Analysis of Processing Parameters to Avoid Additional Oxygen Contamination During Production of Zr-based Bulk Metallic Glasses by Suction Casting in an Arc-melting Furnace

Abstract

This study first reports details of a successful arc-melting furnace in the production of bulk metallic glasses (BMGs). Also, the study presents the results of a statistical experiment evaluating critical processing parameters that can increase oxygen concentration and its effects on the glass forming ability (GFA) of two Zr-based BMGs. The experiments on Zr₄₈Cu_46.5Al₄Nb_1.5 BMG composite found that using low arc-current (200 A), short melting time (11 s), positive pressure of argon inert gas trapped in the synthesis chamber, and the absence of prior melting of a Ti-getter results in a lower oxygen contamination in the produced alloy. The second experiment using the Vitreloy 105 BMG alloy proved the previous findings.

Keywords:
Bulk metallic glasses, Glass forming ability, Arc-melting; Suction casting, Ti-getter

1. Introduction

Most work related to the synthesis of BMGs focuses on variables aiming to improve the GFA of those alloys, i.e., the base composition¹, the influence of microalloying² and the deleterious effect of contaminations as oxygen on Zr-based BMGs³. Though necessary, these variables are not enough to achieve the amorphous structure on BMGs, and process variables have a great influence on the structure formation as well. The production of BMGs started with techniques for rapid solidification processing⁴, and the alloys have been developed during the years in such a way that the dependency of higher cooling rates has decreased considerably, i.e. 10²-10³ Ks^-1 in Pd- and Pt-based systems⁵. One of the most consolidated methods to manufacture BMGs is the copper mold casting with great attention to suction casting⁶ and tilting casting⁷.

The set-ups used in BMGs production commonly are the following⁸: fast and powerful heat source, evacuation and back filling the chamber with inert gas, use of melting oxygen Ti-getters inside the chamber, and remelting and flipping of the ingot to ensure homogeneity. Although these set-ups successfully produce BMGs, the literature lacks in a consistent investigation of the production variables in the final product.

The objective of this study is to present some details of our arc-melting furnace that have been successfully producing BMGs over the years together with a couple of statistical experiments performed to evaluate four process variables that may act directly on the final oxygen content of the produced BMGs.

2. Materials and Methods

Figure 1a shows a picture and Figure 1b shows a drawing of the several components that integrate the arc-melting furnace. The main components are the fusion chamber, the vacuum system, the arc-melting electrode, the power supply, copper base, mold assembly, and the inert gas inlet system.

Figure 1
Arc-melting furnace (a) picture of the equipment, (b) drawing, and (c) example of one of the produced samples.

The fusion chamber is made of 304L stainless steel. The chamber walls have four viewports, 90 degrees from each other, made of sodium borate glass, where three of them are used to view the samples and one is used as light source. A copper coiled tube soldered to the external surface of the vessel acts as a cooling system. Room temperature water flows through the coil, the arc-melting electrode, the copper hearth and in the mold.

The main component of the vacuum system is an Edwards RV12 dual stage rotary vane vacuum pump that acts through the entire system. Under the copper mold, there is a pre-vacuum chamber that creates the differential pressure necessary for the suction process. Two manual valves separate the vacuum pump from the fusion chamber as well as the copper mold from the pre-vacuum chamber. The pre-vacuum chamber is continuously degassed by the vacuum pump. All connections are standard vacuum connections type NW16 and NW25 with the flanges sealed by nitrile O-rings.

Two concentric tubes and a cylindrical bar compose the arc-melting electrode, as shown in Figure 2a. The external tube is made of 304L stainless steel and the inert gas is injected into the chamber through an annular space between its inside surface and the mild tube. The mild tube and the cylindrical bar are made of electrolytic copper. They are attached to the power supply, and room temperature water flows through the annular space. The electrode tip is made of a thoriated tungsten standard alloy used for the TIG welding process.

Figure 2
Detailed drawing of (a) arc-melting electrode and (b) furnace base, copper base and conical assembly for the mold.

The power to generate the electric arc is provided by a welding rectifier (ESAB 400A). It can be operated from 200 A to 400 A, under direct current, with a nominal apparent power of 14.5 kVA. The negative pole is connected to the arc-melting electrode, and the grounding cable is connected to the fusion chamber. A PTFE sphere connected to the external tube of the arc-melting electrode prevents the system from short circuiting.

The furnace’s hearth is made of electrolytic oxygen free copper, in order to achieve higher heat transfer during the sample’s melting process. It is provided with a conical assembly, where the copper mold is placed as shown in Figure 2b. It has a copper crucible where the ingot is placed to be molten and suctioned inside the mold by opening a manually operated valve connected to the vacuum booster vessel to quickly fill the mold.

The inert gas inlet system is settled to use argon, but other inert gases are suitable with easy, such as helium or a mixture of gases. Argon 5.0 PA quality is used in the system. The line is connected to a LiH based (Supelco OMI-2 INDICATOR TUBE) solid state polishing purifier which removes many contaminants, such as water and oxygen, delivering in the furnace chamber a higher purity argon gas. This is especially oxygen free (less than 10 ppb).

Two Zr-based BMGs alloys were selected to perform this study. The first alloy with composition Zr₄₈Cu_46.5Al₄Nb_1.5 (at.%) is a BMG composite with excellent mechanical properties due to the combination of B2 particles embedded in the amorphous matrix⁹. The glass forming ability (GFA) of this first alloy is decreased by the increasing in oxygen concentration leading to the formation of brittle phases¹⁰. The second alloy is commercially known as Vitreloy 105 with composition Zr_52.5Cu_17.9Ni_14.6Al₁₀Ti₅ (at.%). The Vitreloy 105 has been reported to be very sensitive to oxygen contamination¹¹, when even in a small wppm increase in the oxygen concentration in the alloy can lead to a decrease in the critical amorphous sample size from 10 mm to 4 mm ³. The Zr₄₈Cu_46.5Al₄Nb_1.5 alloy was produced from high purity raw materials in 2 master ingots with approximately 100 g, using 350 A and 22 s melting time as melting parameters, being flipped and remelted at least 5 times to ensure composition homogeneity. The 100 g master ingots were cut by a wired electric discharge machine, which resulted in 8 pieces with approximately 10 g each. Vitreloy 105 master alloy was purchased from Materion in 3/4" rod bar with 400 mm length and nominal oxygen concentration 180 wppm. The bar was sectioned with a diamond disc in pieces with approximately 10 g.

The system was evacuated down to 10^-4 kPa followed by back filling with argon until internal pressure reached 170 kPa, repeating this procedure three times, leaving the system pressurized in the last stage, to minimize possible atmospheric contamination due to leakage from outside. Table 1 shows the final melting step used in each one of the 10 g sectioned ingots following the parameters. The samples were suction cast into a water-cooled copper mold, producing stepped samples that were 2 and 10 mm in diameter. Figure 1c shows one of them.

Table 1
Variables and oxygen responses of the Zr₄₈Cu_46.5Al₄Nb_1.5 and Vitreloy 105 experiments.

Zr48Cu46.5Al4Nb1.5 experiment							Vitreloy 105 experiment
Run #	Block	Variables				Response	Run #	Block	Variable		Response
		Eletric arc current	Gas flow	Melting time	Ti-getter	Oxygen (wppm)			Eletric arc current	Melting time	Oxygen (wppm)
1	1	200 A	Static	11 s	No	281 ± 47	1	1	350 A	22 s	195 ± 24
2	1	350 A	Static	11 s	Yes	458 ± 85	2	1	200 A	11 s	148 ± 22
3	1	200 A	Dynamic	11 s	Yes	299 ± 30	3	1	350 A	11 s	171 ± 11
4	1	350 A	Dynamic	11 s	No	304 ± 58	4	1	200 A	22 s	187 ± 53
5	1	200 A	Static	22 s	Yes	293 ± 58	5	1	200 A	11 s	161 ± 25
6	1	350 A	Static	22 s	No	258 ± 50	6	1	200 A	22 s	190 ± 49
7	1	200 A	Dynamic	22 s	No	370 ± 11	7	1	350 A	11 s	188 ± 42
8	1	350 A	Dynamic	22 s	Yes	307 ± 85	8	1	350 A	22 s	213 ± 38
9	2	200 A	Static	11 s	No	217 ± 70
10	2	350 A	Static	11 s	Yes	333 ± 81
11	2	200 A	Dynamic	11 s	Yes	256 ± 58
12	2	350 A	Dynamic	11 s	No	388 ± 89
13	2	200 A	Static	22 s	Yes	332 ± 125
14	2	350 A	Static	22 s	No	322 ± 84
15	2	200 A	Dynamic	22 s	No	248 ± 10
16	2	350 A	Dynamic	22 s	Yes	434 ± 100

Seven factors that could be source of additional oxygen contamination on the final produced alloy were identified: electric arc current, gas flow, melting time, use of Ti-getter, the system evacuation, chamber pressure, and gas purity. An experiment to account for two levels and eight factors, 2⁸, would require 256 samples with no replications. It was chosen to study the first 4 factors considered the most important ones, keeping fixed all other factors to avoid bias. Other possible extra sources of oxygen contamination can be identified such as cleaning of furnace and alloy elements, preparation and handling of the sample. To avoid bias, these extra sources were kept fixed and even for all samples.

The electric arc current is directly related to the energy transferred from the electric arc to the samples. As a result, the alloys’ temperature increases and so does its capacity for absorbing oxygen from the chamber. The two levels for this factor were defined by the maximum continuous capacity of our power source, 350 A, higher level, and the least necessary current to melt the samples, 200 A, at a lower level. In even lower currents, the electric arc was not stable or had no capacity to melt the whole sample.

As described before, the oxygen contamination is present inside the fusion chamber. Its source can be related to the presence of oxygen in the chamber atmosphere, due to leakage, the impurity of the inert gas, or degassing from the chamber’s walls and copper hearth. The gas flow factor is based on the hypothesis that the continuous renewal of the environment gas will expel the oxygen from the chamber once it is less dense than the argon. The higher level is defined as the constant renewal of gas and the lower level as the static atmosphere.

The melting time is related to the Zr ability to getter oxygen. Once the alloy is melted, the Zr is activated and starts to associate with the oxygen. The longer the time as a melt, the higher the amount of oxygen content, until the solubility limit of the alloy. Melt time can also be used to allow some oxides to dissolve and dissociate, leaving the alloy free of oxygen. The higher level, 22 s, was defined as the maximum time, in a 350 A current, that the alloy could be submitted. Longer times could damage the copper hearth. The lower limit, 11 s, was defined as the minimum time, in a 200 A current, to completely melt the samples. Lower times would result in partial melting.

It is common in the literature to describe the use of Ti-getter to remove the remaining oxygen from the chamber atmosphere. We defined the lower level as the absence of Ti-getter melting prior the fusion of the sample. The higher level was the activation (melting) of 10 g of a pure Ti piece by 10 seconds prior the melting of the alloy.

The first experiment with Zr₄₈Cu_46.5Al₄Nb_1.5 alloy was set to a 2^1-4 experiment with 4 factors and 2 levels (resolution IV¹²), as shown in Table 2. With two replicates, the experiment resulted in a total of 16 runs, as shown in Table 1.

Table 2
Factors, levels and effects of the Zr₄₈Cu_46.5Al₄Nb_1.5 experiment. Vitreloy 105 experiment studied two factors: electric arc current and melting time.

Factor	Effect	-1 (low level)	+1 (high level)
Arc current	Higher or lower melting temperature	200 A	350 A
Gas flow	Static or dynamic furnace’s atmosphere in a 170 kPa absolute pressure	Static argon in the chamber	Dynamic argon expelled from the chamber (30 l/min)
Melting time	Dissolution of solids in molten alloys	11 s	22 s
Ti-getter	Remove the remaining oxygen in the furnace’s atmosphere	No use of a Ti-getter	Ti-getter (10 g) melted prior to the alloy melting by 10 s

The second experiment with Vitreloy 105 was planned and executed after the analysis of results of the first experiment. The justification for this approach is later presented in the results and discussions section. The Vitreloy 105 was a 2² experiment, with 2 factors, 2 levels, and 2 replicates. The factors are shown in Table 2, and the results in Table 1.

Oxygen concentration was measured in a Leco RO-400 by the inert gas fusion principle using a free oxygen Ni basket inside a graphite crucible to release the oxygen from the samples according to ASTM-E1019. Three pieces were measured with a mass around 100 mg each for all sectioned 10 g initial ingots and the same for all final samples produced after the suction casting.

The data collected for both experiments were analyzed using Minitab® software (Version 17). Analysis of variance (ANOVA) was used to determine the significance of the model and factors. The model adequacy was based on the residual analysis where it was checked, whether the errors were normally distributed, the absence of a pattern of the errors and the predicted response, as well as the errors independency. The null hypothesis H₀ is rejected for any p-value lower than a level of significance (α) of 0.05. The power curves were calculated fixing an α = 0.05, the sample sizes for each experiment were plotted against the effect and identified powers of 0.75, 0.80, 0.90 and 0.95.

3. Results and Discussion

The oxygen response for the initial Zr₄₈Cu_46.5Al₄Nb_1.5 ingots was 217 ± 22 wppm, and Table 1 shows the oxygen results for the experiment. The results show that the expanded uncertainty has no distinct pattern. The oxygen analyzer in this range of oxygen concentration has an uncertainty around 10 wppm; the remaining uncertainty is due to sample variation. Table 3 shows the ANOVA results.

Table 3
ANOVA results of Zr₄₈Cu_46.5Al₄Nb_1.5 experiment.

Source	DF	SS	MS	F-Value	P-Value
Model	8	33690	4211	0.9	0.56
Block	1	96.7	96.7	0.02	0.89
Linear	4	23439	5860	1.26	0.37
Electric arc current	1	16129	16129	3.46	0.105
Gas flow	1	729	729	0.16	0.704
Melting time	1	46.7	46.7	0.01	0.923
Ti-getter	1	6534	6534	1.4	0.275
2-way interactions	3	10155	3385	0.73	0.568
Electric arc current * Gas flow	1	10	10	0	0.964
Electric arc current * Melting time	1	7744	7744	1.66	0.238
Electric arc current * Ti-Getter	1	2401	2401	0.51	0.496
Error	7	32636	4662
Total	15	66326

No significant effect was found, and this might indicate that none of the set-ups produced an oxygen response in the samples. The residual analysis showed a random pattern and a normality test with a p-value of 0.163, validating the ANOVA. The standard deviation was about 68 wppm. Figure 3a shows the power curve. A power (1-β) = 0.80 observed differences of 100 or more wppm of oxygen in the samples.

Figure 3
The power curve of the experiments for (a) Zr₄₈Cu_46.5Al₄Nb_1.5 and (b) Vitreloy 105.

The lack of significant factors might be explained by the number of replicates. The power curve in Figure 3a shows that for the same power value, the increase of replicates can improve the ability to detect differences in oxygen content. The dispersion in the oxygen measurements can be explained by the difficulty in producing the oxygen measurements in BMGs based on high melting temperature and refractory metals.

In order to minimize the problems observed in the first experiment, it was decided to remove two factors, the gas flow and the Ti-getter, as they have shown no significant effect. This decision was based on the main effects plot, Figure 4a, for Zr₄₈Cu_46.5Al₄Nb_1.5 experiment, where closed glass flow and no use of Ti-getter lead to smaller oxygen contents. Figure 4b presents the two-way interaction plots to understand which variables are causing an effect in each other for Zr₄₈Cu_46.5Al₄Nb_1.5 experiment. One easy way to interpret the two-way interaction plot is to keep in mind that no interactions are shown as parallel lines, and interactions are shown as crossed lines. Therefore, it is possible to identify that the arc current and melting time has the greatest interaction among all studied variables, supporting the decision made.

Figure 4
Zr₄₈Cu_46.5Al₄Nb_1.5 experiment plots for (a) main effects and (b) two-way interactions.

The second experiment was fixed with a static atmosphere and no use of Ti-getter. Any possible doubt about sample homogeneity was removed from this experiment, since Vitreloy 105 was supplied from Materion. This ensures chemical homogeneity (certificate of chemical analysis provided by Materion). The oxygen response for the second experiment is shown in Table 1 and the ANOVA in Table 4. This experiment showed a significant effect for both factors. This indicates that the set-ups produced an oxygen response. The residual analysis showed a random pattern and a normality test with p-value of 0.409, validating the ANOVA. The standard deviation was about 10 wppm. Figure 3b shows the power curve. With a power (1-β) = 0.80, one observed difference higher than 25 wppm of oxygen. The reduction of the number of factors has improved the capacity to observe different responses in oxygen concentration.

Table 4
ANOVA results of Vitreloy 105 experiment.

Source	DF	SS	MS	F-Value	P-Value
Model	3	2552.4	850.81	8.34	0.034
Linear	2	2508.9	1254.4	12.29	0.02
Electric arc current	1	826.89	826.89	8.1	0.047
Melting time	1	1682	1682	16.48	0.015
2-way interactions	1	43.56	43.56	0.43	0.549
Electric arc current * Melting time	1	43.56	43.56	0.43	0.549
Error	4	408.22	102.06
Total	7	2960.7

The second experiment has shown an improved resolution compared to the first one, and the differences in the oxygen content were about 30 wppm from the lower to the higher level, regardless of the factor, arc current or melting time. It was possible to exclude the hypothesis that the samples started with a saturated oxygen level because the literature shows^13-16, for the same alloys, contaminations with oxygen many times higher than the one found in this study.

Those results indicate that using the lowest arc current, lowest melting time, static inert gas atmosphere and absence of Ti-getter, the oxygen contamination in the alloys will be minimized. The use of Ti-getters during the production of BMGs is a well spread method, but the results from this study clearly showed that whether Ti-getter is used or not, the alloys’ oxygen concentration will not be significantly altered, probably because the entering inert gas in the chamber was already improved by the LiH solid state getter in the gas line.

4. Conclusions

This study presented a suction casting arc-melting furnace to produce BMGs and statistically studied four factors that might increase the oxygen content during alloy synthesis, finding that for the specific melting conditions applied in this study, the best casting parameters to avoid additional oxygen contamination in production of BMGs alloys were the lowest arc current (200 A), the lowest melting time (11 s), use of a static inert gas (argon) atmosphere previously cleaned with a LiH solid state getter and the absence prior melting of a Ti-getter in the chamber.

5. Acknowledgements

The authors would like to thank Boeing Research & Technology Brazil (BR&T-Brazil) for the support of this research. The authors would like to thank FAPESP, CNPq, and CAPES for financial support. We thank the writing center, especially Ryan Lambert at the Colorado School of Mines for language assistance.

6. References

• ¹
  Inoue A. Stabilization of metallic supercooled liquid and bulk amorphous alloys. Acta Mater. 2000;48(1):279-306. http://dx.doi.org/10.1016/S1359-6454(99)00300-6
  » http://dx.doi.org/10.1016/S1359-6454(99)00300-6
• ²
  Deng L, Zhou B, Yang H, Jiang X, Jiang B, Zhang X. Roles of minor rare-earth elements addition in formation and properties of Cu–Zr–Al bulk metallic glasses. J Alloys Compd. 2015;632:429-34. http://dx.doi.org/10.1016/j.jallcom.2015.01.036
  » http://dx.doi.org/10.1016/j.jallcom.2015.01.036
• ³
  Kündig AA, Lepori D, Perry AJ, Rossmann S, Blatter A, Dommann A, et al. Influence of low oxygen contents and alloy refinement on the glass forming ability of Zr_52.5Cu_17.9Ni_14.6Al₁₀Ti₅ Mater Trans. 2002;43:3206-10. http://dx.doi.org/10.2320/matertrans.43.3206
  » http://dx.doi.org/10.2320/matertrans.43.3206
• ⁴
  Suryanarayana C. Encyclopedia of materials: science and technology. New York: Elsevier; 2002. p. 1-10. http://dx.doi.org/10.1016/B0-08-043152-6/01831-3
  » http://dx.doi.org/10.1016/B0-08-043152-6/01831-3
• ⁵
  Inoue A. Bulk amorphous alloys with soft and hard magnetic properties. Mater Sci Eng A. 1997;226-228:357-63. http://dx.doi.org/10.1016/S0921-5093(97)80049-4
  » http://dx.doi.org/10.1016/S0921-5093(97)80049-4
• ⁶
  Dong F, Su Y, Luo L, Wang L, Wang S, Guo J, et al. Deoxidation of bulk metallic glasses by hydrogen arc melting. Mater Lett. 2012;83:1-3. http://dx.doi.org/10.1016/j.matlet.2012.05.101
  » http://dx.doi.org/10.1016/j.matlet.2012.05.101
• ⁷
  Yan M, Zou J, Shen J. Cooling rate effects on the microstructure and phase formation in Zr₅₁Cu_20.7Ni₁₂Al_16.3 bulk metallic glass. Sci Technol Adv Mater. 2006;7(8):806-11. http://dx.doi.org/10.1016/j.stam.2006.11.009
  » http://dx.doi.org/10.1016/j.stam.2006.11.009
• ⁸
  Soinila E, Pihlajamäki T, Bossuyt S, Hänninen H. A combined arc-melting and tilt-casting furnace for the manufacture of high-purity bulk metallic glass materials. Rev Sci Instrum. 2011;82(7):073901. http://dx.doi.org/10.1063/1.3606444
  » http://dx.doi.org/10.1063/1.3606444
• ⁹
  Wu FF, Chan KC, Chen SH, Jiang SS, Wang G. ZrCu-based bulk metallic glass composites with large strain-hardening capability. Mater Sci Eng A. 2015;636:502-6. http://dx.doi.org/10.1016/j.msea.2015.04.027
  » http://dx.doi.org/10.1016/j.msea.2015.04.027
• ¹⁰
  Campos ND No, Pereira FS, Antonio SG, Guo Y, Clarke AJ, Kaufman MJ, et al. Phase formation maps in Zr₄₈Cu_46.5Al₄Nb_1.5 bulk metallic glass composites as a function of cooling rate and oxygen concentration. Mater Charact. 2019;158:109932. http://dx.doi.org/10.1016/j.matchar.2019.109932
  » http://dx.doi.org/10.1016/j.matchar.2019.109932
• ¹¹
  Campos ND No, Soares C, Pereira FS, Bergamaschi V, Antonio SG, Kaufman MJ, et al. Glass forming ability and continuous-cooling-transformation (CCT) diagrams of Vitreloy 105 as function of cooling rate and oxygen concentration. J Non-Cryst Solids. 2020;528:119762. http://dx.doi.org/10.1016/j.jnoncrysol.2019.119762
  » http://dx.doi.org/10.1016/j.jnoncrysol.2019.119762
• ¹²
  Montgomery DC. Design and analysis of experiments. 8th ed. New York: Wiley; 2012. 730 p.
• ¹³
  Altounian Z, Batalla E, Strom-Olsen JO, Walter JL. The influence of oxygen and other impurities on the crystallization of NiZr2 and related metallic glasses. J Appl Phys. 1987;61(1):149-55. http://dx.doi.org/10.1063/1.338847
  » http://dx.doi.org/10.1063/1.338847
• ¹⁴
  Kübler A, Eckert J, Gebert A, Schultz L. Influence of oxygen on the viscosity of Zr–Al–Cu–Ni metallic glasses in the undercooled liquid region. J Appl Phys. 1998;83(6):3438-40. http://dx.doi.org/10.1063/1.367114
  » http://dx.doi.org/10.1063/1.367114
• ¹⁵
  Baricco M, Spriano S, Chang I, Petrzhik MI, Battezzati L. “Big cube” phase formation in Zr-based metallic glasses. Mater Sci Eng A. 2001;304-306:305-10. http://dx.doi.org/10.1016/S0921-5093(00)01438-6
  » http://dx.doi.org/10.1016/S0921-5093(00)01438-6
• ¹⁶
  Chen MW, Inoue A, Sakurai T, Ping DH, Hono K. Impurity oxygen redistribution in a nanocrystallized Zr₆₅Cr₁₅Al₁₀Pd₁₀ metallic glass. Appl Phys Lett. 1999;74(6):812-4. http://dx.doi.org/10.1063/1.123376
  » http://dx.doi.org/10.1063/1.123376

Publication Dates

• Publication in this collection
  05 Feb 2021
• Date of issue
  2021

History

• Received
  24 June 2020
• Reviewed
  18 Aug 2020
• Accepted
  21 Nov 2020