[go: up one dir, main page]
More Web Proxy on the site http://driver.im/
You seem to have javascript disabled. Please note that many of the page functionalities won't work as expected without javascript enabled.
 
 
Sign in to use this feature.

Years

Between: -

Subjects

remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline
remove_circle_outline

Journals

Article Types

Countries / Regions

Search Results (129)

Search Parameters:
Keywords = Spatter

Order results
Result details
Results per page
Select all
Export citation of selected articles as:
15 pages, 8003 KiB  
Article
The Ignition Phenomenon and Mechanism of Welding Spatters Under Different Current Intensities
by Feiyue Wang, Litian Wan, Jing Luo and Yanmin Tong
Fire 2024, 7(12), 441; https://doi.org/10.3390/fire7120441 - 28 Nov 2024
Viewed by 520
Abstract
The ignition of combustible materials by electric welding spatters represents a significant cause of fires in welding operations, and the current intensity is a sensitive factor that affects the ignition capacity of welding spatters. In this work, the influence of different current intensities [...] Read more.
The ignition of combustible materials by electric welding spatters represents a significant cause of fires in welding operations, and the current intensity is a sensitive factor that affects the ignition capacity of welding spatters. In this work, the influence of different current intensities on the physical properties and ignition capacity of welding spatters on common combustible materials was investigated, and the ignition mechanism of electric welding spatter was also explained by means of the hot-spot theory. The results indicated that the splash range, the total generated quantity, the maximum diameter, and the temperature of electric welding spatters increased with the enhancement in current intensity. Furthermore, a higher current intensity was associated with a greater likelihood of producing irregular spatter particles. The probability of ignition of electrode welding spatters was found to be sensitive to their physical properties, exhibiting a non-linear increase with increasing current intensity. At a current intensity of 360 A, a surge in both the physical properties and ignition capacity of the spatters was observed, which is attributed to the coupling of a reduction in the critical hot-spot radius and an unstable pulsation in the arc. Full article
(This article belongs to the Special Issue Fire Prevention and Flame Retardant Materials)
Show Figures

Figure 1

Figure 1
<p>Ignition materials and their laying method. (<b>a</b>) Cotton. (<b>b</b>) Foam board. (<b>c</b>) Wood chip. (<b>d</b>) Newspaper.</p>
Full article ">Figure 2
<p>Schematic diagram of the experimental platform.</p>
Full article ">Figure 3
<p>The quantity and the splash range of the spatters under different current intensities.</p>
Full article ">Figure 4
<p>The distribution of the diameter of welding spatters.</p>
Full article ">Figure 5
<p>Shapes of welding spatters.</p>
Full article ">Figure 6
<p>Shape of welding spatters under different current intensities. (<b>a</b>) Shape distribution of the welding spatters under different current intensities. (<b>b</b>) Shape distribution of regular and irregular spatters under different current intensities.</p>
Full article ">Figure 7
<p>Infrared measurements of the temperature of the welding spatters under different current intensities.</p>
Full article ">Figure 8
<p>Temperature variation of the welding spatters with time at different current intensities. (<b>a</b>) Temperature curves under different current intensities. (<b>b</b>) Cooling rate curves under different current intensities.</p>
Full article ">Figure 9
<p>The ability of the welding spatters to ignite the foam board under different current intensities.</p>
Full article ">Figure 10
<p>The ability of the welding spatters to ignite the newspaper under different current intensities.</p>
Full article ">Figure 11
<p>The ability of the welding spatters to ignite the cotton under different current intensities.</p>
Full article ">Figure 12
<p>The ability of the welding spatters to ignite wood chips under different current intensities.</p>
Full article ">Figure 13
<p>Microscopic image of the spatter magnified 50 times under different current intensities.</p>
Full article ">
15 pages, 18440 KiB  
Article
Evaluation of Continuous GMA Welding Characteristics Based on the Copper-Plating Method of Solid Wire Surfaces
by Dong-Yoon Kim and Jiyoung Yu
Metals 2024, 14(11), 1300; https://doi.org/10.3390/met14111300 - 18 Nov 2024
Viewed by 587
Abstract
Gas metal arc welding (GMAW) is widely used in various industries, such as automotive and heavy equipment manufacturing, because of its high productivity and speed, with solid wires being selected based on the mechanical properties required for welded joints. GMAW consists of various [...] Read more.
Gas metal arc welding (GMAW) is widely used in various industries, such as automotive and heavy equipment manufacturing, because of its high productivity and speed, with solid wires being selected based on the mechanical properties required for welded joints. GMAW consists of various components, among which consumables such as the contact tip and continuously fed solid wire have a significant impact on the weld quality. In particular, the copper-plating method can affect the conductivity and arc stability of the solid wire, causing differences in the continuous welding performance. This study evaluated the welding performance during 60 min continuous GMAW using an AWS A5.18 ER70S-3 solid wire, which was copper-plated using chemical plating (C-wire) and electroplating (E-wire). The homogeneity and adhesion of the copper-plated surface of the E-wire were superior to those of the C-wire. The E-wire exhibited better performance in terms of arc stability. The wear rate of the contact tip was approximately 45% higher when using the E-wire for 60 min of welding compared with the C-wire, which was attributed to the larger variation rate in the cast and helix in the E-wire. Additionally, the amount of spatter adhered to the nozzle during 60 min, with the E-wire averaging 5.9 g, approximately half that of the C-wire at 12.9 g. The E-wire exhibits superior arc stability compared with the C-wire based on the spatter amount adhered to the nozzle. This study provides an important reference for understanding the impact of copper plating methods and wire morphology on the replacement cycles of consumable welding parts in automated welding processes such as continuous welding and wire-arc additive manufacturing. Full article
(This article belongs to the Special Issue Welding and Joining of Advanced High-Strength Steels (2nd Edition))
Show Figures

Figure 1

Figure 1
<p>Appearance and specifications of the welding workability evaluation system.</p>
Full article ">Figure 2
<p>Schematic of the welding current and voltage measurement.</p>
Full article ">Figure 3
<p>CT results of solid wire contact condition inside the contact tip during wire feeding.</p>
Full article ">Figure 4
<p>Surface analysis results of the solid wire according to the plating method; drawing direction: (<b>a</b>) C-wire; (<b>b</b>) E-wire; transverse direction; (<b>c</b>) C-wire; (<b>d</b>) E-wire.</p>
Full article ">Figure 5
<p>Analysis of the copper surface homogeneity of the solid wire based on the plating method: (<b>a</b>) C-wire; (<b>b</b>) E-wire.</p>
Full article ">Figure 6
<p>Results of coating adhesion: (<b>a</b>) C-wire; (<b>b</b>) E-wire.</p>
Full article ">Figure 7
<p>Arc stability evaluation for C-wire during 1 h of welding (average current/voltage and standard deviation): (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2.</p>
Full article ">Figure 8
<p>Actual welding current/voltage waveform of C-wire (10 kHz, 10 s): (<b>a</b>) stable welding section (point a); (<b>b</b>) unstable welding section (point b).</p>
Full article ">Figure 9
<p>Analysis of the contact tip and wire after 48.5 min of welding with C-wire #1: (<b>a</b>) the contact tip inside; (<b>b</b>) surface of C-wire after welding.</p>
Full article ">Figure 10
<p>Arc stability evaluation for the E-wire during 1 h of welding (average current/voltage and standard deviation): (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2.</p>
Full article ">Figure 11
<p>Weld appearance during continuous welding: (<b>a</b>) C-wire #1; (<b>b</b>) C-wire #2; (<b>c</b>) E-wire #1; (<b>d</b>) E-wire #2.</p>
Full article ">Figure 12
<p>Appearance of the contact tip end during continuous welding.</p>
Full article ">Figure 13
<p>Nozzle spatter adhesion state by welding time for each solid wire during continuous welding.</p>
Full article ">
11 pages, 3968 KiB  
Article
Comparison of Interfaces Between In Situ Laser Beam Deposition Forming and Electron Beam Welding for Thick-Walled Titanium Alloy Structures
by Pingchuan Yang, Fei Li, Zongtao Zhu and Hui Chen
Micromachines 2024, 15(11), 1383; https://doi.org/10.3390/mi15111383 - 15 Nov 2024
Viewed by 676
Abstract
An investigation was conducted on electron beam-welded and additively manufactured joints on a thick-walled titanium alloy utilizing in situ laser beam deposition and electron beam welding techniques. The surface morphology, microstructural characteristics, and mechanical properties of both joint types were comprehensively analyzed using [...] Read more.
An investigation was conducted on electron beam-welded and additively manufactured joints on a thick-walled titanium alloy utilizing in situ laser beam deposition and electron beam welding techniques. The surface morphology, microstructural characteristics, and mechanical properties of both joint types were comprehensively analyzed using stereomicroscopy, scanning electron microscopy (SEM), microhardness and tensile strength testing, and electron backscatter diffraction (EBSD) techniques. The electron-beam-welded joint exhibited distinct fusion and heat-affected zones, whereas the laser-beam-deposited joint exhibited a smoother surface that was free from excess spatter. Both joints featured a sharp microstructural boundary with a pronounced hardness gradient across the interface, lacking a gradual transition area. During tensile testing, both joint types demonstrated a mixed brittle-ductile fracture mode; however, the electron beam-welded joints surpassed the laser-beam-deposited joints in terms of tensile strength, achieving over 1183 MPa with an elongation of more than 7.3%, compared to 1123 MPa and 5.9% elongation, respectively. Full article
(This article belongs to the Special Issue Future Prospects of Additive Manufacturing)
Show Figures

Figure 1

Figure 1
<p>Schematic diagrams illustrating (<b>a</b>) the EBW of thick titanium plates with a backing plate, (<b>b</b>) additive manufacturing on a forged TC4 plate, (<b>c</b>,<b>d</b>) the location of the regions for metallographic examination and strength testing (viewed from the two cross-sections), and (<b>e</b>) the dimensions of the tensile samples (unit: mm).</p>
Full article ">Figure 2
<p>Microscopic images of base metals: (<b>a</b>–<b>c</b>) microstructure revealed by OM, SEM image, and IPF coloring map of forged TC4, (<b>d</b>–<b>f</b>) microstructure revealed by OM, SEM image, and IPF coloring map of additive-manufactured TC4.</p>
Full article ">Figure 3
<p>The macrostructure of (<b>a</b>) the EB-welded joint and (<b>b</b>) the additive-manufactured joint.</p>
Full article ">Figure 4
<p>OM images of two joints: an overview of (<b>a</b>) the EB-welded joint and (<b>k</b>) the additive-manufactured joint; (<b>b</b>–<b>d</b>), (<b>e</b>–<b>g</b>), and (<b>h</b>–<b>j</b>) represent the top, middle, and bottom of the EB-welded joint, respectively; and (<b>l</b>,<b>m</b>) represents the interface.</p>
Full article ">Figure 5
<p>The microhardness of the (<b>a</b>) EB-welded joint and (<b>b</b>) additive-manufactured joint.</p>
Full article ">Figure 6
<p>(<b>a</b>) The true stress-strain curve and (<b>b</b>) the macroscopic morphology of the fractured samples after the tensile test, from top to bottom: forged TC4, additive-manufactured TC4, top, middle, and bottom of the weld joint, respectively, and the additive-manufactured joint.</p>
Full article ">Figure 7
<p>The Scanning electron microscope fracture morphology of (<b>a</b>,<b>b</b>) the EB-welded joint and (<b>c</b>,<b>d</b>) the additive-manufactured joint.</p>
Full article ">Figure 8
<p>(<b>a</b>–<b>c</b>) IPF maps of the 3D-HAZ, FZ, and Forged-HAZ of the top region of the EB-welded joint, respectively; (<b>d</b>) IPF map for the interface of the additive-manufactured joint; and (<b>e</b>,<b>f</b>) orientation distribution map for the two joints.</p>
Full article ">
17 pages, 11192 KiB  
Article
Microstructure and Mechanical Properties of a Weld Seam from Magnetron High-Current CO2 Welding
by Jun-Yan Miao, Yi-Wen Li, Bo-Wen Ren, Hong-Lei Zhao, Si-Yu Zhang, Yun-Long Chang and Qiang Wang
Crystals 2024, 14(10), 911; https://doi.org/10.3390/cryst14100911 - 21 Oct 2024
Viewed by 885
Abstract
External magnetic field (EMF)-assisted high-current CO2 welding is beneficial for improving the large spatter and poor performance of the welding heat-affected zone for mild steels under high-current welding specifications. In this paper, the droplet transfer behaviors were determined using a high-speed camera [...] Read more.
External magnetic field (EMF)-assisted high-current CO2 welding is beneficial for improving the large spatter and poor performance of the welding heat-affected zone for mild steels under high-current welding specifications. In this paper, the droplet transfer behaviors were determined using a high-speed camera on a self-developed magnetically controlled CO2 welding system. Based on these welding specifications, a three-dimensional, transient, multi-energy field coupling welding system model to investigate the mechanism of the droplet and molten pool in EMF-assisted welding was developed. The microstructure and mechanical properties of the welded joint were systematically studied. The results show that the Lorentz force applied by the EMF to twist the droplet decreases the accumulated energy in the short-circuited liquid bridge and changes the liquid metal flow condition, both of which reduce the spatter by 7% but increase the welded joint hardness by 10% and tensile strength by 8%. Full article
(This article belongs to the Special Issue Surface Modification Treatments of Metallic Materials)
Show Figures

Figure 1

Figure 1
<p>EMF-assisted CO<sub>2</sub> welding platform.</p>
Full article ">Figure 2
<p>Schematic diagram of welded seam section and measurement position, where d, w, and h represent the weld depth, weld width, and weld height, respectively.</p>
Full article ">Figure 3
<p>Droplet model and physical properties.</p>
Full article ">Figure 4
<p>High-speed camera for droplet–molten pool.</p>
Full article ">Figure 5
<p>The change in the weld size under different magnetic field parameters. The red dotted line and the blue dotted line represent the weld depth and the weld height, and the bar graph represents the weld width, where the same color of the bar graph represents the same excitation frequency. In particular, the leftmost black bar represents the weld parameters without the EMF.</p>
Full article ">Figure 6
<p>Comparison between numerical simulation results of weld.</p>
Full article ">Figure 7
<p>Temperature and flow field distributions in the longitudinal section of the molten pool at different moments (no magnetic field on the left, an EMF applied on the right, with Y = 0 mm). (<b>a</b>,<b>f</b>) <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 0.05 s, (<b>b</b>,<b>g</b>) <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 0.30 s, (<b>c</b>,<b>h</b>) <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 0.50 s, (<b>d</b>,<b>i</b>) <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 0.60 s, and (<b>e</b>,<b>j</b>) <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 1.00 s.</p>
Full article ">Figure 8
<p>Force analysis of short-circuit liquid bridge and schematic diagram of molten pool flow. <span class="html-italic">r</span><sub>0</sub> is the radius of the welding wire; <span class="html-italic">r</span><sub>1</sub> is the minimum interface radius after necking of the liquid bridge; <span class="html-italic">r</span><sub>2</sub> is the radius of the contact surface between the liquid bridge and the molten pool.</p>
Full article ">Figure 9
<p>Temperature field and flow field distribution on the surface of the workpiece at <span class="html-italic">t</span> = <span class="html-italic">t</span><sub>0</sub> + 0.80 s (Z = 0 mm). (<b>a</b>) No EMF; (<b>b</b>) EMF.</p>
Full article ">Figure 10
<p>LMF acting on the molten pool.</p>
Full article ">Figure 11
<p>Schematic diagram of the position. (<b>a</b>) Overall view. (<b>b</b>) SEM sampling position. (<b>c</b>) Microstructure of the weld without an EMF. (<b>d</b>) Microstructure of the weld–fusion junction without an EMF. (<b>e</b>) Microstructure of the weld with an EMF. (<b>f</b>) Microstructure of the weld–fusion junction with an EMF.</p>
Full article ">Figure 12
<p>EBSD analysis of weld zone: (<b>a</b>) no EMF IPF, (<b>b</b>) no EMF size angle grain boundary distribution, and (<b>c</b>) no EMF orientation angle distribution; (<b>d</b>) EMF IPF, (<b>e</b>) EMF size angle grain boundary distribution, and (<b>f</b>) EMF orientation angle distribution; (<b>g</b>) no EMF KAM and (<b>h</b>) no EMF KAM distribution; and (<b>i</b>) EMF KAM and (<b>j</b>) EMF KAM distribution.</p>
Full article ">Figure 13
<p>Distribution of weld hardness for different excitation parameters (longitudinal on the left and transverse on the right).</p>
Full article ">Figure 14
<p>Tensile strength of welds with different excitation parameters (excitation current and excitation frequency).</p>
Full article ">
22 pages, 45764 KiB  
Article
Thermography Applied to the Adhesion Phenomenon of Mortars with Additions of Submerged Arc Welding (SAW) Slag
by Érica Sousa, Alef Santana, Millena Moura, João M. P. Q. Delgado and Romildo Berenguer
Buildings 2024, 14(9), 2960; https://doi.org/10.3390/buildings14092960 - 19 Sep 2024
Viewed by 544
Abstract
In this work, the effects of the mixing water loss capacity of hydrated lime mortars with different dosages were analysed—type O (mix 1:2:9), type N (mix 1:1:6), and type M (mix 1:0.5:4.5), with additions of submerged arc welding (SAW) slag. Infrared thermography tests [...] Read more.
In this work, the effects of the mixing water loss capacity of hydrated lime mortars with different dosages were analysed—type O (mix 1:2:9), type N (mix 1:1:6), and type M (mix 1:0.5:4.5), with additions of submerged arc welding (SAW) slag. Infrared thermography tests and optical and scanning electronic microscopy analyses of the mortars were also carried out. The experimental results showed that the mortar samples with additions of SAW slag type M, using low-cost materials, proved to be in economic and technical terms (adhesion strength) the best solution, even more so if a spatter dash layer is used, a fact that increases the adhesion strength even more. Also, the infrared thermographic results revealed that the ability of the mortar paste to yield water to the ceramic substrate in the interface regions is a relevant factor in the adhesion of these coatings. Finally, the analyses by scanning electron microscopy and optical microscopy revealed that the ability to release water to the substrate is related to the hydration of the mortar and its anchoring capacity. Furthermore, the analyses carried out demonstrated that the adhesion of the mortars is influenced and increased with the application of a layer of splashes, as the pores of the substrate become more refined and better filled with the applied mortar. Full article
(This article belongs to the Section Building Materials, and Repair & Renovation)
Show Figures

Figure 1

Figure 1
<p>(<b>a</b>) Mortar applied directly to the ceramic block after 120 min (case T1); (<b>b</b>) Mortar applied on the substrate prepared with spatter dash after 120 min (case T2).</p>
Full article ">Figure 2
<p>Tensile adhesion strength results, after 28 days.</p>
Full article ">Figure 3
<p>(<b>a</b>) Rupture in hydrated lime mortar; (<b>b</b>) Rupture in substrate layer, and (<b>c</b>) Rupture in hydrated lime mortar and spatter dash.</p>
Full article ">Figure 4
<p>(<b>a</b>) Ceramic block thermogram in normal conditions, (<b>b</b>) in laboratory conditions, and (<b>c</b>) submerged in water for 24 h.</p>
Full article ">Figure 5
<p>Thermogram of the mortar frontal view after: (<b>a</b>) 60 min, and (<b>b</b>) 120 min.</p>
Full article ">Figure 6
<p>Thermogram of ceramic blocks: (<b>a</b>) coated with a layer of mortar applied directly to the block (case T1); (<b>b</b>) coated with a layer of spatter dash (case T2).</p>
Full article ">Figure 7
<p>Thermogram of ceramic blocks coated with a mortar layer prepared with a layer of spatter dash, at: (<b>a</b>) 60 min, and (<b>b</b>) 120 min.</p>
Full article ">Figure 8
<p>SEM images of the precursor solid material, cement Portland, with a magnification of: (<b>a</b>) 1.00 kx, (<b>b</b>) 5.00 kx, (<b>c</b>) 15.00 kx, and (<b>d</b>) 30.00 kx.</p>
Full article ">Figure 9
<p>A local energy-dispersive X-ray spectrum (cement Portland).</p>
Full article ">Figure 10
<p>SEM images of the precursor solid material, submerged arc welding (SAW) slag, with magnifications of: (<b>a</b>) 1.00 kx, (<b>b</b>) 5.00 kx, (<b>c</b>) 8.00 kx, and (<b>d</b>) 25.00 kx.</p>
Full article ">Figure 11
<p>A local energy-dispersive X-ray spectrum (submerged arc welding (SAW) slag).</p>
Full article ">Figure 12
<p>SEM images of the precursor solid material, sand, with a magnification of: (<b>a</b>) 1.00 kx, (<b>b</b>) 5.00 kx, (<b>c</b>) 15.00 kx, and (<b>d</b>) 30.00 kx.</p>
Full article ">Figure 13
<p>A local energy-dispersive X-ray spectrum (sand).</p>
Full article ">Figure 14
<p>SEM images of the mortar type O with the following magnifications: (<b>a</b>) 650 x, (<b>b</b>) 5.00 kx, (<b>c</b>) 8.00 kx, and (<b>d</b>) 25.00 kx.</p>
Full article ">Figure 15
<p>Optical microscopy technique of mortar type O with additions of SAW slag: (<b>a</b>) Surface appearance, (<b>b</b>) Quantitative analysis of failures.</p>
Full article ">Figure 16
<p>SEM images of the mortar type M with the following magnifications: (<b>a</b>) 650 x, (<b>b</b>) 5.00 kx, (<b>c</b>) 8.00 kx, and (<b>d</b>) 25.00 kx.</p>
Full article ">Figure 17
<p>Optical microscopy technique of mortar type M additions of SAW slag: (<b>a</b>) Surface appearance, (<b>b</b>) Quantitative analysis of failures.</p>
Full article ">Figure 18
<p>Compositional map of mortar type O.</p>
Full article ">Figure 19
<p>Compositional map of mortar type M.</p>
Full article ">
19 pages, 3334 KiB  
Article
Investigations on the Heat Balance of the Melt Pool during PBF-LB/M under Various Process Gases
by Siegfried Baehr, Fabian Fritz, Stefan Adami, Thomas Ammann, Nikolaus A. Adams and Michael F. Zaeh
Metals 2024, 14(9), 1058; https://doi.org/10.3390/met14091058 - 16 Sep 2024
Viewed by 977
Abstract
During the powder bed fusion of metals using a laser beam (PBF-LB/M), an inert atmosphere is maintained in the build chamber to avoid reactions of the liquid metal with ambient air leading to the creation of oxides or nitrides, which alter the mechanical [...] Read more.
During the powder bed fusion of metals using a laser beam (PBF-LB/M), an inert atmosphere is maintained in the build chamber to avoid reactions of the liquid metal with ambient air leading to the creation of oxides or nitrides, which alter the mechanical properties of the processed part. A continuous gas flow is guided over the process zone to remove spatters and fumes. This flow induces a convective heat transfer from the molten metal to the gas, which, depending on the level of the heat flow, may alter the melt pool dimensions by influencing the cooling rate. The present work investigated these phenomena with single-line trials, both experimentally and numerically. For this reason, a smoothed-particle hydrodynamics model was utilized to investigate the temperatures of the melt pool, cooling rates, and the integral heat balance with various gas atmospheres. In parallel, an on-axis pyrometer was set up on an experimental PBF-LB/M machine to capture the surface emissions of the melt pool. The atmosphere in the simulations and experiments was varied between argon, helium, and two mixtures thereof. The results showed a slight increase in the cooling rates with an increasing fraction of helium in the process gas. Consistently, a slight decrease in the melt pool temperatures and dimensions was found. Full article
(This article belongs to the Special Issue Laser Processing Technology and Principles of Metal Materials)
Show Figures

Figure 1

Figure 1
<p>Cross-sectional view of the computational domain for the PBF-LB/M SPH process simulation. The red area indicates the laser beam. The extend of the domain into the y-direction was <math display="inline"><semantics> <mrow> <mn>25</mn> <mo>×</mo> <msub> <mi>r</mi> <mi>σ</mi> </msub> </mrow> </semantics></math>; negative x: scanning direction.</p>
Full article ">Figure 2
<p>Temperature-dependent material properties for different process gases. (<b>a</b>) a polynomial fit for the thermal conductivity <span class="html-italic">k</span> and (<b>b</b>) a power function for the dynamic viscosity <math display="inline"><semantics> <mi>μ</mi> </semantics></math> for argon (Ar) and helium (He) from <math display="inline"><semantics> <mrow> <mn>300</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">K</mi> </mrow> </semantics></math> to <math display="inline"><semantics> <mrow> <mn>3000</mn> <mspace width="0.166667em"/> <mi mathvariant="normal">K</mi> </mrow> </semantics></math>.</p>
Full article ">Figure 3
<p>Schematic top view of the build plate showing the build job layout (not to scale); x: recoating direction, y: gas flow direction, z: building direction.</p>
Full article ">Figure 4
<p>(<b>a</b>) Cross-sectional view of an etched single line melt pool outlining the measurement of the melt pool width and depth (the melt pool is indicated by a black dotted line), (<b>b</b>) top view of a fabricated cube showing the single lines; z: building direction.</p>
Full article ">Figure 5
<p>Schematic representation of the pyrometry setup.</p>
Full article ">Figure 6
<p>Moving average (mov.avg.) of the mean values of the pyrometer signal depending on the process gas; Ar: argon, He: helium, ArHe30/70: 70/30 vol.-% Ar + 30/70 vol.-% He.</p>
Full article ">Figure 7
<p>Mean values of the melt pool dimensions depending on the process gas; Ar: argon, He: helium, ArHe30/70: 70/30 vol.-% Ar + 30/70 vol.-% He.</p>
Full article ">Figure 8
<p>Cross-sectional view of the melt pool (<span class="html-italic">x</span>-<span class="html-italic">z</span> plane) under various gas flow settings (with and without gas flow) depicting the temperature fields and flow velocity arrows; (<b>a</b>) argon, (<b>b</b>) helium.</p>
Full article ">Figure 9
<p>Cross-sectional view of the melt pool (<span class="html-italic">x</span>-<span class="html-italic">z</span> plane) under various gas flow settings (with and without gas flow) with the absolute temperature rate-of-change fields <math display="inline"><semantics> <mrow> <mo>|</mo> <mover accent="true"> <mi>T</mi> <mo>˙</mo> </mover> <mo>|</mo> </mrow> </semantics></math> in a logarithmic scale; the zones of heating (<math display="inline"><semantics> <mrow> <mover accent="true"> <mi>T</mi> <mo>˙</mo> </mover> <mo>&gt;</mo> <mn>0</mn> </mrow> </semantics></math>) and cooling (<math display="inline"><semantics> <mrow> <mover accent="true"> <mi>T</mi> <mo>˙</mo> </mover> <mo>&lt;</mo> <mn>0</mn> </mrow> </semantics></math>) are separated by the converging iso-contour lines for decreasing values of <math display="inline"><semantics> <mrow> <mo>|</mo> <mover accent="true"> <mi>T</mi> <mo>˙</mo> </mover> <mo>|</mo> </mrow> </semantics></math>, where <math display="inline"><semantics> <mrow> <mo>|</mo> <mover accent="true"> <mi>T</mi> <mo>˙</mo> </mover> <mo>|</mo> </mrow> </semantics></math> approaches zero rapidly; (<b>a</b>) argon, (<b>b</b>) helium.</p>
Full article ">Figure A1
<p>Picture of the AconityMINI PBF-LB/M machine.</p>
Full article ">
21 pages, 7082 KiB  
Article
Dynamic Measurement Method for Steering Wheel Angle of Autonomous Agricultural Vehicles
by Jinyang Li, Zhaozhao Wu, Meiqing Li and Zhijian Shang
Agriculture 2024, 14(9), 1602; https://doi.org/10.3390/agriculture14091602 - 13 Sep 2024
Viewed by 980
Abstract
Steering wheel angle is an important and essential parameter of the navigation control of autonomous wheeled vehicles. At present, the combination of rotary angle sensors and four-link mechanisms is the main sensing approach for steering wheel angle with high measurement accuracy, which is [...] Read more.
Steering wheel angle is an important and essential parameter of the navigation control of autonomous wheeled vehicles. At present, the combination of rotary angle sensors and four-link mechanisms is the main sensing approach for steering wheel angle with high measurement accuracy, which is widely adopted in autonomous agriculture vehicles. However, in a complex and challenging farmland environment, there are a series of prominent problems such as complicated installation and debugging, spattered mud blocking the parallel four-bar mechanism, breakage of the sensor wire during operation, and separate calibrations for different vehicles. To avoid the above problems, a novel dynamic measurement method for steering wheel angle is presented based on vehicle attitude information and a non-contact attitude sensor. First, the working principle of the proposed measurement method and the effect of zero position error on measurement accuracy and path tracking are analyzed. Then, an optimization algorithm for zero position error of steering wheel angle is proposed. The experimental platform is assembled based on a 2ZG-6DM rice transplanter by software design and hardware modification. Finally, comparative tests are conducted to demonstrate the effectiveness and priority of the proposed dynamic sensing method. Experimental results show that the average absolute error of the straight path is 0.057° and the corresponding standard deviation of the error is 0.483°. The average absolute error of the turning path is 0.686° and the standard deviation of the error is 0.931°. This implies the proposed dynamic sensing method can accurately realize the collection of the steering wheel angle. Compared to the traditional measurement method, the proposed dynamic sensing method greatly improves the measurement reliability of the steering wheel angle and avoids complicated installation and debugging of different vehicles. The separate calibrations for different vehicles are not needed since the proposed measurement method is not dependent on the kinematic models of the vehicles. Given that the attitude sensor can be installed at a higher position on the wheel, sensor damage from mud blocking and the sensor wire breaking is also avoided. Full article
(This article belongs to the Section Agricultural Technology)
Show Figures

Figure 1

Figure 1
<p>Problems of steering angle measurement. (<b>a</b>) Complex installation; (<b>b</b>) blocked by spattering soil; (<b>c</b>) recalibration when installing on different vehicles; (<b>d</b>) damage of sensor wire.</p>
Full article ">Figure 2
<p>Installation diagram of steering wheel angle sensor. (<b>a</b>) Steering wheel angle sensor. (<b>b</b>) Installation of steering wheel angle sensor.</p>
Full article ">Figure 3
<p>Schematic diagram of non-contact measuring principle.</p>
Full article ">Figure 4
<p>Schematic diagram of four common situations. (<b>a</b>) The wheel and the vehicle body are both to the right relative to the initial direction; (<b>b</b>) the direction of the wheel is to the right relative to the initial direction while the direction of the body is to the left relative to the initial direction; (<b>c</b>) the direction of the wheel is to the left relative to the initial direction while the direction of the body is to the right relative to the initial direction; (<b>d</b>) the wheel and the vehicle body are both to the left relative to the initial direction.</p>
Full article ">Figure 5
<p>Flowchart of angle value resolver.</p>
Full article ">Figure 6
<p>Diagram of deviation between the steering wheel and vehicle body.</p>
Full article ">Figure 7
<p>Effect of deviation ∆δ on the lateral deviation in steady state.</p>
Full article ">Figure 8
<p>Flowchart of zero error optimization method.</p>
Full article ">Figure 9
<p>Experimental platform. (1) Attitude sensor; (2) Navigation controller; (3) Push rod of gear; (4) Navigation base station; (5) Angle sensor; (6) Vehicle-mounted controller; (7) Electric steering wheel; (8) Navigation mobile station antenna; (9) Navigation data receiver; (10) Serial screen; (11) Data transmission module.</p>
Full article ">Figure 10
<p>Installation schematic diagram of angle sensor. (<b>a</b>) Structure diagram; (<b>b</b>) Installation drawing. 1. Steering shaft; 2. Trellis bar; 3. Angle sensor; 4. Fixed bracket; 5. Fixed link; 6. Ball tie rod.</p>
Full article ">Figure 11
<p>Experiment path.</p>
Full article ">Figure 12
<p>Field test photo.</p>
Full article ">Figure 13
<p>Comparison of experiment results. (<b>a</b>) Variation of lateral deviation; (<b>b</b>) angle output.</p>
Full article ">Figure 14
<p>Segmented amplification of <a href="#agriculture-14-01602-f013" class="html-fig">Figure 13</a>. (<b>a</b>) segmented amplification during 0–260 ms; (<b>b</b>) segmented amplification during 261–340 ms; (<b>c</b>) segmented amplification during 341–555 ms; (<b>d</b>) segmented amplification during 556–625 ms; (<b>e</b>) segmented amplification during 626–828 ms; (<b>f</b>) segmented amplification during 829–880 ms; (<b>g</b>) segmented amplification during 881–1000 ms.</p>
Full article ">Figure 14 Cont.
<p>Segmented amplification of <a href="#agriculture-14-01602-f013" class="html-fig">Figure 13</a>. (<b>a</b>) segmented amplification during 0–260 ms; (<b>b</b>) segmented amplification during 261–340 ms; (<b>c</b>) segmented amplification during 341–555 ms; (<b>d</b>) segmented amplification during 556–625 ms; (<b>e</b>) segmented amplification during 626–828 ms; (<b>f</b>) segmented amplification during 829–880 ms; (<b>g</b>) segmented amplification during 881–1000 ms.</p>
Full article ">Figure 14 Cont.
<p>Segmented amplification of <a href="#agriculture-14-01602-f013" class="html-fig">Figure 13</a>. (<b>a</b>) segmented amplification during 0–260 ms; (<b>b</b>) segmented amplification during 261–340 ms; (<b>c</b>) segmented amplification during 341–555 ms; (<b>d</b>) segmented amplification during 556–625 ms; (<b>e</b>) segmented amplification during 626–828 ms; (<b>f</b>) segmented amplification during 829–880 ms; (<b>g</b>) segmented amplification during 881–1000 ms.</p>
Full article ">
14 pages, 11441 KiB  
Article
Effect of Different Welding Modes on Morphology and Property of SS316L Stainless Steel Deposition by Robotic Metal-Inert Gas Welding
by Wei Wu, Chunjie Wen, Jisheng He, Yanfeng Li, Wei Xu, Ping Yao and Xiangkun Zeng
Materials 2024, 17(18), 4479; https://doi.org/10.3390/ma17184479 - 12 Sep 2024
Viewed by 623
Abstract
The widespread adoption of arc additive manufacturing techniques across various industries has advanced the field of SS316L stainless steel manufacturing. It is crucial to acknowledge that different welding modes exert distinct influences on the forming and mechanical performance. This study analyzed the thermal [...] Read more.
The widespread adoption of arc additive manufacturing techniques across various industries has advanced the field of SS316L stainless steel manufacturing. It is crucial to acknowledge that different welding modes exert distinct influences on the forming and mechanical performance. This study analyzed the thermal input associated with four specific welding modes in LORCH MIG welding, clarifying the transition dynamics of molten droplets through waveform analysis and examining the resultant effects on microstructure and performance characteristics. The Pulse, Speed-Pulse-XT, and Twin-Pulse modes were found to induce spatter during the manufacturing process, consequently reducing molding efficiency in comparison to the SA-XT mode. Notably, the Twin-Pulse mode, characterized by double-pulse agitation, generated fish scale patterns along the lateral surfaces of the fabricated parts, promoting anisotropic grain growth. This microstructural refinement, compared to single-pulse samples with equivalent thermal input, resulted in enhanced mechanical properties. Nevertheless, the horizontal tensile strength of the three pulse modes was lower than the industrial standard for SA-XT mode and forging. In contrast, the SA-XT mode with an average hardness of 168.1 ± 6.9 HV and a tensile strength of 443.58 ± 5.7 MPa. Therefore, while three pulse modes offer certain microstructural advantages, the SA-XT mode demonstrates superior overall performance. Full article
(This article belongs to the Special Issue 3D Printing Technology with Metal Materials)
Show Figures

Figure 1

Figure 1
<p>Test sample cutting position.</p>
Full article ">Figure 2
<p>Waveform of different welding modes: (<b>a</b>) Speed Arc-XT mode; (<b>b</b>) Pulse mode; (<b>c</b>) Twin-Pulse mode; (<b>d</b>) enlarged picture of (<b>c</b>); (<b>e</b>) Speed Pulse-XT mode.</p>
Full article ">Figure 3
<p>Profile morphology of different welding modes.</p>
Full article ">Figure 4
<p>Microstructure of middle section of four modes samples with 1.2mm diameter.</p>
Full article ">Figure 5
<p>Average microhardness of samples.</p>
Full article ">Figure 6
<p>Column chart of tensile results.</p>
Full article ">Figure 7
<p>Microscopic fracture morphologies of tensile samples with different modes.</p>
Full article ">
18 pages, 26175 KiB  
Article
Influence of Scanning Paths on the Weld Pool Behavior, Microstructure, and Mechanical Property of AA2060 Al-Li Alloy Joints by Laser Beam Oscillation Welding
by Yanbo Song, Ying Liang, Hongbing Liu, Luchan Lin, Yanfeng Gao, Hua Zhang and Jin Yang
Coatings 2024, 14(8), 1065; https://doi.org/10.3390/coatings14081065 - 20 Aug 2024
Viewed by 1077
Abstract
In this paper, the laser beam oscillation welding (LBOW) was utilized to weld a 2 mm thick AA2060 aluminum-lithium (Al-Li) alloy plate. The weld pool behaviors under three scanning paths (pure laser, O-shaped, and ∞-shaped) were investigated. It was observed that the O-shaped [...] Read more.
In this paper, the laser beam oscillation welding (LBOW) was utilized to weld a 2 mm thick AA2060 aluminum-lithium (Al-Li) alloy plate. The weld pool behaviors under three scanning paths (pure laser, O-shaped, and ∞-shaped) were investigated. It was observed that the O-shaped scanning path resulted in the most stable welding process. In addition, the weld macroscopic formation, microstructure, and mechanical property between different paths were studied. The results showed that pure laser and ∞-shaped patterns produced welding defects such as spatters and collapse during the welding process, while the O-shaped pattern exhibited good macroscopic formation at varying laser powers. The O-shaped pattern promoted the finest grain in the weld center and reduced the heat input during the welding process. The equiaxed grain zone (EQZ) width of the O-shaped pattern is the smallest compared to the other two patterns at high laser power. In addition to this, the O-shaped pattern could effectively reduce the porosity in the weld. When an O-shaped scanning pattern was adopted at the ideal laser power parameter of 3000 W, the microhardness of the weld center increased by approximately 5.6% compared to pure laser mode. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of the experimental set-up.</p>
Full article ">Figure 2
<p>Schematic diagram of the scanning paths and beam tracks.</p>
Full article ">Figure 3
<p>Schematic diagram of the microhardness.</p>
Full article ">Figure 4
<p>(<b>a</b>) Weld width under different scanning paths and (<b>b</b>) weld depth under different scanning paths.</p>
Full article ">Figure 5
<p>High-speed camera images of 3000 W laser welding: (<b>a</b>) pure laser, (<b>b</b>) O-shaped, and (<b>c</b>) ∞-shaped.</p>
Full article ">Figure 6
<p>High-speed camera view of 3500 W laser welding: (<b>a</b>) pure laser, (<b>b</b>) O-shaped, and (<b>c</b>) ∞-shaped.</p>
Full article ">Figure 7
<p>Schematic diagram of microstructure of Al-Li alloy joint.</p>
Full article ">Figure 8
<p>Typical weld metallograph.</p>
Full article ">Figure 9
<p>SEM of EQZ: (<b>a</b>) 3000 W pure laser, (<b>b)</b> 3000 W O-shaped, (<b>c</b>) 3000 W ∞-shaped, (<b>d</b>) 3500 W pure laser, (<b>e</b>) 3500 W O-shaped, and (<b>f</b>) 3500 W ∞-shaped.</p>
Full article ">Figure 10
<p>SEM of the columnar dendrites at 3000 W. (<b>a</b>) Pure laser, (<b>b</b>) O-shaped, and (<b>c</b>) ∞-shaped.</p>
Full article ">Figure 11
<p>SEM of the equiaxed dendrites at 3000 W. (<b>a</b>) Pure laser, (<b>b</b>) O-shaped, and (<b>c</b>) ∞-shaped.</p>
Full article ">Figure 12
<p>(<b>a</b>) The SEM of EQZ (<b>b</b>,<b>c</b>). The EDS from the zones.</p>
Full article ">Figure 13
<p>EDS mappings for EQZ. (<b>a</b>) Al, (<b>b</b>) Mg, (<b>c</b>) Cu, (<b>d</b>) Zr, (<b>e</b>) Ag, and (<b>f</b>) Zn.</p>
Full article ">Figure 14
<p>(<b>a</b>) The SEM of equiaxed dendrites. (<b>b</b>–<b>e</b>) The EDS from the zones.</p>
Full article ">Figure 15
<p>(<b>a</b>) The SEM of the columnar dendrites. (<b>b</b>,<b>c</b>) The EDS from the zones.</p>
Full article ">Figure 16
<p>(<b>a</b>) The SEM of PMZ. (<b>b</b>,<b>c</b>) The EDS from the zones.</p>
Full article ">Figure 17
<p>Microhardness distribution of welded joints with different scanning paths. (<b>a</b>–<b>f</b>) Samples 1–6; (<b>g</b>) the track and the value of microhardness in sample 2.</p>
Full article ">Figure 18
<p>Schematics of weld pool flow and microstructure formation in the O-shaped laser beam welding process: (<b>a</b>) top-surface; (<b>b</b>) cross-section.</p>
Full article ">
17 pages, 7957 KiB  
Article
Investigating the Influence Mechanism of Different Shielding Gas Types on Arc Characteristics and Weld Quality in TA2 Laser–Arc Hybrid Welding
by Haojie Zhang, Mingyao Shen, Xueqin Tian, Qunli Zhang, Zhijun Chen and Jianhua Yao
Metals 2024, 14(8), 946; https://doi.org/10.3390/met14080946 - 20 Aug 2024
Viewed by 993
Abstract
The effective welding of a 6 mm thick TA2 pure titanium medium-thickness plate was achieved by laser–arc hybrid welding (LAHW) with helium–argon mixed shielding gas. Conducted research on the influence of helium–argon mixed shielding gas on plasma and arc characteristics during welding, and [...] Read more.
The effective welding of a 6 mm thick TA2 pure titanium medium-thickness plate was achieved by laser–arc hybrid welding (LAHW) with helium–argon mixed shielding gas. Conducted research on the influence of helium–argon mixed shielding gas on plasma and arc characteristics during welding, and its further impact on the microstructure, internal porosity defects, tensile properties, and corrosion resistance of welded joints was explored. The study demonstrated that under the shielding gas with 75% helium, the arc width narrowed significantly from 6.96 mm to 2.61 mm, achieving a 63% reduction, which enhanced the concentration of arc heat flux density. Achieved a well-formed weld with no surface spatter and significantly reduced the internal porosity rate from 3.02% to 0.47%, which is an 84% decrease. Tensile fractures are located in the base material, all exhibiting plastic failure. The corrosion resistance of the welded joint initially increased and then decreased with the increase of helium content in the shielding gas, peaking at 75% helium content. Full article
Show Figures

Figure 1

Figure 1
<p>Welding experiment schematic diagram and sampling schematic diagram: (<b>a</b>) Metallographic specimen; (<b>b</b>) electrochemical test specimen; (<b>c</b>) tensile test specimen; (<b>d</b>) slicing plane.</p>
Full article ">Figure 2
<p>Plasma images of different shielding gas laser–arc hybrid welding: (<b>a</b>) 100%Ar; (<b>b</b>) 75%Ar + 25%He; (<b>c</b>) 50%Ar + 50%He; (<b>d</b>) 25%Ar + 75%He; (<b>e</b>) 100%He.</p>
Full article ">Figure 3
<p>The influence of different He contents on the morphology of arc: (<b>a</b>) 100%Ar; (<b>b</b>) 75%Ar + 25%He; (<b>c</b>) 50%Ar + 50%He; (<b>d</b>) 25%Ar + 75%He; (<b>e</b>) 100%He.</p>
Full article ">Figure 4
<p>Effect of different He contents on arc width: (<b>a</b>) Width diagram; (<b>b</b>) arc width.</p>
Full article ">Figure 5
<p>Effect of different He content on arc shape: (<b>a</b>) 100%Ar; (<b>b</b>) 75%Ar + 25%He; (<b>c</b>) 50%Ar + 50%He; (<b>d</b>) 25%Ar + 75%He; (<b>e</b>) 100%He.</p>
Full article ">Figure 6
<p>The distribution of arc heat flux density under different shielding gases.</p>
Full article ">Figure 7
<p>Characteristics of laser–arc hybrid weld formation under different shielding gases: (<b>a</b>) 100%Ar; (<b>b</b>) 75%Ar + 25%He; (<b>c</b>) 50%Ar + 50%He; (<b>d</b>) 25%Ar + 75%He; (<b>e</b>) 100%He.</p>
Full article ">Figure 8
<p>Weld joint cross-sectional morphology: (<b>a</b>) 100%Ar; (<b>b</b>) 75%Ar + 25%He; (<b>c</b>) 50%Ar + 50%He; (<b>d</b>) 25%Ar + 75%He; (<b>e</b>) 100%He.</p>
Full article ">Figure 9
<p>The influence of helium content on weld cross-section.</p>
Full article ">Figure 10
<p>Comparison of the microstructure of argon and helium welded joints: (<b>a</b>) argon arc zone; (<b>b</b>) argon laser zone; (<b>c</b>) helium arc zone; (<b>d</b>) helium laser zone.</p>
Full article ">Figure 11
<p>Pore distribution of welded joints under different shielding gases.</p>
Full article ">Figure 12
<p>Tensile curves of welded joints under different shielding gases.</p>
Full article ">Figure 13
<p>Macroscopic morphology of tensile specimen.</p>
Full article ">Figure 14
<p>Dynamic potential polarization curves of welded joints under different shielding gas.</p>
Full article ">Figure 15
<p>EIS curves of welded joints under different shielding gas and fitted equivalent circuit diagrams: (<b>a</b>) Nyquist curve; (<b>b</b>) Bode curve; (<b>c</b>) fitted equivalent circuit diagrams.</p>
Full article ">
14 pages, 11613 KiB  
Article
Analysis of the Effects of Water Temperature on Water-Assisted Laser Trepanning in Superalloys
by Kaibo Xia, Liang Wang, Mingchao Li and Huayu Yang
Metals 2024, 14(8), 943; https://doi.org/10.3390/met14080943 - 19 Aug 2024
Viewed by 844
Abstract
The water-assisted laser trepanning method has been proven to improve the quality of laser drilling; however, the effect of water temperature on this process is currently unclear. In order to investigate the influence of water temperature on the quality of holes produced via [...] Read more.
The water-assisted laser trepanning method has been proven to improve the quality of laser drilling; however, the effect of water temperature on this process is currently unclear. In order to investigate the influence of water temperature on the quality of holes produced via water-assisted laser trepanning in superalloys, this study used the controlled variable method to investigate the effects of three water temperatures—low temperature (2 °C), normal temperature (20 °C), and high temperature (70 °C)—on the following factors: spatter, hole diameter, taper angle, hole sidewall morphology, and recast layer. The results show that the spatter around the hole reduced, the hole entrance/exit diameter increased, and the roughness of the hole’s sidewall decreased with an increase in single-pulse energy. However, the effect of single-pulse energy on the recast layer was not obvious. As the temperature of the water increased, the hole entrance/exit diameter increased, and the roughness of the hole’s sidewall decreased. When the single-pulse energy was 1.0–1.9 J, using a lower water temperature produced a hole with a smaller taper angle. Compared with a water temperature of 20 °C, the movement of the melt film on the hole’s sidewall accelerated when the water temperature was 70 °C; as a result, more molten material could be removed from the hole, resulting in a decrease in the thickness of the recast layer. However, when the water temperature was 2 °C, the heat-affected zone and the thickness of the recast layer decreased more significantly. The results of this study provide technical support for the optimization of water-assisted laser drilling. Full article
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of the water-assisted millisecond laser trepanning method: (<b>a</b>) scanning path; (<b>b</b>) water-assisted laser drilling.</p>
Full article ">Figure 2
<p>Effect of single-pulse energy on spatter at the entrance of microholes at different water temperatures: (<b>a</b>) 2 °C; (<b>b</b>) 20 °C; and (<b>c</b>) 70 °C.</p>
Full article ">Figure 3
<p>Effect of single-pulse energy on the morphology of microholes’ entrance and exit at different water temperatures: (<b>a</b>) 2 °C; (<b>b</b>) 20 °C; and (<b>c</b>) 70 °C.</p>
Full article ">Figure 4
<p>Effect of single-pulse energy on microhole diameters: (<b>a</b>) hole entrance; (<b>b</b>) hole exit.</p>
Full article ">Figure 5
<p>Effect of single-pulse energy on the hole cross-section morphology at different water temperatures: (<b>a</b>) 2 °C; (<b>b</b>) 20 °C; and (<b>c</b>) 70 °C.</p>
Full article ">Figure 6
<p>Effect of single-pulse energy on microholes’ taper angles.</p>
Full article ">Figure 7
<p>CLSM 2D morphology of different areas on the hole sidewall at different water temperatures: (<b>a</b>) 2 °C, (<b>b</b>) 20 °C, and (<b>c</b>) 70 °C.</p>
Full article ">Figure 8
<p>CLSM 3D morphology of different areas of hole sidewall at different water temperatures: (<b>a</b>) 2 °C, (<b>b</b>) 20 °C, and (<b>c</b>) 70 °C.</p>
Full article ">Figure 9
<p>CLSM 2D morphology of the middle of the hole wall at a single-pulse energy of 1.9 J and various temperatures: (<b>a</b>) 2 °C; (<b>b</b>) 20 °C; and (<b>c</b>) 70 °C.</p>
Full article ">Figure 10
<p>Effect of single-pulse energy on the roughness of different areas on the hole sidewall: (<b>a</b>) hole entrance; (<b>b</b>) hole middle; and (<b>c</b>) hole exit.</p>
Full article ">Figure 11
<p>The thickness of the recast layer at different areas of the hole wall at different water temperatures: (<b>a</b>) 2 °C, (<b>b</b>) 20 °C, and (<b>c</b>) 70 °C.</p>
Full article ">Figure 12
<p>Effect of single-pulse energy on hole recast layer: (<b>a</b>) hole entrance; (<b>b</b>) hole middle; and (<b>c</b>) hole exit.</p>
Full article ">Figure 13
<p>Schematic of water-assisted millisecond laser trepanning: (<b>a</b>) 2 °C; (<b>b</b>) 20 °C; and (<b>c</b>) 70 °C.</p>
Full article ">
17 pages, 12847 KiB  
Article
Influence of Pd-Layer Thickness on Bonding Reliability of Pd-Coated Cu Wire
by Junling Fan, Donglin Yuan, Juan Du, Tao Hou, Furong Wang, Jun Cao, Xuemei Yang and Yuemin Zhang
Micromachines 2024, 15(7), 931; https://doi.org/10.3390/mi15070931 - 22 Jul 2024
Cited by 2 | Viewed by 907
Abstract
In this paper, three Pd-coated Cu (PCC) wires with different Pd-layer thicknesses were used to make bonding samples, and the influence of Pd-layer thickness on the reliability of bonded points before and after a high-temperature storage test was studied. The results show that [...] Read more.
In this paper, three Pd-coated Cu (PCC) wires with different Pd-layer thicknesses were used to make bonding samples, and the influence of Pd-layer thickness on the reliability of bonded points before and after a high-temperature storage test was studied. The results show that smaller bonding pressure and ultrasonic power lead to insufficient plastic deformation of the ball-bonded point, which also leads to small contact area with the pad and low bonding strength. Excessive bonding pressure and ultrasonic power will lead to ‘scratch’ on the surface of the pad and large-scale Ag spatter. The wedge-bonded point has a narrowed width when the bonding pressure and ultrasonic power are too small, and the tail edge will be cocked, resulting in false bonding and low strength. When the bonding pressure or ultrasonic power is too large, it will cause stress concentration, and the pad will appear as an ‘internal injury’, which will improve the failure probability; a high-temperature environment can make Cu-Ag intermetallic compounds (IMCs) grow and improve the bonding strength. With the extension of high-temperature storage time, the shear force of Pd100 gradually reaches the peak and then decreases, due to Kirkendall pores caused by excessive growth of IMCs, while the shear force of Pd120 continued to increase due to the slow growth rate of IMCs. In the high-temperature storage test, the thicker the Pd layer of the bonding wire, the higher the bonding strength; in the cold/hot cycle test, the sample with the largest Pd-layer thickness has the lowest failure rate. The thicker the Pd layer, the stronger its ability to resist changes in the external environment, and the higher its stability and reliability. Full article
(This article belongs to the Special Issue MEMS Packaging Technologies and 3D Integration, 3rd Edition)
Show Figures

Figure 1

Figure 1
<p>Ball-thrust/wire-breaking force test. ((<b>a</b>) Schematic diagram of shear force test of ball-bonded point; (<b>b</b>) schematic diagram of wire-breaking force test.)</p>
Full article ">Figure 2
<p>Sample failure inspection.</p>
Full article ">Figure 3
<p>Shear force of Pd80 ball-bonded point under different bonding parameters.</p>
Full article ">Figure 4
<p>Morphology of Pd80 ball-bonded points under different bonding pressure/ultrasonic power. ((<b>a</b>) 40 g/110 mW; (<b>b</b>) 40 g/100 mW; (<b>c</b>) 40 g/120 mW; (<b>d</b>) 35 g/110 mW; (<b>e</b>) 45 g/110 mW).</p>
Full article ">Figure 4 Cont.
<p>Morphology of Pd80 ball-bonded points under different bonding pressure/ultrasonic power. ((<b>a</b>) 40 g/110 mW; (<b>b</b>) 40 g/100 mW; (<b>c</b>) 40 g/120 mW; (<b>d</b>) 35 g/110 mW; (<b>e</b>) 45 g/110 mW).</p>
Full article ">Figure 5
<p>Morphology of Pd80 wedge-bonded points under different bonding pressure/ultrasonic power ((<b>a</b>) 45 g/105 mW; (<b>b</b>) 45 g/95 mW; (<b>c</b>) 45 g/115 mW; (<b>d</b>) 40 g/105 mW; (<b>e</b>) 50 g/105 mW).</p>
Full article ">Figure 6
<p>Shear of ball-bonded point with different combined bonding parameters.</p>
Full article ">Figure 7
<p>Morphology of Pd100 ball joints under different bonding pressures/ultrasonic power ((<b>a</b>) 45 g/115 mW; (<b>b</b>) 45 g/105 mW; (<b>c</b>) 45 g/125 mW; (<b>d</b>) 50 g/115 mW).</p>
Full article ">Figure 8
<p>Morphology of Pd100 wedge-bonded points under different bonding pressures/ultrasonic power ((<b>a</b>) 50 g/110 mW; (<b>b</b>) 50 g/100 mW; (<b>c</b>) 50 g/120 mW; (<b>d</b>) 45 g/110 mW; (<b>e</b>) 55 g/110 mW).</p>
Full article ">Figure 9
<p>Shear of ball-bonded points with different combined bonding parameters.</p>
Full article ">Figure 10
<p>Morphology of Pd120 ball-bonded points under different bonding pressures/ultrasonic power ((<b>a</b>) 50 g/120 mW; (<b>b</b>) 50 g/110 mW; (<b>c</b>) 50 g/130 mW; (<b>d</b>) 55 g/120 mW).</p>
Full article ">Figure 10 Cont.
<p>Morphology of Pd120 ball-bonded points under different bonding pressures/ultrasonic power ((<b>a</b>) 50 g/120 mW; (<b>b</b>) 50 g/110 mW; (<b>c</b>) 50 g/130 mW; (<b>d</b>) 55 g/120 mW).</p>
Full article ">Figure 11
<p>Morphology of Pd120 wedge-bonded points under different bonding pressures/ultrasonic power ((<b>a</b>) 55 g/115 mW; (<b>b</b>) 55 g/105 mW; (<b>c</b>) 55 g/125 mW; (<b>d</b>) 50 g/115 mW; (<b>e</b>) 60 g/115 mW).</p>
Full article ">Figure 12
<p>Tensile force of bonded point under different high-temperature storage times.</p>
Full article ">Figure 13
<p>Shear force of ball-bonded point under different high-temperature storage times.</p>
Full article ">Figure 14
<p>Breakpoint position proportion under different high-temperature storage times.</p>
Full article ">Figure 15
<p>Partition of bonding interface.</p>
Full article ">Figure 16
<p>Sample failure rate under different cold/hot cycles.</p>
Full article ">
16 pages, 15661 KiB  
Article
Research on the Welding Process and Weld Formation in Multiple Solid-Flux Cored Wires Arc Hybrid Welding Process for Q960E Ultrahigh-Strength Steel
by Ting Xiang, Mingrui Zhang, Qiang Ma, Zhenlong Fang, Huan Li and Hao Wang
Materials 2024, 17(13), 3178; https://doi.org/10.3390/ma17133178 - 28 Jun 2024
Cited by 1 | Viewed by 565
Abstract
This paper proposes a novel welding process for ultrahigh-strength steel. The effects of welding parameters on the welding process and weld formation were studied to obtain the optimal parameter window. It was found that the metal transfer modes of solid wires were primarily [...] Read more.
This paper proposes a novel welding process for ultrahigh-strength steel. The effects of welding parameters on the welding process and weld formation were studied to obtain the optimal parameter window. It was found that the metal transfer modes of solid wires were primarily determined by electrical parameters, while flux-cored wires consistently exhibited multiple droplets per pulse. The one droplet per pulse possessed better welding stability and weld formation, whereas the short-circuiting transfer or one droplet multiple pulses easily caused abnormal arc ignition that decreased welding stability, which could easily lead to a “sawtooth-shaped” weld formation or weld offset towards one side with more spatters. Thus, the electrical parameters corresponding to one droplet per pulse were identified as the optimal parameter window. Furthermore, the weld zone (WZ) was predominantly composed of AF, and the heat-affected zone (HAZ) primarily consisted of TM and LM. Consequently, the welded joint still exhibited excellent mechanical properties, particularly toughness, despite higher welding heat input. The average tensile strength reached 928 MPa, and the impact absorbed energy at −40 °C for the WZ and HAZ were 54 J and 126 J, respectively. In addition, the application of triple-wire welding for ultrahigh-strength steel (UHSS) demonstrated a significant enhancement in post-weld deposition rate, with increases of 106% and 38% compared to single-wire and twin-wire welding techniques, respectively. This process not only utilized flux-cored wire to enhance the mechanical properties of joints but also achieved high deposition rate welding. Full article
Show Figures

Figure 1

Figure 1
<p>Initial microstructure of Q960E: (<b>a</b>) optical microscopy (OM) and (<b>b</b>) scanning electron microscopy (SEM).</p>
Full article ">Figure 2
<p>Schematic diagram of the welding system.</p>
Full article ">Figure 3
<p>Corresponding relationship between the three-wire arrangement and the positions in high-speed photograph.</p>
Full article ">Figure 4
<p>Groove dimensions of butt welding.</p>
Full article ">Figure 5
<p>Dimensions of specimens for mechanical property test: (<b>a</b>) impact specimen and (<b>b</b>) tensile specimen.</p>
Full article ">Figure 6
<p>Electrical signals and high-speed photographs at different preset voltages: (<b>a</b>) preset voltage of 22 V, (<b>b</b>) preset voltage of 26 V, and (<b>c</b>) preset voltage of 30 V.</p>
Full article ">Figure 7
<p>Effect of preset voltage on metal transfer frequency.</p>
Full article ">Figure 8
<p>Electrical signals and high-speed photographs at different preset currents: (<b>a</b>) preset current of 160 A and (<b>b</b>) preset current of 180 A.</p>
Full article ">Figure 9
<p>Effect of preset current on metal transfer frequency.</p>
Full article ">Figure 10
<p>Arcing and metal transfer mode for multiple solid-flux cored wires arc hybrid welding.</p>
Full article ">Figure 11
<p>Effect of different preset voltages on weld formation: (<b>a</b>) preset voltage of 22 V, (<b>b</b>) preset voltage of 26 V, (<b>c</b>) preset voltage of 30 V, and (<b>d</b>) weld size.</p>
Full article ">Figure 12
<p>Effect of preset currents on weld formation: (<b>a</b>) preset current of 140 A, (<b>b</b>) preset current of 160 A, (<b>c</b>) preset current of 180 A, and (<b>d</b>) weld size.</p>
Full article ">Figure 13
<p>Optimal parameter window for the welding process.</p>
Full article ">Figure 14
<p>Cross-section profile of the welded joint.</p>
Full article ">Figure 15
<p>Microstructures observed via OM and SEM in different sub-zones for the upper part of the joint: (<b>a</b>,<b>b</b>) evolution within each subzone, (<b>c</b>,<b>d</b>) weld zone (WZ), (<b>e</b>,<b>f</b>) coarse-grained HAZ (CGHAZ), (<b>g</b>,<b>h</b>) fine-grained HAZ (FGHAZ), (<b>i</b>,<b>j</b>) intercritical HAZ (ICHAZ), and (<b>k</b>,<b>l</b>) subcritical HAZ (SCHAZ).</p>
Full article ">Figure 16
<p>Spectrum of inclusion nucleating acicular ferrite.</p>
Full article ">Figure 17
<p>Microhardness distribution characteristics of the joint.</p>
Full article ">Figure 18
<p>Fracture location and macro- and microfracture morphologies of the tensile specimens: (<b>a</b>) fracture location; (<b>b</b>) macroscopic fracture; (<b>c</b>) microscopic fracture.</p>
Full article ">Figure 19
<p>Macroscopic and microscopic-fractured surfaces of WZ after Charpy impact testing at −40 °C: (<b>a</b>) macroscopic fracture, (<b>b</b>) ductile fracture region, and (<b>c</b>) quasi-cleavage fracture region.</p>
Full article ">Figure 20
<p>Macroscopic and microscopic-fractured surfaces of HAZ after Charpy impact testing at −40 °C: (<b>a</b>) macroscopic fracture, (<b>b</b>) ductile fracture region, and (<b>c</b>) quasi-cleavage fracture region.</p>
Full article ">
15 pages, 6576 KiB  
Article
Optimization of the Laser Drilling Processing Parameters for Carbon Steel Based on Multi-Physics Simulation
by Shanqing Liang, Fengxian Li, Yichun Liu, Jianhong Yi and Jürgen Eckert
Metals 2024, 14(6), 682; https://doi.org/10.3390/met14060682 - 8 Jun 2024
Viewed by 1313
Abstract
The laser drilling of carbon steel is always suffered from the formation of slag, the presence of cutting burrs, the generation of a significant quantity of spatter, and the incomplete penetration of the substrate. In order to avoid these defects formed during the [...] Read more.
The laser drilling of carbon steel is always suffered from the formation of slag, the presence of cutting burrs, the generation of a significant quantity of spatter, and the incomplete penetration of the substrate. In order to avoid these defects formed during the laser drilling of carbon steel, the COMSOL multi-physics simulation method was used to model and optimize the laser drilling process. Considering the splash evolution of the material during the complex drilling process, the transient evolution of the temperature field, the flow of the molten fluid, the geometrical changes, and the absorption of the laser energy during the laser drilling process were investigated. The simulated borehole dimensions are consistent with the experimental results. The process parameters have a great influence on the fluid flow pattern and material slag splashing. The laser power has a significant effect on the laser processing compared with the process parameters. With the increase in laser power and the decrease in laser heat source radius, the time required for perforation is reduced, the flow of melt is accelerated, the perforation efficiency is increased, and the hole wall is smoother, but the degree of spattering is greater. The optimized process parameters were obtained: laser heat source radius of 0.3 mm, laser power of 3000 W. These findings can help reduce the machining defects in carbon steel with excellent mechanical properties by optimizing the laser drilling processing parameters. Full article
Show Figures

Figure 1

Figure 1
<p>A photo of the G4020MF fiber laser cutting machine and the machining head.</p>
Full article ">Figure 2
<p>The effect of actual laser drilling of carbon steel at different laser powers: (<b>a</b>) the laser power is too low, and the molten liquid does not reach the complete melting state; (<b>b</b>) the laser power is too high, and the molten liquid produces a lot of slag splashing.</p>
Full article ">Figure 3
<p>Temperature distribution within the field at distinct time intervals: (<b>a</b>) at 30 ms, (<b>b</b>) at 80ms, and (<b>c</b>) near the perforation point under a constant power laser. (<b>d</b>–<b>f</b>) Corresponding flow field under the same conditions.</p>
Full article ">Figure 4
<p>Isothermal line distribution during laser drilling: (<b>a</b>) at 30ms and (<b>b</b>) near the perforation point under a constant power laser.</p>
Full article ">Figure 5
<p>The width of the molten pool changed with time in the laser drilling process.</p>
Full article ">Figure 6
<p>Comparison of the depth of laser perforation under different laser powers at the same time: (<b>a</b>) 1200 W, (<b>b</b>) 2000 W, (<b>c</b>) 3000 W, and (<b>d</b>) 3500 W.</p>
Full article ">Figure 7
<p>Changes in fluid volume fraction at the same time of laser drilling under different laser powers: (<b>a</b>) 1200 W, unable to penetrate; (<b>b</b>) 2000 W, slow processing; (<b>c</b>) 3000 W, the surface is flat; (<b>d</b>) 3500 W, the surface begins to deform.</p>
Full article ">Figure 8
<p>Comparison of the hole depth over time under different laser powers.</p>
Full article ">Figure 9
<p>Depth of the hole processed by laser drilling under different laser heat source radii: (<b>a</b>) 0.5 mm, processing depth of 0.15 mm, (<b>b</b>) 0.40 mm, processing depth of 0.55 mm, (<b>c</b>) 0.30 mm, processing depth of 1.20 mm, and (<b>d</b>) 0.15 mm, processing depth of 2.45 mm.</p>
Full article ">Figure 10
<p>Variation in fluid volume fraction of the molten liquid under different radii of the laser heat source at the same time: (<b>a</b>) 0.5 mm, (<b>b</b>) 0.40 mm, (<b>c</b>) 0.30 mm, (<b>d</b>) 0.15 mm.</p>
Full article ">Figure 11
<p>Variation in the width dimension of the holes with time during laser drilling processing.</p>
Full article ">Figure 12
<p>Laser-drilled sample prepared under the optimized laser perforation process parameters: (<b>a</b>) perforated surface, (<b>b</b>) perforated section.</p>
Full article ">
17 pages, 8561 KiB  
Article
Effects of Beam Mode on Hole Properties in Laser Processing
by Tingzhong Zhang, Hui Li, Chengguang Zhang and Aili Zhang
Coatings 2024, 14(5), 594; https://doi.org/10.3390/coatings14050594 - 9 May 2024
Cited by 1 | Viewed by 1527
Abstract
The laser beam mode affects the power density distribution on the irradiated target, directly influencing the product quality in laser processing, especially the hole quality in laser drilling. The Gaussian beam shape, Mexican-Hat beam shape, Double-Hump beam shape, and Top-Hat beam shape are [...] Read more.
The laser beam mode affects the power density distribution on the irradiated target, directly influencing the product quality in laser processing, especially the hole quality in laser drilling. The Gaussian beam shape, Mexican-Hat beam shape, Double-Hump beam shape, and Top-Hat beam shape are four typical laser beam modes used as a laser heat source and introduced into our proficient laser-drilling model, which involves complex physical phenomena such as heat and mass transfer, solid/liquid/gas phase changes, and two-phase flow. Simulations were conducted on an aluminum target, and the accuracy was verified using experimental data. The results of the simulations for the fundamental understanding of this laser–material interaction are presented in this paper; in particular, the hole shape, including the depth–diameter ratio and the angle of the cone, as well as spatter phenomena and, thus, the formed recast layer, are compared and analyzed in detail in this paper. This study can provide a reference for the optimization of the laser-drilling process, especially the selection of laser beam mode. Full article
(This article belongs to the Special Issue Recent Development in Post-processing for Additive Manufacturing)
Show Figures

Figure 1

Figure 1
<p>Schematic diagram of laser drilling and corresponding boundary conditions.</p>
Full article ">Figure 2
<p>Intensity distribution of four different laser beam modes: (<b>a</b>) GS, (<b>b</b>) MH, (<b>c</b>) DH, and (<b>d</b>) TH along the <span class="html-italic">x</span> axis.</p>
Full article ">Figure 3
<p>Comparison of the predicted and the physical hole cross sections for three different laser beam modes: (<b>a</b>) GS, (<b>b</b>) TH, and (<b>c</b>) DH.</p>
Full article ">Figure 4
<p>Sequences of penetrating hole at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in laser-drilled aluminum under GS mode. (The red is air, and the blue is the target).</p>
Full article ">Figure 5
<p>Sequences of the temperature field of the melt pool and spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under GS mode.</p>
Full article ">Figure 6
<p>Sequences of the velocity field of the melt pool and spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under GS mode.</p>
Full article ">Figure 7
<p>Sequences of the liquid layer (in red) with the hole evolution at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under GS mode.</p>
Full article ">Figure 8
<p>Sequences of the horn-shaped hole at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under MH mode. (The red is air and the blue is the target).</p>
Full article ">Figure 9
<p>Sequences of the temperature field of the melt pool and spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under MH mode.</p>
Full article ">Figure 10
<p>Sequences of the velocity field of the melt pool and the spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under MH mode.</p>
Full article ">Figure 11
<p>Sequences of the horn-shaped liquid layer (the red) with the hole evolution at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under MH mode.</p>
Full article ">Figure 12
<p>Sequences of the W-shaped hole at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under DH mode. (The red is air and the blue is the target).</p>
Full article ">Figure 13
<p>Sequences of the temperature field of the melt pool and star-shaped spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under DH mode.</p>
Full article ">Figure 14
<p>Sequences of the velocity field of the melt pool and the star-shaped spatter phenomena at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under DH mode.</p>
Full article ">Figure 15
<p>Sequences of the W-shaped liquid layer (red) with the hole evolution at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under DH mode.</p>
Full article ">Figure 16
<p>Sequences of the U-shaped hole at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under TH mode. (The red is air and the blue is the target).</p>
Full article ">Figure 17
<p>Sequences of the temperature field of the melt pool and vase-shaped spatter at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under TH mode.</p>
Full article ">Figure 18
<p>Sequences of the velocity field of the melt pool and the vase-shaped spatter at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under TH mode.</p>
Full article ">Figure 19
<p>Sequences of U-shaped liquid layer (red) with the hole evolution at the moments of (<b>a</b>) 100 μs, (<b>b</b>) 300 μs, (<b>c</b>) 500 μs, (<b>d</b>) 700 μs, (<b>e</b>) 900 μs, and (<b>f</b>) 1000 μs in the laser drilling of aluminum under TH mode.</p>
Full article ">
Back to TopTop