ray patterns of the four as-prepared Ni-Fe LDH samples (<b>a</b>,<b>b</b>). FTIR measurement of the four synthesized Ni-Fe LDH samples (<b>c</b>).</p>
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<p>TG and DTG curves of Ni-Fe LDH samples. Ni/Fe ratios of 2 (<b>a</b>), 3 (<b>b</b>), 4 (<b>c</b>) and 6 (<b>d</b>).</p>
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<p>TG and DTG curves of Ni-Fe LDH samples. Ni/Fe ratios of 2 (<b>a</b>), 3 (<b>b</b>), 4 (<b>c</b>) and 6 (<b>d</b>).</p>
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<p>Tribological performance of Ni-Fe LDHs. (<b>a</b>,<b>b</b>) variations of COF, AFC and WSD of GTL base oil with load (60 min, RT, 1200 rpm), (<b>c</b>–<b>j</b>) variations of COF, AFC and WSD of GTL base oil with Ni-Fe ratio and concentration (600 N, 60 min, RT, 1200 rpm).</p>
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<p>Tribological performance of Ni-Fe LDHs. (<b>a</b>,<b>b</b>) variations of COF, AFC and WSD of GTL base oil with load (60 min, RT, 1200 rpm), (<b>c</b>–<b>j</b>) variations of COF, AFC and WSD of GTL base oil with Ni-Fe ratio and concentration (600 N, 60 min, RT, 1200 rpm).</p>
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<p>Tribological performance of Ni-Fe LDHs. (<b>a</b>,<b>b</b>) variations of COF, AFC and WSD of GTL base oil with load (60 min, RT, 1200 rpm), (<b>c</b>–<b>j</b>) variations of COF, AFC and WSD of GTL base oil with Ni-Fe ratio and concentration (600 N, 60 min, RT, 1200 rpm).</p>
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<p>3D morphology and average depth of steel ball wear scar surfaces, (<b>a</b>–<b>c</b>) lubricated by GTL base oil, (<b>d</b>–<b>f</b>) lubricated by GTL base oil + 0.3 mg/ml Ni−Fe LDH with Ni/Fe ratio of 6.</p>
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<p>3D morphology and average depth of steel ball wear scar surfaces, (<b>a</b>–<b>c</b>) lubricated by GTL base oil, (<b>d</b>–<b>f</b>) lubricated by GTL base oil + 0.3 mg/ml Ni−Fe LDH with Ni/Fe ratio of 6.</p>
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<p>SEM images and EDS mapping of worn surface of steel ball lubricated by GTL base oil.</p>
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<p>SEM images and EDS mapping of worn surface of steel ball lubricated by GTL base oil + 0.3 mg/mL Ni-Fe LDH with Ni/Fe ratio of 6.</p>
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<p>SEM images and EDS mapping of worn surface of steel ball lubricated by GTL base oil + 0.3 mg/mL Ni-Fe LDH with Ni/Fe ratio of 6.</p>
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<p>XPS spectrum of steel ball wear spot surface lubricated by GTL base oil and GTL base oil + 0.3 mg/ml Ni−Fe LDH with Ni/Fe ratio of 6. (<b>a</b>) XPS survey spectra, (<b>b</b>) C 1s, (<b>c</b>) Fe 2p, (<b>d</b>) Ni 2p, (<b>e</b>) O 1s.</p>
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<p>XPS spectrum of steel ball wear spot surface lubricated by GTL base oil and GTL base oil + 0.3 mg/ml Ni−Fe LDH with Ni/Fe ratio of 6. (<b>a</b>) XPS survey spectra, (<b>b</b>) C 1s, (<b>c</b>) Fe 2p, (<b>d</b>) Ni 2p, (<b>e</b>) O 1s.</p>
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<p>Schematic diagrams of lubrication mechanism for GTL base oil enhanced with Ni-Fe LDH with Ni/Fe ratio of 6: (<b>a</b>) schematic illustration of the four-sphere point contact model, (<b>b</b>,<b>d</b>) boundary lubrication between two sliding surfaces of a solid rough peaks and ridges, (<b>c</b>,<b>e</b>) hydrodynamic lubrication in the area of fluid contact.</p>
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22 pages, 15957 KiB  
Article
Part Defect Detection Method Based on Channel-Aware Aggregation and Re-Parameterization Asymptotic Module
by Enyuan Bian, Mingfeng Yin, Shiyu Fu, Qi Gao and Yaozong Li
Electronics 2024, 13(3), 473; https://doi.org/10.3390/electronics13030473 - 23 Jan 2024
Viewed by 1005
Abstract
In industrial production, the quality, reliability, and precision of parts determine the overall quality and performance of various mechanical equipment. However, existing part defect detection methods have shortcomings in terms of feature extraction and fusion, leading to issues of missed detection. To address [...] Read more.
In industrial production, the quality, reliability, and precision of parts determine the overall quality and performance of various mechanical equipment. However, existing part defect detection methods have shortcomings in terms of feature extraction and fusion, leading to issues of missed detection. To address this challenge, this manuscript proposes a defect detection algorithm for parts (CRD-YOLO) based on the improved YOLOv5. Our first aim is to increase the regional features of small targets and improve detection accuracy. In this manuscript, we design the channel- aware aggregation (CAA) module, utilizing a multi-branch convolutional segmentation structure and incorporating an attention mechanism and ConvNeXt V2 Block as bottleneck layers for feature processing. Secondly, the re-parameterization asymptotic module (RAFPN) is used to replace the original model neck structure in order to improve the interaction between shallow-detail features and deeper semantic features, and to avoid the large semantic gaps between non-neighboring layers. Then, the DO-DConv module is encapsulated within the BN layer and the LeakyReLU activation function to become the DBL module, which further processes the feature output from the backbone network and fuses neck features more comprehensively. Finally, experiments with the self-made dataset show that the model proposed in this paper improves the accuracy of detecting various types of defect. In particular, it increased the accuracy of detecting bearing scuffing defects with significant dimensional variations, with an improvement of 6%, and gear missing teeth defects with large shape differences, with an 8.3% enhancement. Additionally, the mean average precision (mAP) reached 96.7%, an increase of 5.5% and 6.4% compared to YOLOv5s and YOLOv8s, respectively. Full article
(This article belongs to the Section Artificial Intelligence)
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<p>CRD-YOLO architecture structure: (<b>a</b>) CAA module; (<b>b</b>) DBL module. (where green arrows indicate down-sampling operations and blue arrows indicate up-sampling operations).</p>
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<p>Schematic diagram of CAA modules: (<b>a</b>) ConvNeXt V2 Block; (<b>b</b>) ConvNeXtV2SE Block; (<b>c</b>) C3 module; (<b>d</b>) CAA module.</p>
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<p>Structure of the SE attention mechanism.</p>
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<p>CAA module feature map visualization: (<b>I</b>) Original image; (<b>II</b>) C3 module result; (<b>III</b>) CAA module result; (<b>a</b>) groove; (<b>b</b>) abrasion; (<b>c</b>) blemish; (<b>d</b>) break; (<b>e</b>) lack; (<b>f</b>) scratch.</p>
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<p>SPPF spatial pyramid pooling.</p>
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<p>RepConv module.</p>
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<p>RAFPN module.</p>
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<p>DBL module.</p>
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<p>Sample of defects in the datasets.</p>
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<p>Evolution of the evaluation metrics for the model training process based on the self-constructed datasets.</p>
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<p>Detection results of the improved model for various types of defective images.</p>
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<p>Eight-channel predicted images and visual feature maps of the posterior three detection layers of the neck after different approaches: (<b>I</b>) original model; (<b>II</b>) CAA; (<b>III</b>) ConSE and RAFPN; (<b>IV</b>) final improved model.</p>
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<p>Thermograms’ Visualization: (<b>a</b>) grooves; (<b>b</b>) wear; (<b>c</b>) scratches; (<b>d</b>) broken teeth; (<b>e</b>) missing teeth; (<b>f</b>) scratches; (<b>I</b>) original; (<b>II</b>) YOLOv5s; (<b>III</b>) modified YOLOv5s.</p>
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<p>Feature map visualization: (<b>I</b>) original image; (<b>II</b>) P3 layer CBS module results; (<b>III</b>) C3 module results; (<b>IV</b>) CAA module results; (<b>V</b>) RAFPN module results; (<b>a</b>) groove; (<b>b</b>) abrasion; (<b>c</b>) blemish; (<b>d</b>) break; (<b>e</b>) lack; (<b>f</b>) scratch.</p>
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14 pages, 7462 KiB  
Article
Investigation of the Influence of Contact Patterns of Worm-Gear Sets on Friction Heat Generation during Meshing
by Aleksandar Miltenović, Milan Banić, Nikola Vitković, Miloš Simonović, Marko Perić and Damjan Rangelov
Appl. Sci. 2024, 14(2), 738; https://doi.org/10.3390/app14020738 - 15 Jan 2024
Viewed by 1352
Abstract
Friction losses and scuffing failures are interesting research topics for worm gears. One of the factors leading to scuffing is the heat generated in the contact of gear teeth. The contact geometry of worm gears is complex, leading to high friction between contact [...] Read more.
Friction losses and scuffing failures are interesting research topics for worm gears. One of the factors leading to scuffing is the heat generated in the contact of gear teeth. The contact geometry of worm gears is complex, leading to high friction between contact surfaces. High friction between contact surfaces during operation generates heat friction that causes the occurrence of scuffing, which in turn determines the scuffing load capacity. To analyse the thermal characteristics of a worm-gear pair and the thermal behaviour of contact teeth, a direct-coupled thermal–structural 3D finite element model was applied. The heat flux due to friction-generated heat was determined on the gear tooth to investigate thermal characteristics and predict transient temperature fields. This study permits an in-depth understanding of the temperature fields and the friction heat generation process. Also, better control of the contact pattern between worm-gear teeth would decrease friction heat and increase scuffing load capacity. This paper investigates the transient thermal behaviour among different pinion machine setting parameters that can result in an optimal tooth-contact pattern that produces a lower temperature field, thus achieving higher transmission efficiency. Full article
(This article belongs to the Special Issue Modern Research of Gears and Power Transmission)
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<p>CAD model of worm-gear pair.</p>
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<p>Worm-gear tooth.</p>
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<p>Contact pattern of the version in the middle.</p>
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<p>Contact pattern at the worm gear with the contact shifted to the outlet side.</p>
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<p>Contact pattern at the worm gear with the contact shifted to the inlet side.</p>
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<p>FEM setup for the directly coupled transient thermal–structural analysis.</p>
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<p>Mesh at the worm-gear tooth.</p>
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<p>Contact surfaces of worm and worm gear.</p>
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<p>Pressure distribution in the worm gear: (<b>a</b>) normal contact pattern; (<b>b</b>) contact pattern on the outlet side; (<b>c</b>) contact pattern on the inlet side.</p>
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<p>Heat flux distributions for the standard contact pattern: (<b>a</b>) contact on two teeth, (<b>b</b>) contact on three teeth.</p>
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<p>Heat flux distributions for the contact pattern shifted to the outlet side: (<b>a</b>) contact on two teeth, (<b>b</b>) contact on three teeth.</p>
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<p>Heat flux distribution for the contact pattern shifted to the inlet side: (<b>a</b>) contact on two teeth, (<b>b</b>) contact on three teeth.</p>
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<p>Differences in heat flux for three variants.</p>
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9 pages, 1115 KiB  
Proceeding Paper
Bending Stresses in Profile Corrected Gears
by Sachidananda Hassan Krishnamurthy and Raghunandana Kurkal
Eng. Proc. 2023, 59(1), 109; https://doi.org/10.3390/engproc2023059109 - 24 Dec 2023
Viewed by 511
Abstract
In the present investigation, bending stress of a profile corrected altered tooth-sums gear train, for a constant center distance, is estimated. The number of teeth altered by ±4% is considered and bending stress is estimated for 25° and 20° pressure angle gears. Since [...] Read more.
In the present investigation, bending stress of a profile corrected altered tooth-sums gear train, for a constant center distance, is estimated. The number of teeth altered by ±4% is considered and bending stress is estimated for 25° and 20° pressure angle gears. Since the stress concentration depends on the type of fillet radius, in this work, the bending stresses are computed in the tooth for various fillet radii generated by rack cutters such as; sharp corner tip, rounded corner tip, protuberance tip, and fully rounded tip. It is found that the bending stress is less in the tooth radius generated by a fully rounded tip cutter. Full article
(This article belongs to the Proceedings of Eng. Proc., 2023, RAiSE-2023)
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<p>Fillet Profile.</p>
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<p>Maximum bending stress at various profile shift for tooth sum of: (<b>a</b>) 96 teeth, (<b>b</b>) 100 teeth and (<b>c</b>) 104 teeth for 25° Pressure angle.</p>
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<p>Maximum bending stress at various profile shift for tooth sum of: (<b>a</b>) 96 teeth, (<b>b</b>) 100 teeth, and (<b>c</b>) 104 teeth for 20° Pressure angle.</p>
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11 pages, 7048 KiB  
Article
Tribological Performance and Scuffing Resistance of Cast-Iron Cylinder Liners and Al-Si Alloy Cylinder Liners
by Chengdi Li, Xiao Chen, Hao Liu, Lianjie Dong, Huihua Jian, Jingsi Wang and Fengming Du
Coatings 2023, 13(11), 1951; https://doi.org/10.3390/coatings13111951 - 15 Nov 2023
Cited by 2 | Viewed by 1162
Abstract
In order to better determine the applicable working conditions of Al-Si alloy cylinder liners and cast-iron cylinder liners, their tribological performance and scuffing resistance are discussed in this paper. After wear and scuffing tests, it was found that cast-iron cylinder liners had better [...] Read more.
In order to better determine the applicable working conditions of Al-Si alloy cylinder liners and cast-iron cylinder liners, their tribological performance and scuffing resistance are discussed in this paper. After wear and scuffing tests, it was found that cast-iron cylinder liners had better wear resistance and better scuffing resistance, but poor friction performance. Al-Si alloy cylinder liners had weaker wear resistance and scuffing resistance, but excellent friction performance. The wear mechanism of cast-iron cylinder liners is slight adhesive wear, and they are suitable for traditional fuel engines and turbocharged engines with high load, high power, and high stability. The wear mechanism of Al-Si alloy cylinder liners was a mixture of adhesive wear and abrasive wear, and they are suitable for engines that are lightweight, efficient, and energy-saving, and operate at high speeds. Full article
(This article belongs to the Special Issue Thin Films for Tribological Applications)
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<p>Honing roads on the surface of cylinder liners. (<b>a</b>) Cast-iron cylinder liner. (<b>b</b>) Al-Si alloy cylinder liner.</p>
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<p>Polished surface of cylinder liners. (<b>a</b>) Cast-iron cylinder liner. (<b>b</b>) Al-Si alloy cylinder liner.</p>
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<p>Schematic diagram of reciprocating-wear tests.</p>
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<p>Trend in friction force variation in scuffing test.</p>
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<p>Friction coefficient of two matched pairs.</p>
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<p>Weight loss of two matched pairs.</p>
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<p>Worn surface morphology of cylinder liners: (<b>a</b>) cast-iron cylinder liner; (<b>b</b>) Al-Si alloy cylinder liner.</p>
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<p>Worn surface morphology of CKS piston ring (SEM): (<b>a</b>) CKS piston ring worn against cast-iron cylinder liner; (<b>b</b>) CKS piston ring worn against Al-Si alloy cylinder liner.</p>
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<p>Friction force changes over time. (<b>a</b>) Cast-iron cylinder liner. (<b>b</b>) Al-Si alloy cylinder liner.</p>
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<p>Scuffing time of two matched pairs.</p>
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<p>Scuffing surface morphology of cylinder liners: (<b>a</b>) cast-iron cylinder liner; (<b>b</b>) Al-Si alloy cylinder liner.</p>
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<p>Scuffing surface morphology of piston ring (SEM): (<b>a</b>) CKS piston ring worn against cast-iron cylinder liner; (<b>b</b>) CKS piston ring worn against Al-Si alloy cylinder liner.</p>
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<p>Schematic diagram of the cylinder liner wear process.</p>
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22 pages, 13478 KiB  
Article
An Effective Analytical Approach to Predicting the Surface Contact Temperature of the Face Gear Drives
by Jun Wen, Yuansheng Zhou, Jinyuan Tang and Yu Dai
Mathematics 2023, 11(14), 3087; https://doi.org/10.3390/math11143087 - 13 Jul 2023
Cited by 3 | Viewed by 1246
Abstract
The anti-scuffing bearing capacity of gears is a significant issue for their service lives, especially for the cases with heavy loads or high speeds. Generally, the anti-scuffing bearing capacity is evaluated according to the surface contact temperature that can be calculated with either [...] Read more.
The anti-scuffing bearing capacity of gears is a significant issue for their service lives, especially for the cases with heavy loads or high speeds. Generally, the anti-scuffing bearing capacity is evaluated according to the surface contact temperature that can be calculated with either analytical methods or finite element analysis (FEA) methods. The analytical methods usually apply the theory of Blok to efficiently obtain the results by simplifying some actual physical conditions, which are well considered in the FEA methods with accurate results but more computation time. Conversely, a new efficient and accurate analytical method is proposed by introducing the actual lubricant film thickness and continuous heat transfer for the theory of Blok. These two physical conditions are the key issues for the calculation of the two parts of surface contact temperature, flash temperature and bulk temperature, respectively. For the calculation of flash temperature, elastohydrodynamic lubrication (EHL) is introduced to consider the lubricant film thickness for the theory of Blok, and the result is obtained by solving the Reynolds equation efficiently with the finite difference method. For the bulk temperature, the result for a contacting point on the gear tooth surface is directly obtained according the theory of Blok, and the continuous heat transfer among the adjacent contacting points is considered with Gaussian heat morphology, which can accurately construct the bulk temperature field distribution in the contact region. The proposed method is validated as in good agreement with the FEA method and with less computation time. Full article
(This article belongs to the Section Engineering Mathematics)
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<p>The flow chart of the organization of this work.</p>
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<p>The meshing of a face gear drives.</p>
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<p>Schematic diagram of the contact path of the face gears.</p>
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<p>Coordinate system and assembly errors for the TCA face gear drives.</p>
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<p>Contact temperature composition diagram.</p>
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<p>Gaussian distribution of bulk temperature.</p>
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<p>Face gear tooth surface contact temperature calculation software (° is the unit of angle).</p>
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<p>Face gear numerical model and tooth surface contact path.</p>
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<p>Temperature distribution along the contact path.</p>
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<p>Face gear drives with a helical pinion.</p>
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<p>Tooth surface contact temperature field distribution: (<b>a</b>) contact temperature of the face gear drives; (<b>b</b>) contact temperature of the face gear; (<b>c</b>) contact temperature of the pinion.</p>
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<p>Comparison of analytical results which are optimized by a Gaussian distribution with finite element analysis (FEA) results.</p>
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<p>Comparison of analytical results which use constant bulk temperature with FEA results.</p>
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<p>Influence of different geometric parameters on surface contact temperature: (<b>a</b>) effect of pressure angle on temperature; (<b>b</b>) effect of helix angle on temperature; (<b>c</b>) effect of shaft angle on temperature; (<b>d</b>) effect on face width on temperature.</p>
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<p>Influence of different geometric parameters on surface contact temperature: (<b>a</b>) effect of pressure angle on temperature; (<b>b</b>) effect of helix angle on temperature; (<b>c</b>) effect of shaft angle on temperature; (<b>d</b>) effect on face width on temperature.</p>
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<p>Face gear drives with a spur pinion.</p>
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<p>The result of the contact temperature at different pressure angles.</p>
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<p>Result of the contact temperature at different shaft angles.</p>
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13 pages, 6508 KiB  
Article
Analysis of the Operational Wear of the Combustion Engine Piston Pin
by Sławomir Kowalski, Bogusław Cieślikowski, Dalibor Barta, Ján Dižo and Aleš Dittrich
Lubricants 2023, 11(3), 100; https://doi.org/10.3390/lubricants11030100 - 26 Feb 2023
Cited by 8 | Viewed by 2506
Abstract
This article presents the results of research into the causes of the wear of the piston pin mounted in piston bosses by means of a hinge joint and in the connecting rod small end by means of the thermocompression bond. Changes in geometry [...] Read more.
This article presents the results of research into the causes of the wear of the piston pin mounted in piston bosses by means of a hinge joint and in the connecting rod small end by means of the thermocompression bond. Changes in geometry and in the pin-top surface structure, which are caused by the mutual influence of the mating surfaces in variable lubrication conditions, are presented. The progress of scuffing as a result of insufficient lubrication of the mating elements or oil film breaking is demonstrated. The state of destruction was confirmed by the results of surface roughness measurements showing the formation of build-ups. The loss of the thermocompression bond surface, caused by the penetration of sintered engine oil fractions containing biofuel additive components and spent engine oil improver packages, was noted. The progressing forms of wear are the cause of engine failures due to the pin movement towards the cylinder wall, and due to boss breakage in the piston. Full article
(This article belongs to the Special Issue Tribology in Mobility, Volume II)
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<p>Geometry of the joint between the piston pin (<b>a</b>) and connecting rod small end zone (<b>b</b>).</p>
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<p>Macroscopic image of the piston pin surface: (<b>a</b>) before operational tests and (<b>b</b>) after operational tests.</p>
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<p>Microscope image (200× magnification, reflected light) of the deposits on the piston pin in the destruction zone of the joint with the connecting rod small end.</p>
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<p>IR spectrum of the soluble part of the deposits on the piston pin in the destruction zone of the thermocompression bond with the connecting rod small end. The left side of the pin (green color), right side of the pin (red color).</p>
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<p>XRF spectrum of the soluble part of the deposits on the piston pin in the destruction zone of the thermocompression bond with the connecting rod small end.</p>
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<p>Microscopic images of the piston pin surface with visible traces of scuffing.</p>
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<p>Three-dimensional image of the piston pin surface profile in the wear zone.</p>
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<p>Map of the roughness profile of the piston pin in the wear zone (<b>a</b>) and the pattern of the Abbott-Firestone curve (<b>b</b>).</p>
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17 pages, 5344 KiB  
Article
Numerical Analysis of Friction Reduction and ATSLB Capacity of Lubricated MTS with Textured Micro-Elements
by Xigui Wang, Hui Huang, Jingyu Song, Yongmei Wang and Jiafu Ruan
Lubricants 2023, 11(2), 78; https://doi.org/10.3390/lubricants11020078 - 11 Feb 2023
Viewed by 1312
Abstract
The simulation analysis numerically investigates the thermoelastic lubricated interfacial Textured Micro-Element (TME) load-bearing contact, a theoretical model is proposed, and the effective friction reduction and Anti-Thermoelastic Scuffing Load bearing (ATSLB) capacity between random rough Meshing Teeth Surfaces (MTS) are presented, the mechanism linking [...] Read more.
The simulation analysis numerically investigates the thermoelastic lubricated interfacial Textured Micro-Element (TME) load-bearing contact, a theoretical model is proposed, and the effective friction reduction and Anti-Thermoelastic Scuffing Load bearing (ATSLB) capacity between random rough Meshing Teeth Surfaces (MTS) are presented, the mechanism linking interfacial thermoelastic lubrication, TME meshing friction reduction and ATSLB is revealed. The real contact domain area between MTS with multi-scale Micro-Element Textures (MET) is obtained for the numerical calculation of the three-dimensional equivalent TME contact volume, which is the correlation bridge between friction reduction and ATSLB of the thermoelastic lubrication interface. The proposed theoretical model predicts the time-varying behaviour of the textured meshing interface friction reduction with TME contact load under thermoelastic lubrication conditions. Numerical simulations show that the textured interface meshing volume is the key to solving the load-bearing problem of line contact between randomly rough teeth surfaces. The friction coefficients of the MTS are reduced by 13–24%. The lubricated load-bearing and friction reduction behaviour between the textured MTS is quantified by the thermoelastic voids of TME interface and actual meshing volume ratio, which provides a new perspective for further insight into the lubrication and friction reduction behaviour between the MTS with multi-scale MET-ATSLB coupling mechanism. Full article
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<p>Discrete and continuous micro-element textures.</p>
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<p>Discrete and continuous micro-element textures.</p>
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<p>Multiscale characterization for micro-element textures of contact interfaces (Distribution density and geometric parameters).</p>
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<p>A Homogenized equivalent meshing interface section of TME computational domain.</p>
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<p>An algorithm flow chart of multi-scale numerical model algorithm for lubricated MTS with TME.</p>
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<p>Experimental details of simulated micro-elements texturing MTS under TEHL: (<b>a</b>) Column Pin-Disc type simulated MTS line contact test rig, (<b>b</b>) Simulated analytical test procedure, (<b>c</b>) Determination of thermocouple sensor (Embedded) position (for measuring the contact temperature of MTS between lubricating interfaces) and (<b>d</b>) Actual MTS contact test bench with TME.</p>
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<p>Contact pressure distribution and TEHL film thickness variation of MTS without TME characteristics: (<b>a</b>) Contact pressure of untextured MTS under a load of 100N varies with linear velocity, (<b>b</b>) Contact pressure of untextured MTS under a load of 200N varies with linear velocity, (<b>c</b>) TEHL oil film thickness of untextured MTS under a load of 100N varies with linear velocity, and (<b>d</b>) TEHL oil film thickness of untextured MTS under a load of 200N varies with linear velocity.</p>
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<p>Variations of contact pressure and TEHL oil film thickness with textured MTS under 100 N, 150 N and 200 N loads and 1.0 m/s, 1.5 m/s and 2.0 m/s linear velocities: (<b>a</b>) Contact pressure with textured MTS under 100 N, 150 N and 200 N loads and 1.0 m/s, 1.5 m/s and 2.0 m/s linear velocities, (<b>b</b>) TEHL oil film thickness with textured MTS under 100 N, 150 N and 200 N loads and 1.0 m/s, 1.5 m/s and 2.0 m/s linear velocities.</p>
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<p>Contact pressure variations of interface TME aspect ratios and TME depths under 200 N load and 2.0 m/s slip linear velocity: (<b>a</b>) TME depth of 5.0 μm, (<b>b</b>) TME depth of 10 μm and (<b>c</b>) TME depth of 20 μm.</p>
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<p>Variation curves of minimum TEHL oil film thickness for different TME depth scale sizes with different interface TME aspect ratios at a load of 200 N and a slip linear velocity of 2.0 m/s.</p>
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<p>Variation curves of MTS maximum contact pressure with interface TME aspect ratio for different interface TME depths.</p>
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<p>Variation curves in MTS contact pressure for different interface TME depth scale sizes for applied loads.</p>
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6 pages, 2771 KiB  
Case Report
Slow Continuous Ultrafiltration in Regional Citrate Anticoagulation Performed with a Standard Fluid Infusion Central Venous Catheter in Intensive Care Unit for Fluid Overload in Acute on Chronic Heart Failure: A Case Report
by Federico Nalesso, Federica Stefanelli, Leda Cattarin, Mariaelena Billo, Maddalena Gnappi, Gabriele Partesano, Martina Cacciapuoti, Luciano Babuin and Lorenzo A. Calò
J. Clin. Med. 2023, 12(3), 988; https://doi.org/10.3390/jcm12030988 - 27 Jan 2023
Cited by 1 | Viewed by 2669
Abstract
Slow continuous ultrafiltration (SCUF) is an extracorporeal therapy able to reduce fluid overload in chronic or acute heart failure resistant to diuretics. An in-vitro study demonstrated the SCUF feasibility using a standard fluid infusion central venous catheter (CVC). We describe the clinical application [...] Read more.
Slow continuous ultrafiltration (SCUF) is an extracorporeal therapy able to reduce fluid overload in chronic or acute heart failure resistant to diuretics. An in-vitro study demonstrated the SCUF feasibility using a standard fluid infusion central venous catheter (CVC). We describe the clinical application of this SCUF in regional citrate anticoagulation (SCUF-RCA) in a patient admitted to the Intensive Care Unit for acute decompensate heart failure with severe systemic fluid overload resistant to diuretics. To avoid risks deriving from a new catheterization, we used a pre-existing multi-lumen CVC for drug administration to provide 10 h of SCUF-RCA with a blood flow of 35 mL/min and 100 mL/h of ultrafiltration with a final weight loss of 1 Kilogram without technical and clinical complications. The patient had a hemodynamics improvement with the diuresis recovery from the previous oliguria after the SCUF-RCA. This clinical case can open the use of the SCUF-RCA in the clinical practice to treat the fluid overload unresponsive to maximal diuretic therapy not exposing the patient to the risks and complications related to the use of SCUF with CVC for dialysis and systemic anticoagulation with heparin. Accordingly, this technique may be useful in the treatment of fluid overload in outpatients. Full article
(This article belongs to the Section Nephrology & Urology)
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Figure 1
<p>The 14 G lumen of the CVC was used as arterial line, and the 16 G lumen as venous line.</p>
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<p>The SCUF with HF-20 set on Prismaflex in regional citrate anticoagulation.</p>
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