# Hot Embossing of Zr-Based Bulk Metallic Glass Micropart Using Stacked Silicon Dies

Authors: Zhijing Zhu; Chuanyun Yi; Tielin Shi; Yichun Zhang; Yang Gao; Guanglan Liao
Journal: Advances in Materials Science and Engineering
 (2015)

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## Abstract

We demonstrated hot embossing of Zr65Cu17.5Ni10Al7.5 bulk metallic glass micropart using stacked silicon dies. Finite element simulation was carried out, suggesting that it could reduce the stress below 400 MPa in the silicon dies and enhance the durability of the brittle silicon dies when using varying load mode (100 N for 60 s and then 400 N for 60 s) compared with using constant load mode (200 N for 120 s). A micropart with good appearance was fabricated under the varying load, and no silicon die failure was observed, in agreement with the simulation. The amorphous state of the micropart was confirmed by differential scanning calorimeter and X-ray diffraction, and the nanohardness and Young’s modulus were validated close to those of the as-cast BMG rods by nanoindentation tests. The results proved that it was feasible to adopt the varying load mode to fabricate three-dimensional Zr-based bulk metallic glass microparts by hot embossing process.


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## Body

## 1. Introduction

With superior strength, high hardness, large elasticity, excellent wear, and corrosion resistance, BMGs (Bulk Metallic Glasses) are recognized as promising materials for structure, sensor, wear-resistant, and corrosion-resistance coating [1, 2]. When formed into microparts, their macroscopic brittle nature can be mitigated [3, 4], which suggests desirable applications in MEMS (Microelectromechanical Systems).To fabricate BMG microparts, there are mainly two processes: direct casting and thermoplastic forming [5]. The former casts the molten alloy into a microdie followed by fast cooling to inhibit crystallization [6, 7]. This process is usually carried out to form macroscale BMG materials [8, 9], which can be used as feedstock for other processes [10]. The latter reheats the BMG feedstock into a viscous metastable supercooled liquid [11, 12] and forms it into microdies before crystallization occurring [13], which is also called hot embossing [14, 15] or superplastic forming [16, 17]. The hot embossing process is considered to be more controllable compared with direct casting because of relatively long processing time and separation of forming and fast cooling [18] and has been used to fabricate microparts [19, 20] and microdies [20, 21]. For forming microparts by hot embossing process, microdies are necessary. As silicon owns high strength and hardness and can be structured into micro geometry with high precision and low surface roughness by lithography and etching process, it has been widely used for microdies in hot embossing process to form BMG microparts [19, 22]. However, due to brittleness and strength reduction caused by the etching process, silicon dies failure can be observed [23]. To enhance the durability of the silicon dies, the load in the hot embossing process needs to be optimized. In addition, most of microparts fabricated by the hot embossing process using silicon dies are quasi three-dimensional structures, which cannot satisfy diverse requirements in MEMS [24].In this work, stacked silicon dies for fabricating three-dimensional microparts were prepared by lithography and ICP (Inductively Coupled Plasma) etching process. Simulations and experiments were carried out to optimize the hot embossing process. A three-dimensional BMG microgear with good appearance was hot embossed successfully, its glassy state was detected by DSC (Differential Scanning Calorimeter) and XRD (X-Ray Diffraction), and the mechanical properties were validated by nanoindentation tests.


## 2. Experimental

Figure1(a) sketched silicon dies preparing process. The silicon wafer was coated with photoresist (AZ9260), exposed for 100 s (MA6, Karl Suss), and followed by developing to transfer patterns onto the photoresist. The exposed region of the silicon wafer was etched to a depth of 300 μm by ICP process (Oxford PlasmaLab System 100). After that, the silicon wafer was thinned by mechanical polishing to make the cavity through the die (Ecomet 300/Automet 300, Buehler). The silicon dies were stacked and aligned by pins to assemble dual-layer dies, as shown in Figure 1(b).Figure 1
Sketches of silicon dies preparation (a), silicon dies stacking (b), and hot embossing process (c).A Zr65Cu17.5Ni10Al7.5 BMG rod with 3 mm in diameter and 80 mm in length was prepared by water-cooled copper mold suction casting method (WK-II vacuum arc melting furnace), where T
g (the glass transition temperature) and T
x (the crystallization onset temperature) were 648.1 K and 734.2 K, respectively. The relationship between the crystallization incubation time of the BMG and the isothermal holding temperature was confirmed by DSC (Diamond DSC, PerkinElmer Instruments) at a heating rate of 150 K·min−1, and the viscosity of the BMG supercooled liquid versus the temperature was measured by parallel plate rheometry with TMA (Thermomechanical Analyzer, TMA Q400EM, TA Instruments-Waters LIC) under a heating rate of 10 K·min−1 and a load of 0.9 N [25].The hot embossing experiments were conducted with home-made super plasticity microforming equipment, in which the temperature after calibration was controlled in ±3 K by a Shimaden SR253 program controller. Two stages had been designed in the equipment for the hot embossing process, the preload and load stages. The preload stage was carried out to stabilize the hot embossing system and the load stage was to form microparts. Figure1(c) showed the sketch of hot embossing process. A BMG feedstock of 3 mm in diameter and 1 mm in height was prepared. A silicon wafer with the thickness of 1 mm was placed beneath the stacked silicon die for padding. The top die moved down under a velocity of 8 μm·s−1 before the load was reaching the preset value in the hot embossing process. After that, the redundant flash was removed by mechanical polishing, and the silicon die was etched away in KOH solution (40% wt) under the temperature of 353 K. The appearance of the obtained micropart was observed by SEM (Scanning Electron Microscopy, FEI Quanta 200), its glassy state was detected with DSC and XRD (X’Pert PRO, PANalytical B.V.), and the mechanical properties were evaluated by nanoindentation tests under a load of 8 mN for 5 s with the loading and unloading rate of 0.5 mN·s−1 (TI750Ubi system, Hysitron).


## 3. Finite Element Simulation

As mentioned in Figure1, silicon dies failure will occur under improper loading conditions; thus, the hot embossing load should be optimized and the stress in silicon dies should be maintained in a low level as long as the dies cavity is fully filled by BMG within the limited processing time. DEFORM 3D, finite element simulation software, was employed to investigate the behavior of the BMG in the microdie cavity and the stress in the silicon die. A Newtonian model of σ
=
μ
·
ε
˙ was adopted, where σ is the flow stress, ε
˙ is the strain rate, and μ is the Newtonian viscosity. As shown in Figure 2, a quarter model including a top die, a feedstock, and a bottom die was established to simplify the calculation. The feedstock with 3 mm in diameter and 1 mm in height was set as plastic body. The bottom die was a combination of two stacked silicon dies: the first layer was a 20 teeth microgear with 100 μm in modulus and 300 μm in depth, and the second layer was a shaft with 1 mm in diameter and 300 μm in depth. The pressure and flowing of the BMG supercooled liquid under constant load mode (200 N holding for 120 s) and varying load mode (100 N holding for 60 s and then 400 N holding for 60 s) were investigated, where the top and bottom dies were set as rigid bodies. Then, the bottom die was changed to elastic body, and the stress in the bottom silicon dies was studied, in which the Young modulus and Poisson’s ratio were set to 186 GPa and 0.27, respectively.Figure 2
Simulation model for hot embossing of BMG microgear.


## 4. Results and Discussion

### 4.1. Processing Temperature

The BMG feedstock becomes a high viscosity and metastable liquid in the supercooled liquid region and will lose its glassy structure when the processing time exceeds the crystallization incubation time. Table1 lists the incubation time of Zr65Cu17.5Ni10Al7.5 BMG obtained by DSC isothermal holding experiments. The incubation time is 46.3 min at 683 K and reduces rapidly when the processing temperature increases (1 min @ 733 K). For high processing temperature (≥723 K), the incubation time will be too short to carry out the hot embossing. Thus, we need to choose suitable processing temperature.Table 1
Incubation time of Zr65Cu17.5Ni10Al7.5 under different processing temperature.
Processing temperature (K)
683
693
703
713
723
733
Incubation time (min)
46.3
29.6
7.92
3.57
1.67
1.00The viscosity of Zr65Cu17.5Ni10Al7.5, as shown in Figure 3, is also affected by the temperature and strain rate. Under low strain rate, the BMG supercooled liquid exhibits Newtonian flow and owns best thermoplastic forming ability, where the viscosity is mainly determined by the temperature [26]. When the temperature increases, the viscosity gradually decreases to the minimum value (6.78 × 106 Pa·s at about 707 K) in the low temperature zone and then increases in the high temperature zone due to occurrence of crystallization.Figure 3
Newtonian viscosity of Zr65Cu17.5Ni10Al7.5 BMG versus temperature.Therefore, the processing temperature is the most important parameter for the BMG hot embossing process, as it determines the maximum processing time and the Newtonian viscosity of the BMG supercooled liquid [27]. To enhance the controllability and forming ability, the processing temperature must ensure low viscosity for the supercooled liquid and enough time for the hot embossing process. In this study, the temperature of 703 K is chosen, in which the maximum processing time reaches 7.92 min and the viscosity is 7.36 × 106 Pa·s.


### 4.2. Simulation Results

Figure4 shows the simulation results. The filling process under the constant load mode (200 N for 120 s) can be split into three stages. Filling begins in the first stage, in which the maximum pressure and velocity of the supercooled liquid are observed. The macro scale structure of the die cavity is filled in the second stage, where both the pressure and the velocity decrease slowly as the filling depth increases. In the third stage, the supercooled liquid flows into the micro scale structures of the die cavity with the pressure and velocity reducing to the minimum values.Figure 4
Simulation results: the distribution of pressure (a) and velocity (b) in the BMG supercooled liquid for the two loading modes.
(a)
(b)Under the varying load mode, the maximum pressure of the supercooled liquid contacting the silicon die is lower (about 500 MPa) than that under the constant load mode (about 780 MPa), as shown in Figure4(a). This illustrates that adopting lower load (100 N for 60 s) in the preload stage will reduce the maximum pressure. When the embossing load is added (400 N for 60 s) in the load stage, the pressure is reincreased to 500 MPa and the flowing of the supercooled liquid is accelerated significantly (see Figure 4(b)). The final microparts under the two load modes are shown in Figure 4(b). It can be observed from the magnified velocity distribution that the micropart fabricated with the varying load mode has more clear edges than that fabricated with the constant load mode. The simulation results demonstrate that under the varying load the maximum pressure during the hot embossing process maintains a lower level, and the micropart will be formed more completely within the same processing time due to the flow acceleration.Figure5 shows the stress distribution in the silicon dies. Under the constant load, the stress in the silicon dies concentrates in the gear teeth region (above 500 MPa) and reaches the highest level (exceeding 1000 MPa) in the edges of the gear teeth at the first stage. Then, the stress in the gear teeth reduces to about 450 MPa in the second stage and maintains below 150 MPa during the third stage. Under the varying load, the stress in the gear teeth is below 300 MPa at first and increases to the maximum value (about 400 MPa) after the forming load is added to 400 N at 62.2 s. As reported in [28], there was a risk of silicon dies failure when the stress exceeded 400 MPa. The simulation results suggest that the risk of the silicon dies broken may occur for the constant load mode and can be minished by using the varying load.Figure 5
The stress distribution in silicon mold for the two load modes.


### 4.3. Experimental Result and Micropart Inspection

Figure6(a) shows the curves of the embossing force versus time for the two load modes. It can be seen that there is a pause at about 110 N before the embossing force was increasing to 200 N under the constant load mode. This implies that the force about 110 N is enough for the supercooled liquid flowing into the dies cavity in the first stage. The silicon dies keep unbroken under the varying load in the experiments. The insets of Figure 6(a) display the microscale structures obtained by these two load modes. We can find that the micropart fabricated under the varying load has more distinct edges than that under the constant load. Figure 6(b) shows the SEM image of the whole 3D BMG micropart embossed under the varying load, demonstrating a good appearance. These are all in agreement with the simulation results.Figure 6
The experimental results. (a) True force curves for the two load modes with the details of the microgear teeth in the insets, (b) SEM image of the microgear formed under the varying load.
(a)
(b)Figure7(a) shows the DSC curves of the hot embossed micropart and the as-cast BMG feedstock under the heating rate of 20 K/min. The distinct glass transition and crystallization heat of the micropart are in accordance with the amorphous alloy, where T
g and T
x are 645.7 K and 730.2 K, and the crystallization heat is 30.39 J·g−1, lower than those of the as-cast BMG. The XRD curves of the as-cast BMG and micropart are shown in Figure 7(b). The two curves show similar patterns with a broad diffuse peak typical for the presence of noncrystalline phases rather than sharp diffraction peaks, confirming that no large size crystals occur in the micropart during the hot embossing process.Figure 7
The results of DSC (a) and XRD (b) for the as-cast BMG and microgear.
(a)
(b)The nanohardness and Young’s modulus for the micropart and as-cast BMG feedstock are displayed in Figures8(a) and 8(b), where the averaged nanohardness and Young’s modulus of the microgear are 5.52 GPa and 89.28 GPa, very close to those of the as-cast BMG rod (5.48 GPa and 88.07 GPa).Figure 8
Nanohardness (a) and Young’s modulus (b) of the as-cast BMG feedstock and microgear.
(a)
(b)


## 4.1. Processing Temperature

The BMG feedstock becomes a high viscosity and metastable liquid in the supercooled liquid region and will lose its glassy structure when the processing time exceeds the crystallization incubation time. Table1 lists the incubation time of Zr65Cu17.5Ni10Al7.5 BMG obtained by DSC isothermal holding experiments. The incubation time is 46.3 min at 683 K and reduces rapidly when the processing temperature increases (1 min @ 733 K). For high processing temperature (≥723 K), the incubation time will be too short to carry out the hot embossing. Thus, we need to choose suitable processing temperature.Table 1
Incubation time of Zr65Cu17.5Ni10Al7.5 under different processing temperature.
Processing temperature (K)
683
693
703
713
723
733
Incubation time (min)
46.3
29.6
7.92
3.57
1.67
1.00The viscosity of Zr65Cu17.5Ni10Al7.5, as shown in Figure 3, is also affected by the temperature and strain rate. Under low strain rate, the BMG supercooled liquid exhibits Newtonian flow and owns best thermoplastic forming ability, where the viscosity is mainly determined by the temperature [26]. When the temperature increases, the viscosity gradually decreases to the minimum value (6.78 × 106 Pa·s at about 707 K) in the low temperature zone and then increases in the high temperature zone due to occurrence of crystallization.Figure 3
Newtonian viscosity of Zr65Cu17.5Ni10Al7.5 BMG versus temperature.Therefore, the processing temperature is the most important parameter for the BMG hot embossing process, as it determines the maximum processing time and the Newtonian viscosity of the BMG supercooled liquid [27]. To enhance the controllability and forming ability, the processing temperature must ensure low viscosity for the supercooled liquid and enough time for the hot embossing process. In this study, the temperature of 703 K is chosen, in which the maximum processing time reaches 7.92 min and the viscosity is 7.36 × 106 Pa·s.


## 4.2. Simulation Results

Figure4 shows the simulation results. The filling process under the constant load mode (200 N for 120 s) can be split into three stages. Filling begins in the first stage, in which the maximum pressure and velocity of the supercooled liquid are observed. The macro scale structure of the die cavity is filled in the second stage, where both the pressure and the velocity decrease slowly as the filling depth increases. In the third stage, the supercooled liquid flows into the micro scale structures of the die cavity with the pressure and velocity reducing to the minimum values.Figure 4
Simulation results: the distribution of pressure (a) and velocity (b) in the BMG supercooled liquid for the two loading modes.
(a)
(b)Under the varying load mode, the maximum pressure of the supercooled liquid contacting the silicon die is lower (about 500 MPa) than that under the constant load mode (about 780 MPa), as shown in Figure4(a). This illustrates that adopting lower load (100 N for 60 s) in the preload stage will reduce the maximum pressure. When the embossing load is added (400 N for 60 s) in the load stage, the pressure is reincreased to 500 MPa and the flowing of the supercooled liquid is accelerated significantly (see Figure 4(b)). The final microparts under the two load modes are shown in Figure 4(b). It can be observed from the magnified velocity distribution that the micropart fabricated with the varying load mode has more clear edges than that fabricated with the constant load mode. The simulation results demonstrate that under the varying load the maximum pressure during the hot embossing process maintains a lower level, and the micropart will be formed more completely within the same processing time due to the flow acceleration.Figure5 shows the stress distribution in the silicon dies. Under the constant load, the stress in the silicon dies concentrates in the gear teeth region (above 500 MPa) and reaches the highest level (exceeding 1000 MPa) in the edges of the gear teeth at the first stage. Then, the stress in the gear teeth reduces to about 450 MPa in the second stage and maintains below 150 MPa during the third stage. Under the varying load, the stress in the gear teeth is below 300 MPa at first and increases to the maximum value (about 400 MPa) after the forming load is added to 400 N at 62.2 s. As reported in [28], there was a risk of silicon dies failure when the stress exceeded 400 MPa. The simulation results suggest that the risk of the silicon dies broken may occur for the constant load mode and can be minished by using the varying load.Figure 5
The stress distribution in silicon mold for the two load modes.


## 4.3. Experimental Result and Micropart Inspection

Figure6(a) shows the curves of the embossing force versus time for the two load modes. It can be seen that there is a pause at about 110 N before the embossing force was increasing to 200 N under the constant load mode. This implies that the force about 110 N is enough for the supercooled liquid flowing into the dies cavity in the first stage. The silicon dies keep unbroken under the varying load in the experiments. The insets of Figure 6(a) display the microscale structures obtained by these two load modes. We can find that the micropart fabricated under the varying load has more distinct edges than that under the constant load. Figure 6(b) shows the SEM image of the whole 3D BMG micropart embossed under the varying load, demonstrating a good appearance. These are all in agreement with the simulation results.Figure 6
The experimental results. (a) True force curves for the two load modes with the details of the microgear teeth in the insets, (b) SEM image of the microgear formed under the varying load.
(a)
(b)Figure7(a) shows the DSC curves of the hot embossed micropart and the as-cast BMG feedstock under the heating rate of 20 K/min. The distinct glass transition and crystallization heat of the micropart are in accordance with the amorphous alloy, where T
g and T
x are 645.7 K and 730.2 K, and the crystallization heat is 30.39 J·g−1, lower than those of the as-cast BMG. The XRD curves of the as-cast BMG and micropart are shown in Figure 7(b). The two curves show similar patterns with a broad diffuse peak typical for the presence of noncrystalline phases rather than sharp diffraction peaks, confirming that no large size crystals occur in the micropart during the hot embossing process.Figure 7
The results of DSC (a) and XRD (b) for the as-cast BMG and microgear.
(a)
(b)The nanohardness and Young’s modulus for the micropart and as-cast BMG feedstock are displayed in Figures8(a) and 8(b), where the averaged nanohardness and Young’s modulus of the microgear are 5.52 GPa and 89.28 GPa, very close to those of the as-cast BMG rod (5.48 GPa and 88.07 GPa).Figure 8
Nanohardness (a) and Young’s modulus (b) of the as-cast BMG feedstock and microgear.
(a)
(b)


## 5. Conclusions

The fabrication of Zr65Cu17.5Ni10Al7.5 BMG three-dimensional microgear by hot embossing process with the stacked silicon dies is investigated. The processing temperature of 703 K is chosen, in which the BMG exhibits enough processing time (7.92 min) and good fluidity (7.36 × 106 Pa·s in viscosity). The finite element simulation results reveal that under the varying load mode (100 N for 60 s and then 400 N for 60 s) the maximum pressure of the BMG supercooled liquid will maintain a lower level and the edges of the micropart can be formed more clear than that under the constant load mode (200 N for 120 s). The experimental results agree well with the simulation. The silicon dies failure is not observed under the varying load, and the formed microgear has a good appearance. The glassy state is preserved after the hot embossing process, while the structure relaxation happens in the BMG micropart. The mechanical properties of the microgear (with the nanohardness 5.52 GPa and Young’s modulus 89.28 GPa) are very close to those of the as-cast BMG feedstock (with the nanohardness 5.48 GPa and Young’s modulus 88.07 GPa). These prove that the durability of the stacked silicon dies can be enhanced and the three-dimensional BMG microparts with good appearance and mechanical properties can be fabricated successfully by using the varying load mode in the hot embossing process.



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*Source: 179714-2015-07-09.xml*