# Analysis of Solid-Liquid Interface Behavior during Continuous Strip-Casting Process Using Sharp-Interface Technique

Authors: Changbum Lee; Wooyoung Yoon; Seungwon Shin; Jaewoo Lee; Hee-eun Song
Journal: International Journal of Photoenergy
 (2013)

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## Abstract

Continuous strip casting (CSC) has been developed to fabricate thin metal plates while simultaneously controlling the microstructure of the product. A numerical analysis to understand the solid-liquid interface behaviors during CSC was carried out and used to identify the solidification morphologies of the plate, which were then used to obtain the optimum process conditions. In this study, we used a modified level contour reconstruction method and the sharp-interface method to modify the interface tracking, and we performed a simulation analysis to identify the differences in the material properties that affect the interface behavior. The effects of the process parameters such as the heat transfer coefficient and extrusion velocity on the behavior of the solid-liquid interface are estimated and also used to improve the CSC process.


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## Body

## 1. Introduction

Identifying the underlying mechanisms that occur during the solidification process is essential for determining the microstructure of a material, which in turn determines the physical properties of the final product. Understanding the solid-liquid interface system is important for understanding the morphology, but the dynamics of an interface are relatively complex, both experimentally and theoretically, even for the simplest substances [1, 2]. Continuous strip casting (CSC) is a horizontal continuous-casting technique designed to yield a thin metal plate or strip while simultaneously controlling the microstructure. CSC is also a promising technique for producing silicon wafers without kerf loss for silicon solar cells [3]. Because the size and orientation of the silicon grains significantly affect the solar cell efficiency [4], CSC could be used to fabricate thin Si strips. A planar solid-liquid interface needs to have a longitudinal grain structure, and therefore, the simulation model for CSC should take into account the interface behaviors. In a previous study, tracking of a solid-liquid interface was performed with numerical simulation of the CSC process [3]. In this paper, we studied the solid-liquid interface behavior as a function of the material properties using the level contour reconstruction method (LCRM). Interface tracking and the analysis of the shape of the solid-liquid interface with a specific heat transfer coefficient were carried out in order to determine the optimum CSC process parameters. The sharp-interface method employed in a few earlier studies [5–7] was also used in this study to implement the exact boundary conditions for a moving solid interface, thus maintaining an accurate phase equilibrium at the solid-liquid interface and enabling us to perform a simulation analysis of the CSC process. Front tracking, the method used here, has many advantages, including its lack of numerical diffusion and the ease and accuracy with which interfacial physics can be described on a subgrid level. It was found that tracking often does not require highly refined grids and that the grid orientation does not affect the numerical solution [8]. Tracking affords a precise description of the location and geometry of the interface, and thus, the surface tension force can be very accurately computed directly on the interface [9].


## 2. Materials and Methods

A schematic of the equipment apparatus, designed for manufacturing a continuous thin metal plate, is shown in Figure1. Two heating zones were installed: one to control the melt temperature and the other to apply a temperature gradient. A cooling system was used to extract heat from the liquid for solidification. The pressure, which determines the production rate of the metal plate, was controlled by a mass flow controller (MFC) and a vent valve. The dummy bar was used as a stopper and the heat extraction route. A numerical simulation was performed for optimizing the continuous casting parameters. The single-field formulation of the continuity and momentum equation is solved for incompressible two-phase flow:
(1)∇·u=0,ρ(∂u∂t+u·∇u)=-∇P+ρg+∇·μ(∇u+∇uT)+F,∂T∂t+u·∇T=α∇2T(α=αLinliquidphaseα=αSinsolidphase),
where u is the velocity,P is the pressure, g is the gravitational acceleration, and F is the local surface tension force at the interface. Material property fields can be described by using the indicator function I(x,t). The density is calculated by
(2)ρ(x,t)=ρ1+(ρ2-ρ1)I(x,t).
The interface is advected in a Lagrangian fashion by integrating
(3)dxfdt·n=m˙fρf=V·n,
where V is the interface velocity vector. In problems involving phase changes, the interface velocity and the fluid velocity at the interface are not necessarily the same. Without a phase change, the interface velocity will be equal to the fluid velocity at the interface, that is, V=uf=u(xf). Only the normal component of the interface motion is determined by the physics and not the tangential motion, and we may assume that the interface and fluid at the interface have the same tangential component of velocity.Figure 1
Dimensions (3×0.3 mm) for the numerical simulation. Initial interface and heat extraction sides are marked (hup, hdown, and hside).The equation of conservation of mass written for the entire flow field is(4)∂ρ∂t+∇·(ρu)=0.The momentum equation is written for the entire flow field and the forces resulting from surface tension and inserted at the interface as body forces, which act only at the interface. In conservative form, this equation is(5)∂(ρu)∂t+∇·(ρuu)=-∇P+ρg+∇·μ(∇u+∇uT)+∫Γ(t)σκnδ(x-xf)ds,
where σ is the surface tension coefficient and κ is twice the mean interface curvature. The thermal energy equation with an interfacial source term to account for the liberation or absorption of latent heat is
(6)∂(ρcT)∂t+∇·(ρucT)=∇·k∇T+∫Γ(t)m˙fLδ(x-xf)ds.Here,T is the temperature and L=L0+(c1-c2)Tsat·L0 is the latent heat measured at the equilibrium saturation temperature Tsat(P), corresponding to the reference ambient system pressure. The Navier-Stokes equation is derived by the phase-change projection method [10] using first-order forward Euler time integration [11]. In this study, the marker-and-cell method [12] is used for staggered grid discretization. The convection term, viscosity term, and pressure field are calculated by the second-order essentially nonoscillatory (ENO) method, the central difference method, and FISHPACK [13], respectively. The detailed procedures for solving the governing equations and introducing the interface-tracking method can be found in [9, 10, 14, 15]. In front tracking, the customary stationary volumetric mesh is supplemented by a moving interface mesh that is used to explicitly track the interface. This interface mesh is composed of nonstationary Lagrangian computational points connected to form a two-dimensional surface. At each time step, information must be passed between the moving Lagrangian interface and the stationary Eulerian grid. Because the Lagrangian interface points do not necessarily coincide with the Eulerian grid points, the passing of information is accomplished using Peskin’s immersed boundary method [15]. With this technique, an infinitely thin interface is approximated by a smooth distribution function that is used to distribute sources at the interface over several grid points near the interface. In a similar manner, this function is used to interpolate field variables from the stationary grid to the interface. In this way, the front is given a finite thickness on the order of the mesh size to provide stability and smoothness. There is also no numerical diffusion because this thickness remains constant. Our LCRM [14] is a simplified front-tracking method that eliminates the logical connectivity between discrete interface elements. The associated algorithmic and bookkeeping burden is eliminated, and at the same time, the accuracy and advantages of explicit Lagrangian surface tracking are retained. The interface elements are periodically discarded and then reconstructed on a level contour of the characteristic indicator function I(x,t). The newly reconstructed interface elements automatically take on the topological characteristics of the indicator function, and thus, the operations of element deletion, addition, and reconnection are accomplished simultaneously and automatically in one step, without the need for element connectivity. Furthermore, once the elements are constructed, the interface normal and element areas are easily defined and surface tension forces are accurately computed directly on the interface for each element independently.


## 3. Results and Discussion

The dimensions of the simulated model are shown in Figure1. The initial surface is assumed to be a semicircular shape, and the heat extraction of both the up side and the down side was assumed to be the same. The range of heat extraction applied was from 50 W/m2K to 1.0×105 W/m2K, and the range of the external velocity (Vex) was from 0.001 m/s to 1 m/s. To analyze the behavior of the solid-liquid interface, we tracked the location of the interface and the temperature change. The importance of the final solid-liquid region has been studied before [3]; therefore, the position of the interface should be analyzed in order to understand the behavior. The location of the solid-liquid interface as a function of time at an external velocity of 0.01 m/s is shown in Figures 2 and 3 for silicon and tin, respectively. The heat transfer coefficient, which denotes the amount of heat transferred from a liquid to a mold and solid, ranged from 50 W/m2K to 1.0×105 W/m2K.Figure 2
Numerical results of the location of the silicon solid-liquid interface with time at a fixed external velocity (0.01 m/s). The heat transfer coefficient ranged from 50 W/m2K to 1.0×105 W/m2K.Figure 3
Numerical results of the location of the tin solid-liquid interface with time at a fixed external velocity (0.01 m/s). The heat transfer coefficient ranged from 50 W/m2K to 2.0×104 W/m2K.As shown in Figure4, the locations of the final solid-liquid interfaces are classified according to the heat transfer coefficients: 1.2×103 to 1×106, 9×102 to 1.2×103, and below 9×102 W/m2K for tin and silicon. In particular, the position of the interface is moved away from the boundary when the heat transfer coefficient is less than 9×102 W/m2K with a 0.01 m/s extrusion velocity. The interface is not positioned in the chamber at small values of the heat transfer coefficient, and the interfaces at heat transfer coefficients of 1.2×103 to 1×106 W/m2K may not be conducive to the extrusion of a thin metal plate from a chamber because solidification occurs before reaching the target region. The location of the interface strongly depends on heat transfer coefficients below 104 W/m2K. From these results, it is evident that the position of the solid-liquid interface can be controlled by the heat transfer coefficient, which is an important factor affecting the formation of a solid-liquid interface. There seems to be a little difference between the heat transfer coefficients of silicon and tin; however, the difference appears big because the heat transfer coefficients are expressed in the y-axis in a log scale.Figure 4
Final location of the solid-liquid interface with each heat transfer coefficient at a fixed external velocity (0.01 m/s).In Figure5, the mapping results of the initial state are shown. The Kelvin temperature scale was used for mapping. The mapping results of each heat extrusion direction and heat transfer coefficient are shown in Table 1. For both the side and up-and-down routes at 1.0×102 W/m2K, the cooling has no effect on the formation of a solid-liquid interface in the final state. The lowest temperature region is higher than the melting point of silicon. Because of latent heat, the silicon needs a large amount of heat extraction in order to solidify. For the same amount of heat extraction, the side route has a tendency to cool faster than the up-and-down direction. The result of the 1.0×104 W/m2K up-and-down route shows that the atypical mapping results may be caused by the external velocity. The up-and-down cooling is not sufficient to cool the entire melt. Therefore, heat remains in the melt, and the temperature gradient resulting from it may cause defects in the final product. Moreover, irregular distribution of temperature also affects the microstructure.Table 1
The temperature mapping of simulation dimension of each heat extrude direction and heat transfer coefficient at final state.Figure 5
Temperature mapping of simulation dimensions at the initial state.


## 4. Conclusions

The numerical simulation model for CSC was modified to analyze the solid-liquid interface behavior of silicon and tin. The final location of the interface was calculated and tracked using the front-tracking and sharp-interface method. We concluded that the heat transfer coefficient is an important factor that affects the formation of a solid-liquid interface. In addition, the heat transfer coefficient is also found to influence the shape of the interface, as determined through an investigation of the temperature mapping results. Therefore, the heat transfer coefficient is considered to be the main parameter in the fabrication of a thin metal plate. A more accurate simulation with 3D modeling is necessary for optimizing the conditions for a microstructure-controlled CSC process.



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