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Article

Performance of the GH4169 Joint Using a Novel Ni-Based Amorphous Brazing Filler Metal

by
Xiaohong Yang
1,*,
Kaitao Zhu
2,
Dan Huang
3 and
Lin Yang
1
1
Academician Workstation, Jinhua University of Vocational Technology, Jinhua 321017, China
2
School of Mechanical Engineering, Zhejiang University of Technology, Hangzhou 310000, China
3
Taizhou Institute of Product Quality and Safety Inspection, Taizhou 318000, China
*
Author to whom correspondence should be addressed.
Metals 2024, 14(11), 1274; https://doi.org/10.3390/met14111274
Submission received: 14 September 2024 / Revised: 24 October 2024 / Accepted: 7 November 2024 / Published: 9 November 2024
(This article belongs to the Special Issue Brazing and Diffusion Welding of New Materials and Dissimilar Materials)
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Abstract

:
A novel Ni-Cr-Si-B filler metal (JNi-5) was designed and further fabricated into the amorphous brazing filler metal for joining the GH4169 alloy. The effect of brazing temperature on the microstructure and mechanical properties of GH4169 joints was investigated. The typical microstructure of the joint at 1030 °C is composed of four specific zones: the base metal (BM), heat-affected zone (HAZ), isothermal solidification zone (ISZ), and athermal solidification zone (ASZ). The typical microstructure of the joint is GH4169/(Nb, Mo)-rich boride+(Cr, Nb, Mo)-rich boride/γ(Ni)/Ni-rich boride+γ(Ni)/γ(Ni)/(Cr, Nb, Mo)-rich boride+(Nb, Mo)-rich boride/GH4169. As the temperature increased, the HAZ continued to widen and the ASZ depleted at 1090 °C and 1120 °C. Additionally, the borides within the HAZ coarsened at temperatures of 1090 °C and 1120 °C. At 1030 °C, the fracture path is in the ASZ, and the existence of the brittle phase in the ASZ provides the potential origin for crack growth. The fracture mode is a quasi-cleavage fracture. At 1060 °C, 1090 °C, and 1120 °C, the fracture behavior mainly happened in the HAZ, and the existence of borides in the HAZ provides the potential origin for crack growth. Namely, the shear strength of joints was principally dominated by the brittle precipitations in the HAZ. The fracture mode of these joints is the hybrid ductile. At 1060 °C, the shear strength of the obtained joint is the highest value (693.78 MPa) due to the volume fraction increase in the Ni-based solid solution. Finally, the optimized brazing parameter of 1060 °C/10 min was determined, and the corresponding highest shear strength of 693.78 MPa was obtained owing to the increased content of the Ni-based solid solution in the joint.

1. Introduction

Recently, in the field of aerospace, increasing the thrust-to-weight ratio of aircraft engines has been an effective means to improve the efficiency of spacecraft operations [1,2]. However, these methods may have adverse effects on high-temperature materials, such as thermal stresses and fatigue cracks, which may lead to engine failures [3,4]. To avoid these glitches happening in the engines, choosing an alloy with high purity and excellent properties is key in the design of advanced engines. The GH4169 alloy, a typical precipitation hardening Ni-based superalloy, offers advantages such as high yield strength and good weldability, making it a preferred material in engine design [5,6,7]. The GH4169 alloy has been used in fabricating important components in aircraft engines, such as critical rotating parts, airfoils, and pressure vessels, which account for more than 30% of the engines [8]. Brazing technology is usually used to achieve the welding of structurally complex GH4169 parts, such as nozzle guide vanes and turbine blades. Braze, as a precise connection technology, could accommodate the assembly requirements of heated end components above and thus becomes the only option for the connection of some engine components. This technology has advantages such as a simple production process and low residual stress, overcoming the problems of material cracking and heat-affected zones in traditional welding [9,10].
Ni-based filler metal is usually used to connect the GH4169 heated components, and its unique chemical composition leads to the brazed joint having excellent anti-corrosion and mechanical properties [11]. Lin Yuan et al. [12] used BNi-2 powder filler metal to braze Inconel 718 and FeCoNiAlTi. Binesh et al. [13] used MBF-15 Ni-based foil filler metal to connect Inconel 738LC. The results show that the microstructure of the brazed joint is composed of an isothermal solidification zone (ISZ), an athermal solidification zone (ASZ), and a heat-affected zone (HAZ). The eutectic structure and Ni3Si particles are distributed in the ASZ. The fracture path shows that cracks extend along these brittle phases, which reveals that the ASZ is the weakest zone by an external force. Dong et al. [14] designed a novel Ni-based filler metal and fabricated it into an amorphous brazing filler metal. Then, using this amorphous filler metal to join the GH4169 alloy, a brazed joint consisting of ISZ and HAZ regions was obtained. The amorphous brazing filler metal has been widely used to join Ni alloys. For example, the Ti21.25Zr25Ni25Cu18.75 (at.%) was used for joining K4169 and TiAl alloys [15]. The highest shear strength of the joints reached 322 MPa when brazed at 1030 °C/10 min. Xie Chenlang [16] developed a family of Ni-based amorphous alloys for joining the GH3230 Ni-based superalloy. The optimized tensile strength of the joints was 860 MPa. Based on the research above, traditional Ni-based powder filler metal suffers from assembly misalignment, the overflow of liquid filler metal, and adhesive contamination during the brazing process [17,18]. However, the amorphous brazing filler metal, produced by the rapid solidification technique, could well overcome these disadvantages of traditional filler metal [19]. Moreover, with the rapid development of superalloys, it has become difficult to obtain joints with uniform microstructure by adjusting brazing parameters for standard brazing materials such as BNi-2 and MBF-15 [20,21]. Research has shown that specially designed novel Ni-based filler metals are widely used in high-temperature alloy brazing due to their superior properties [22,23]. Therefore, designing Ni-based brazing material for the connection of heated end pieces of GH4169 alloy and using rapid solidification technology to prepare the filler metal into a ductile amorphous foil is of great significance for advancing the aerospace field.
In this paper, the novel Ni-Cr-Si-B filler metal (JNi-5) was designed by reducing the content of Si and B and adding special alloy elements (Co and Y). The elements of B and Si are usually considered as the melting point depressants in the filler metal to lower the brazing temperatures [24,25]. However, the excessive addition of them might produce massive brittle phases of borides and silicides, increasing the possibility of joint brittle fracture while severely reducing its reliability. Therefore, appropriately reducing the content of B and Si in the filler is expected to restrain the formation of brittle compounds [26] while joining the GH4169 alloy at lower temperatures. Moreover, the addition of Co and Y can enhance the joint bonding strength through solid strengthening effects.
It has been known that Co and Ni share ultimate solubility with each other. In this study, the added Co elements are expected to reduce the melting point of the filler metal to some extent and mitigate the possible thermal damage to the base material. Moreover, the Co elements are dissolved in the Ni-based solid solution within the joint, which enhances the solution-strengthening effects and thereby strengthens the brazed joint. Based on prior analysis, one can know that the addition of Y in the filler metal could enhance the ductility and improve the oxidation resistance ability of the alloys [27,28]. In addition, it has been proven that with the minor addition of the Y element, the glass-forming ability of the alloys is greatly enhanced [29]. Thus, the JNi-5 filler metal can be fabricated into the amorphous brazing filler metal and this amorphous brazing filler metal can be used to braze GH4169 alloy. With the modification of the filler metal composition, the matched ideal brazing process parameters also need to be further explored. The joint with good mechanical properties was obtained by optimizing the brazing parameters. The effect of brazing temperature on the microstructure and mechanical properties of the joint is discussed. The inherent correspondence between the microstructure and mechanical properties was analyzed. Through the above experimental exploration, near homogeneous joining of GH4169 was realized in this work.

2. Materials and Methods

In this paper, GH4169 alloy was the base metal (BM), and its composition is listed in Table 1. To facilitate obtaining samples for microstructure analysis and shear testing, the GH4169 bar was cut into cubic specimens with dimensions of 4 mm × 4 mm × 4 mm and 10 mm × 10 mm × 4 mm. Among them, brazed samples in 4 mm × 4 mm × 4 mm blocks were used for microstructure analysis, and brazed samples using blocks in 4 mm × 4 mm × 4 mm and 10 mm × 10 mm × 4 mm sizes were used for shear tests. The contact surface was ground using 1500 grit silicon carbide paper, then ultrasonically cleaned in ethanol for 6 min before brazing. JNi-5 amorphous foil was used as the filler metal, and its composition is listed in Table 1. This filler metal was prepared using the rapid solidification technique. Its width is about 4 mm, and its thickness is about 50 μm. The thermal properties of this filler metal were characterized by the differential thermal analysis (DTA) device at a heating rate of 10 °C/min as shown in Figure 1. The melting temperature (Tm) is 987 °C, and the liquidus temperature (Tl) is 1029 °C. The JNi-5 filler metal developed in this study is similar to the BNi-4 brazing alloy in the literature [30], both exhibiting the characteristic of a low liquid temperature.
Specimens and filler metal were assembled as a sandwich structure in Figure 2a. The brazing experiments were carried out under a vacuum of 8 × 10−3 Pa. Figure 3 shows the brazing process: the combined specimens, pressured using a Mo block, were first heated up to 300 °C at 10 °C/min and held for 30 min. Then the assemblies were heated further up to the target brazing temperature (1030 °C, 1060 °C, 1090 °C, and 1120 °C) at a rate of 10 °C/min and held for 10 min. After that, all these bonded specimens were cooled to 300 °C at a rate of 5 °C/min. Finally, specimens were cooled in the furnace to room temperature.
After grinding and polishing, the microstructure and quantitative composition analysis of brazed joints were examined by scanning electron microscopy (SEM) equipped with an energy dispersive spectroscopy (EDS). Phase identification was carried out by the X-ray diffractometer (XRD). Hardness distributions across the brazed region were measured by a digital microhardness tester at a load of 50 g for 10 s. The shear test was conducted by a universal test machine with a cross-head speed of 0.5 mm/min, and this test is shown in Figure 2b. Fracture morphologies of joints were characterized by scanning electron microscopy and confocal microscopy.

3. Results

3.1. Typical Microstructure of GH4169 Joint

Figure 4 shows the typical microstructure and heat-affected zone of the obtained joint brazed at 1030 °C. Based on the distribution features of phases, the microstructure could be divided into four specific zones: base metal, heat-affected zone, isothermal solidification zone, and athermal solidification zone.
Figure 5 shows the element distribution of the joint. The entire joint contains high Ni concentrations because the BM and filler metal are Ni-based alloys. The Ni and Si concentration of the ISZ is higher than the BM, which can be attributed to incomplete diffusion, resulting in a partially uniform microstructure and chemical composition. Moreover, the large atomic radium of the Si atom also impeded the diffusion of this element and led to the aggregation of Si in the ISZ. The ASZ contains high Ni concentration and low Si concentration. The ASZ contains high Ni concentration and low Si concentration, which agrees with the phenomenon found in the previous study [14]. No Nb, Mo and Fe elements were in the interlayer before brazing, and these alloy elements transferred to the interlayer during the substantial dissolution of the BM. This process could be called meltback [31]. Therefore, it can be observed that ISZ and ASZ contain small amounts of Nb, Mo, and Fe elements. The diffusion of B, Co, and Y throughout the entire joint indicates a violent reaction between the filler metal and BM.
In order to identify the phases in the joint, the fracture of the joint at 1030 °C was characterized by XRD, and the XRD pattern is shown in Figure 6. It could be observed that the GH4169 joint contains γ(Ni), CrB, Ni3B, Cr2B3, and Mo3B2. The joint mainly contains six specific phases, and these phases were marked using A, B, C, D, E, and F, as shown in Figure 4. Table 2 displays the chemical compositions (at. %) of the marked points analyzed by EDS. Phase A is distributed in the ASZ, and the EDS results indicate that the chemical composition of phase A is 77.29% Ni, 8.86% Cr, and 1.39% Fe. Combined with relevant research and the Ni-B binary diagram, phase A was deduced as the eutectic, which is composed of Ni-rich boride and γ(Ni) [14]. Phase B contains high Ni and Cr concentrations. Following the XRD result, this phase is γ(Ni). Phase C is located in HAZ and contains 76.48% Nb and 5.55% Ti. Thus, this phase was considered a (Nb, Ti)-rich phase. Phase D and E are distributed in the HAZ due to the B diffusion, respectively, in the shape of needle and chain. These phases contain high Cr, Nb, and Mo concentrations and thus were deduced as borides. It could be found that the Nb and Mo content of phase D was higher than phase E, namely, phase D may be (Cr, Nb, Mo)-rich boride, and phase E may be (Nb, Mo)-rich boride. This phenomenon could be interpreted from the mixing enthalpy between different metal elements with B (Figure 7): B element could aggregate in the BM near the interlayer, and hence this area precipitates (Cr, Nb, Mo)-rich boride. On the contrary, the BM far away from the interlayer, containing a small B concentration, may precipitate (Nb, Mo)-rich boride due to the fact that B tends to react with Nb and Mo. Phase F contains 54.82% Ni, 14.39% Cr, and 19.30% Fe. This phase is considered as (Cr, Fe)-rich substrate. In conclusion, the typical microstructure is GH4169/(Nb, Mo)-rich boride+(Cr, Nb, Mo)-rich boride/γ(Ni)/Ni-rich boride+γ(Ni)/γ(Ni)/(Cr, Nb, Mo)-rich boride+(Nb, Mo)-rich boride/GH4169.

3.2. Effect of Brazing Temperature on Microstructure of GH4169 Joints

Figure 8 shows the effect of brazing temperature on the microstructure of GH4169 joints. The width of the HAZ gradually increased, and the volume fraction of borides in the HAZ first increased and then decreased, with the increase in the temperature. This could be interpreted from the fact that the diffusion could diffuse farther with increased temperatures. In addition, it could be found that chain-like borides were coarsened at 1090 °C and 1120 °C. Relevant research reveals that precipitation coarsening was responsible for the degradation of corrosion resistance, fatigue life, and creep–rupture properties because it depletes the beneficial elements, such as Nb and Cr, in the substrate [32]. Therefore, the microstructure of the joint at an exceptionally high temperature was undesirable in practical application. When the temperature is 1030 °C, there are a quantity of eutectic structures in the ASZ. At 1060 °C, there was a notable decrease in the volume fraction of the brittle phase in the ASZ. According to the main composition of phase G (76.8Ni7.5Cr1.5Si5.5Co1.3Fe2.5Nb1.2Al0.80Ti, at.%), marked in Figure 8, this phase is deduced as the eutectic structure composed of Ni-rich boride and γ(Ni), as its composition is similar to the area A in Table 2. When the temperature further increased to 1090 °C and 1120 °C, sufficient B diffusion led to the elimination of the ASZ. Therefore, the microstructure of these joints becomes homogeneous. This phenomenon could be interpreted from the previous study [33]: the aggregation of B in the residual liquid leads to the formation of brittle phases, and increasing the temperature effectively enhances the B diffusion ability, which indicates that the effect of the temperature on the element diffusion coefficient is higher than the element concentration gradient. Although the Ni-based solution continuously repeals B into the residual liquid in the way of regional segregation during the isothermal process, the high temperature causes B in the residual liquid to diffuse sufficiently again.

3.3. Effects of Brazing Temperature on Mechanical Properties of GH4169 Joints

Microhardness distributions of the joint directly reflect the inherent connection between the microstructure and mechanical properties of the joints. Figure 9 shows the microhardness distributions of joints at different brazing temperatures. When brazed at 1030 °C and 1060 °C, the joint microstructure is composed of the ASZ, ISZ, and HAZ. The existence of brittle phases, such as the eutectic structure and borides, led to the microhardness of the ASZ and HAZ being high. When the temperature was increased to 1090 °C and 1120 °C, the ASZ was eliminated, and the microhardness of the ISZ increased compared with the ISZ of the joint at low temperatures. Binesh et al. [33] found that the high microhardness of the BM was caused by the existence of the γ′ strengthening phase and the solid solution strengthening effect, and sufficient diffusion of solution strengthening elements (Cr and Co) and γ′ strengthening elements (Al and Ti) at high temperatures resulted in the hardness increase in the ISZ. In addition, sufficient alloy element diffusion led to the hardness distributions in the ISZ at high temperatures, showing a small fluctuation, which reflects the more homogeneous microstructure.
Figure 10 illustrates the effect of brazing temperatures on the shear strength of joints. At 1030 °C, the shear strength of the joint is 435.54 ± 13.06 MPa. At 1060 °C, the shear strength arrived at the maximum value (693.78 ± 20.81 MPa), because the volume fraction of Ni-based solid solution increased, which could alleviate the stress concentration caused by brittle phases. When the temperature is 1090 °C, the shear strength slightly decreases to 683.42 ± 20.50 MPa. At 1120 °C, the shear strength is 689.33 ± 18.67 MPa.
Figure 11 shows the fracture path of joints at different brazing temperatures. At 1030 °C, the fracture path is in the ASZ, which means that the ASZ is the weakest area of the joint. It could be found that cracks occupy the brittle phase. This phenomenon is similar to other research: the brittle phase results in the stress concentration in the ASZ and provides a preferentially low resistance path for the initiation and propagation of cracks [34]. Further increasing the temperature to 1060 °C, the joint ruptured through the ASZ and HAZ because the volume fraction decreased in the brittle phase and the volume fraction increased in borides in the HAZ. The morphology of the brazed seam ends at 1060 °C is depicted in Figure 12. It can be observed that a large amount of brittle phase is distributed at the end of the brazed seam, indicating that the brittle phase deteriorates the mechanical properties of the joint. At 1090 °C and 1120 °C, the fracture path is mainly in the HAZ and ISZ. The borides in the HAZ become coarser, as shown in Figure 8. Therefore, the crack extends through the coarse borides in Figure 11e, indicating that the coarse borides in the HAZ reduce the shear strength of the joint.
Figure 13 shows the fracture morphology of the joints at different brazing temperatures. At 1030 °C, the blue area was deduced as the fracture morphology in the ASZ combined with the conclusion of the fracture path above. At 1060 °C, the roughness range was mainly in the low area, and the tendency of the joint dropped quickly from the bottom left and then plateaued. Hence, combined with the analysis above, it could be inferred that a few cracks happened at the end of the brazed seam, and partial cracks went through the brazed seam and spread along the HAZ because of the existence of many borides in the HAZ [35]. At 1090 °C and 1120 °C, the fracture morphology also shows that fracture behaviors happened in the HAZ. Namely, the HAZ of joints at high temperatures is the weak area under the external force, and cracks propagate quickly in this area.
Figure 14 shows the fracture morphology of joints brazed at different temperatures (SEM), and Table 3 demonstrates the EDS results of these fractures. At 1030 °C, the fracture mode was considered as the quasi-cleavage fracture due to the fracture characteristics, such as cleavages and dimples. The EDS results show that the fracture is in the ASZ. At 1060 °C, 1090 °C, and 1120 °C, these joints all fractured in a ductile mode according to a mass of dimples. The EDS results indicate that the fractures of these joints at high temperatures are in the HAZ, which is consistent with the conclusion above.

4. Conclusions

To better connect the GH4169 alloy, a novel Ni-Cr-Si-B filler metal was designed and further fabricated into the amorphous brazing filler metal. The effect of brazing temperatures on the microstructure and mechanical properties of GH4169 joints was investigated. The conclusions are summarized below:
(1)
The typical microstructure of the joint brazed at 1030 °C is composed of four specific zones, respectively, the BM, HAZ, ISZ, and ASZ. The typical microstructure of the joint is GH4169/(Nb, Mo)-rich boride+(Cr, Nb, Mo)-rich boride/γ(Ni)/Ni-rich boride+γ(Ni)/γ(Ni)/(Cr, Nb, Mo)-rich boride+(Nb, Mo)-rich boride/GH4169. Increasing the temperature led to the HAZ widening and the ASZ depleted at 1090 °C and 1120 °C. In addition, borides in the HAZ coarsened at 1090 °C and 1120 °C.
(2)
At 1030 °C, the fracture path is in the ASZ. The fracture mode is the quasi-cleavage fracture. At 1060 °C, 1090 °C, and 1120 °C, the fracture behavior mainly happened in the HAZ. The fracture mode of these joints is the hybrid ductile. At 1060 °C, the shear strength of the obtained joint is the highest value (693.78 MPa) due to the volume fraction increase in the Ni-based solid solution. When brazed with parameters 1060 °C/10 min, thanks to the volume fraction increase in the Ni-based solid solution, the shear strength of the joints reached the peak value of 693.78 MPa.

Author Contributions

Conceptualization, X.Y. and D.H.; writing—original draft, X.Y.; methodology, K.Z. and L.Y.; data curation, K.Z., L.Y. and X.Y.; formal analysis, K.Z.; investigation, K.Z. and D.H.; visualization, L.Y.; writing—review and editing, L.Y. and D.H.; resources, X.Y. and D.H. All authors have read and agreed to the published version of the manuscript.

Funding

This research was funded by the National Natural Science Foundation of China (No. 52071165) and the Key R&D Program of Zhejiang (2024C01154). We would like to thank Zhengzhong Zhang, Shenggang Wang, Feng Lv, Yongbin Li, and Chengrong Cao for their help with this manuscript.

Data Availability Statement

The authors confirm that the data supporting the findings of this study are available within the article.

Conflicts of Interest

The authors declare no conflicts of interest.

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Figure 1. The DTA curve of the JNi-5 filler metal foil.
Figure 1. The DTA curve of the JNi-5 filler metal foil.
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Figure 2. Schematic of (a) the sample assembly and (b) the shear test fixture.
Figure 2. Schematic of (a) the sample assembly and (b) the shear test fixture.
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Figure 3. Schematic of the brazing process.
Figure 3. Schematic of the brazing process.
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Figure 4. Typical microstructure and heat-affected zone of the joint: (a) typical microstructure; (b) heat-affected zone.
Figure 4. Typical microstructure and heat-affected zone of the joint: (a) typical microstructure; (b) heat-affected zone.
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Figure 5. Typical microstructure and element distributions of the joint brazed at 1030 °C: (a) typical microstructure; (b) Si; (c) Ni; (d) Cr; (e) Fe; (f) Nb; (g) Mo; (h) B; (i) Y; (j) Co.
Figure 5. Typical microstructure and element distributions of the joint brazed at 1030 °C: (a) typical microstructure; (b) Si; (c) Ni; (d) Cr; (e) Fe; (f) Nb; (g) Mo; (h) B; (i) Y; (j) Co.
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Figure 6. XRD pattern of the joint brazed at 1030 °C.
Figure 6. XRD pattern of the joint brazed at 1030 °C.
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Figure 7. The mixing enthalpy between different metal elements with B.
Figure 7. The mixing enthalpy between different metal elements with B.
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Figure 8. Microstructure and heat-affected zone of GH4169 joints at different brazing temperatures: (a) 1030 °C; (c) 1060 °C; (e) 1090 °C; (g) 1120 °C; (b,d,f,h) correspond to the enlarged views at the dashed boxes in (a,c,e,g), respectively.
Figure 8. Microstructure and heat-affected zone of GH4169 joints at different brazing temperatures: (a) 1030 °C; (c) 1060 °C; (e) 1090 °C; (g) 1120 °C; (b,d,f,h) correspond to the enlarged views at the dashed boxes in (a,c,e,g), respectively.
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Figure 9. Microhardness distributions of joints at different brazing temperatures.
Figure 9. Microhardness distributions of joints at different brazing temperatures.
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Figure 10. Shear strength of joints at different brazing temperatures.
Figure 10. Shear strength of joints at different brazing temperatures.
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Figure 11. Fracture paths of joints at different brazing temperatures: (a) 1030 °C; (b,c) 1060 °C; (d) 1090 °C; (e) 1120 °C.
Figure 11. Fracture paths of joints at different brazing temperatures: (a) 1030 °C; (b,c) 1060 °C; (d) 1090 °C; (e) 1120 °C.
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Figure 12. Microstructure of the end of the brazed seam at 1060 °C.
Figure 12. Microstructure of the end of the brazed seam at 1060 °C.
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Figure 13. Fracture morphology of joints at different brazing temperatures (confocal microscopy): (a) 1030 °C; (b) 1060 °C; (c) 1090 °C; (d) 1120 °C.
Figure 13. Fracture morphology of joints at different brazing temperatures (confocal microscopy): (a) 1030 °C; (b) 1060 °C; (c) 1090 °C; (d) 1120 °C.
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Figure 14. Fracture morphology of joints at different brazing temperatures (SEM): (a) 1030 °C; (b) 1060 °C; (c) 1090 °C; (d) 1120 °C.
Figure 14. Fracture morphology of joints at different brazing temperatures (SEM): (a) 1030 °C; (b) 1060 °C; (c) 1090 °C; (d) 1120 °C.
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Table 1. Chemical compositions of GH4169 alloy and JNi-5 filler metal (wt. %).
Table 1. Chemical compositions of GH4169 alloy and JNi-5 filler metal (wt. %).
MaterialsNiCrCoFeNbMoSiAlTiCBY
GH4169Bal.17.90-18.005.503.100.060.521.04---
JNi-5Bal.8.05.0---4.0---3.00.1
Table 2. Chemical compositions (at. %) of the marked points in Figure 4 and Figure 8.
Table 2. Chemical compositions (at. %) of the marked points in Figure 4 and Figure 8.
PhaseNiCrSiCoFeNbMoTiAlYBPossible Phase
A77.298.861.825.961.392.310.210.731.180.25-Ni-rich boride+γ(Ni)
B67.1711.907.755.042.643.380.020.711.080.31-γ(Ni)
C8.557.36-0.331.1276.480.275.550.34--(Nb, Ti)-rich phase
D37.2134.19-0.5111.8210.833.810.950.65-0.03(Cr, Nb, Mo)-rich boride
E22.9326.24-1.8313.7419.4111.092.711.75-0.30(Nb, Mo)-rich boride
F54.8214.390.551.4119.304.911.261.461.680.22-(Cr, Fe)-rich substrate
Table 3. EDS results (at. %) of the typical fracture characteristics in Figure 14.
Table 3. EDS results (at. %) of the typical fracture characteristics in Figure 14.
PointNiCrSiCoFeNbMoTiAlYBPossible Zone
179.056.451.285.771.611.660.421.331.340.060.31ASZ
257.0413.561.635.2418.292.001.090.350.450.070.29HAZ
353.8914.754.073.9117.492.411.470.950.760.000.29HAZ
454.6616.671.971.3616.182.061.730.882.540.250.26HAZ
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MDPI and ACS Style

Yang, X.; Zhu, K.; Huang, D.; Yang, L. Performance of the GH4169 Joint Using a Novel Ni-Based Amorphous Brazing Filler Metal. Metals 2024, 14, 1274. https://doi.org/10.3390/met14111274

AMA Style

Yang X, Zhu K, Huang D, Yang L. Performance of the GH4169 Joint Using a Novel Ni-Based Amorphous Brazing Filler Metal. Metals. 2024; 14(11):1274. https://doi.org/10.3390/met14111274

Chicago/Turabian Style

Yang, Xiaohong, Kaitao Zhu, Dan Huang, and Lin Yang. 2024. "Performance of the GH4169 Joint Using a Novel Ni-Based Amorphous Brazing Filler Metal" Metals 14, no. 11: 1274. https://doi.org/10.3390/met14111274

APA Style

Yang, X., Zhu, K., Huang, D., & Yang, L. (2024). Performance of the GH4169 Joint Using a Novel Ni-Based Amorphous Brazing Filler Metal. Metals, 14(11), 1274. https://doi.org/10.3390/met14111274

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