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Scientific Reports volume 14, Article number: 6303 (2024 ) Cite this article Crucibles Graphite
Induction skull melting (ISM) technology could melt metals with avoiding contamination from crucible. A long-standing problem of ISM is that the low charge energy utilization and inhomogeneous fields have obstructed its application in many critical metal materials and manufacturing processes. The present work investigated the problem through the structure optimization strategy and established a numerical electromagnetic-field model to evaluate components’ eddy current loss. Based on the model, the effect of crucible and inductor structure on charge energy utilization, etc. was studied. Furtherly, the charge energy utilization was increased from 27.1 to 45.89% by adjusting the system structure. Moreover, structure modifications are proposed for enhancing electromagnetic intensity and uniformity, charge soft contact and uniform heating. The work constructed a basis for framing new solutions to the problem through ISM device structure optimization.
In order to improve service performance and energy-saving, the application of lightweight materials is urgent in the aerospace and automobile industry 1,2. Furthermore, induction skull melting (ISM) is widely used for processing high melting point and reactive metals such as Ti, Zr, Mo, etc. 3,4 to produce excellent performance castings working in critical fields such as aerospace vehicles 5,6,7. The unique feature of ISM technology is a solid skull layer between melt and crucible, thus, avoiding molten melt contamination 8. Meanwhile, the molten melt is stirred by electromagnetic (EM) force, which caused a better composition homogeneity 9. However, the well-known limitations of ISM are remained up to now, low charge energy utilization and inhomogeneous fields above the charge have a negative impact on the energy utilization and charge heating process. Therefore, elimination or reduction of the limitations by optimizing melting system structure is desired.
Due to high temperature and vacuum conditions, modern metallurgical technology mostly uses numerical simulation methods to optimize the parameters of such furnaces 10,11,12. For the past years, researchers have mostly focused on aspects such as EM distribution 13, heat and mass transfer 14,15,16,17,18, melt free surface phenomenon 19,20, turbulence 21, superheat 22,23,24, and evaporation process 25, etc. with different numerical methods including finite element method (FEM) 26,27, finite volume method (FVM) 14, large eddy simulations (LES) 28 and meshless methods 29,30 and so on. However, the effect of cold crucible and inductor structures on magnetic potential and charge energy utilization was seldom reported. It is infinitely detrimental to the efficiency of EM energy utilization in the induction heating process. It has been shown that reducing crucible mass and adding magnetic shunts could reduce energy loss 31. Also, a thinner crucible leads to a higher charge efficiency 32,33. These studies set down the foundations for crucible and induction coil structural optimization.
The present work established a numerical model to evaluate the effect of crucible and induction coil structure on magnetic intensity and charge energy utilization. Also, methods to improve the charge energy utilization, magnetic strength and uniformity are further proposed to gain the heating process.
The energy utilization calculation with ISM melting was achieved by volume fraction calculations of each component eddy current loss, as shown in Eq. (1). Therefore, comparison of the charge energy utilization in different crucible and coil structures could be done by modelling the EM field.
where Qv is the eddy current loss (W), Je and Ee are the current density (A/m3) and the electric intensity (V/m3) in unit volume.
Vector potential was introduced to calculate the electromagnetic field based on Maxwell equations.
where B is the magnetic induction (T), A is the magnetic vector potential (V s m−1), E is the electric field intensity (V m−1), J is the current density (A m−2), Js is the current density source (A m−2), ω is the frequency (Hz), μ is magnetic permeability (H m−1), σ is electrical conductivity (S m−1).
The EM force was given in the following equation.
where FEM is the force density averaged over time (N m−3), B is the magnetic induction (T), J is the current density (A m−2), B* is the complex conjugate, and c represents the charge.
A cold crucible with variable structures was studied in this study for optimization. Due to the slits of the copper crucible, it cannot be simplified to a 2-D model in numerical calculations. Thanks to the centrosymmetric structure of crucible, only a quarter of the geometry model was selected for calculations. In EM field calculations, the research domain should contain all elements including atmosphere (Argon protector), induction coil, crucible and charge. The initial model for EM calculations is shown in Fig. 1a. And the specific dimensional details of the initial model are shown in Table 1. Specific dimensional information can be found in previous publication 34.
(a) The simplification model and (b) grid division.
Mesh discretization is vital in numerical simulations, which determines the calculation accuracy. In EM field calculations, the skin layer depth must be taken into account, which is calculated as follows.
where λ is the depth of the skin layer (m), ω is the frequency (Hz), μ is magnetic permeability (H m−1), σ is electrical conductivity (S m−1).
In the calculations, the skin layer depth usually contains at least two layers of mesh. In our previous study 22, the mesh division using a minimum size of 0.5 mm was able to pass the independence verification. So, we inherited the previous meshing method and optimized the skin layer meshing according to the calculation results of Eq. (7). Furthermore, the infinite domain condition was set at the open boundaries. The mesh was divided as shown in Fig. 1b.
For atmosphere openings and periodicity conditions in Fig. 1a, the zero magnetic vector and periodicity boundary conditions were introduced, as shown below.
where n is the normal vector, b1 and b2 represent different periodicity boundaries.
For material properties, the crucible and coil were made of copper with electrical conductivity of 5.998 × 107 S/m, and density as 8960 kg/m3. And the parameter was measured as 2.22 × 105 S/m for the charge (Vit1 metal) by the physical properties measurement system, density as 6250 kg/m3.
The experiments were carried out on an ISM furnace equipped with cold crucible, induction coil and cooling device, as shown in Fig. 2a. The induction coil has the capability to deliver a maximum induction power of 180 kW and frequency of 10 kHz, enabling the heating of 2 kg alloys (in terms of titanium). The cooling device ensures complete cooling of the coil and crucible to prevent burn out, as well as facilitating the creation of a skull, resulting in a nearly contamination-free melting of the charge.
(a) ISM furnace with a cold crucible, (b) DX-120F Gauss meter.
The magnetic intensity accuracy measurements were carried out by a Gauss meter (DX-120F), which has a maximum error of 0.16% and suitable for 360 mT AC magnetic field with 10 kHz sampling bandwidth, as shown in Fig. 2b. Also, the Gauss meter has been corrected in zero magnetic environment. We carried out measurements at low induction power in empty crucible for safety. The position was chosen to be located on the central axis of the crucible.
All of the simulations were performed on one node of an Intel Xeon Silver 4208 CPU @ 2.10 GHz with 2 T of RAM installed, containing 64 cores. The numerical model was calculated by using COMSOL Multiphysics, which has powerful post-processing capabilities and is based on the FEM method for calculations. Under varying induction power levels, the magnetic induction intensity exhibited a C-shaped distribution trend at the crucible central axis and simulation results have passed the consistency test, as reported in previous article 34.
The number of crucible sections (slits) directly affects the penetration of magnetic flux. We explored the component parts' energy utilization, including crucible, induction coil and charge at different crucible section number with 40 kW induction power and 5 kHz frequency, as shown in Fig. 3. As the section number increases, the energy utilization of crucible and coil tend to decrease and the energy utilization of charge tends to increase. It can be inferred that as the section number rises, more magnetic potential is applied to the charge. However, the increase of charge energy utilization is no longer significant when the number is too large since the magnetic potential inside the crucible becomes saturated. It is due to the fact that the magnetic potential inside the crucible is saturated, which is essentially the same as the potential that can enter inside the crucible from the inductor magnetic excitation in this condition. The remaining energy acts on the crucible, the coil and other power-consuming devices.
Variation of energy utilization with different crucible section number.
The magnetic intensity analysis of the charge top surface shows that the magnetic fluctuates bitterly in the circumferential direction, and there exist magnetic intensity peaks at the crucible slits, as shown in Fig. 4a. The mean squared deviation was introduced to describe the uniformity of the magnetic intensity in this position. The calculation formula is as follows.
where δ is the mean squared deviation, xi is the sample value, \(\overline{x}\) is the sample average value and n is the sample number.
(a) Fluctuation of the magnetic intensity in the circumferential direction of the charge and (b) the variation of the mean squared deviation with the crucible section number.
The mean squared deviation values of the magnetic intensity in the circumferential direction and the fitting curve are shown in Fig. 4b. As the crucible section number increases from 4 to 12, the mean squared deviation value decreases significantly; while from 16 to 36 section number, the value decreases slowly, suggesting an enhanced magnetic potential in the crucible with increasing the section number and has a positive effect on increasing the charge magnetic uniformity. However, when the section number is too large, the magnetic potential inside the crucible gradually approaches saturation. After that, it is no longer possible to obviously improve the magnetic permeability of the crucible by increasing the number, as shown in Table 2.
When there exist slits in the crucible bottom, the magnetic flux is able to act on the charge through this location. The magnetic intensity above the charge with bottom slits is more evenly distributed in the vertical direction than without, and it results in a higher magnetic intensity at the bottom of the charge. In this case, the charge energy utilization is increased by 1.2%. The comparison of the charge magnetic intensity is shown in Fig. 5 in two cases.
The charge magnetic intensity (a) without crucible bottom slits or (b) with slits.
As can be observed from the contours in the diagram, the magnetic flux is more concentrated at the charge bottom when there exist slits in the crucible bottom. The variation of magnetic intensity on the outside of the charge is shown in Fig. 6. The magnetic intensity is more uniform above the charge when there exist slits. At the same time, the introduction of new skin layer at the charge bottom allows the formation of a current density convergence zone at this position, which has an inductive heating effect. Therefore, a new heat transfer trend appears in this way, and the skull thickness could be further reduced during the melting process.
Variation of the magnetic intensity with generatrix height of the charge.
As shown in Fig. 7a,b, the lifting force in charge bottom is enhanced by introducing slits, which then increases the micro-air gap between charge and crucible and reduces the skull thickness. This was beneficial in improving superheat 22. Moreover, it was shown that a curved crucible bottom could induce EM force along the normal direction of curved surface and so causes further increased force on the charge, as shown in Fig. 7c. However, such a design of curved bottom crucible will increase the crucible mass and increase its eddy current loss 35.
(a) Electromagnetic force above the charge with slits in the crucible bottom or (b) without, (c) electromagnetic force above the charge with crucible bottom rounding treatment.
The slits of each copper sector vertical adjacent surfaces consume most of eddy current losses in each sector, resulting in a high crucible temperature 36,37. However, excessively wide slits tend to get internal melt to leak out or produce over-burning of the filling material between the slits. Furthermore, the disadvantage of the narrow slits is the low charge energy utilization and the high-power supply required for the same conditions. Previous researches have also shown that the crucible mass is also a fatal factor in the electrical efficiency and should be reduced as much as possible when optimizing the crucible structure 38. Therefore, the crucible slit size is increased to reduce the crucible mass. Meanwhile, the wide slit structure also serves to converge the magnetic flux in this region and increases the charge magnetic intensity. So, two configurations of the slit were proposed in this subsection, t1 − θ slit type (t1: crucible wall thickness for the first slit width; θ: slit angle) and t1 − d2 type (d2: second slit width), respectively, with the internal slit remaining narrow (0.4 mm), as shown in Fig. 8a. The initial crucible size as t = 17.5 mm (t: total wall thickness of crucible) and the variation of the charge energy utilization with t1 and θ is shown in Fig. 8b. For the initial size crucible (t1 ≈ 15 mm, t = 17.5 mm, d1 = 0.4 mm (d1: first slit width), θ = 90°), the charge energy utilization is 27.1%. As t1 decreases and θ increases, the energy utilization of the charge increases. The smaller the t1, the more significant the increase in the charge energy utilization. Therefore, the reduction in crucible mass could improve the charge energy utilization. Analysis of t1 − d2 type crucible shows that the trend in charge energy utilization is approximately the same as in the t1 − θ type, as shown in Fig. 8c. In view of the mechanical processing and the arrangement of the cooling channels, the t1 − θ type will tend to create sharp corners on the crucible edge when t1 decreases and θ increases, and the cooling channels have to be double-piped, resulting in a poor cooling effect of the crucible. Therefore, the t1 − d2 type was used for crucible optimization in subsequent studies. As already mentioned, the reduction of the crucible mass could increase the charge energy efficiency. So, the crucible was modified to a thin-wall construction. Fixing several parameters (t1 = 5 mm, t = 10 mm, d1 = 0.4 mm) and exploring the effect of changes in d2 on the energy utilization of the charge to determine the optimum value of d2. When the crucible structure parameters as t1 = 5 mm, t = 10 mm, d1 = d2 = 0.4 mm, the charge energy utilization is 34.04%. The results of d2 parameter scan are shown in Fig. 8d. When d2 tends to 4–6 mm, the energy utilization tends stable. It was also found that a further reduction of the crucible thickness (t1 and t) would reduce the weakening of the magnetic flux and lead to a higher charge energy utilization. However, too thin wall could cause crucible burning, so a thin-walled crucible should correspond to the correct melting process parameters, e.g. cooling water flow, etc. When the crucible structure parameters are adjusted as t1 = 5 mm, t = 10 mm, d1 = 0.4 mm, d2 = 5 mm, the efficiency will increase from 27.1 to 38.3% for the charge in this research.
(a) The schematic diagram of two type crucibles, the charge energy utilization with (b) t1 − θ type and (c) t1 − d2 type crucible, (d) d2 scanning results with t1 − d2 type crucible.
The initial coil cross-section was circular and we compared the effect of circular and rectangular coils on the magnetic intensity and charge energy utilization respectively in this subsection. Furthermore, the two types of coils have same cross-section area. The configurations were schematically set as shown in Fig. 9, which ensures the cross-section area per turn is about 160 mm2.
Coil with (a) circular cross section and (b) rectangular.
The magnetic field distribution between the slits is shown in Fig. 10a,b for both, respectively. With the same induction power and frequency, both coils excite large magnetic intensity in the lower part of the crucible, and the maximum magnetic intensity is 149 mT for the circular coil and 212 mT for the rectangular. In addition, the magnetic leakage in the circular coil is more severe than in the rectangular, presumably related to the edge effect of the circular coil. In order to demonstrate the speculation, a comparison of the vertical and radial magnetic intensity was carried out. The location of the magnetic intensity data extraction is marked by yellow and red lines in Fig. 10a,b. The yellow line is located in the middle of the inner part of the coil and the outer part of the crucible; the red line is located in the middle of the second and third turns of the coil. The magnetic intensity of both is shown in Fig. 10c,d. The sine wave trend of the magnetic intensity exhibited by the circular coil confirms the same inference as before. In the vertical direction, the magnetic intensity of the circular coil fluctuates more sharply and is less uniform than the rectangular; in the radial direction, the magnetic intensity of both remains essentially the same. And the charge energy utilization has no significant change. A more homogeneous magnetic field will excite a more homogeneous electric field in terms of uniformity of heat distribution. In summary, the rectangular coil is better.
The magnetic field distribution between the slits for (a) circular and (b) rectangular coil; (c) vertical and (d) radial magnetic intensity of both coils.
This subsection investigates the effect of coils connected in series or parallel on the magnetic field to study the charge energy utilization, all other parameters being fixed and coil type as rectangular. As in the previous position of yellow and red lines shown in Fig. 10a,b, the magnetic intensity excited by both is shown in Fig. 11a,b. In the vertical direction, the magnetic field is more homogeneous in parallel connection. It can be inferred that there exists path loss with series type. In the radial direction, the parallel excites a larger magnetic intensity on the charge. It may be caused by low electrical loss in the coil. The charge energy utilization increased from 37.35% (series) to 45.89% (parallel).
The magnetic intensity in (a) vertical and (b) radial direction of series and parallel type induction coil.
In addition, with the series type, if the current imbalance or sudden overload occurs in one turn, the other turns could be also affected at the same time. Furthermore, for increasing the coil turns number, the coil length increases, which increases the voltage between the coil terminals, which may induce arcing phenomenon. By connecting the coils in parallel, it is possible to reduce the voltage at both terminals and make the coil height control easier by manoeuvring power input mode. In our previous experiments, we found that the energy utilization and field uniformity on the charge was better when the coil height was the same as the melt meniscus height.
Coils can be classified as sparse or densely wound according to the size of their turn spacing. Keeping the coil total length, the effective cross-sectional area of each turn and other parameters unchanged, the vertical magnetic intensity varies with the turn spacing size as shown in Fig. 12. As the turn spacing increases, the magnetic leakage becomes more serious and the uniformity of the magnetic intensity is significantly reduced. Therefore, the reduction in turn spacing is beneficial for magnetic intensity homogeneity above the charge, which plays a positive role in soft contact and homogeneous heating. However, to prevent the breakdown of adjacent coil, the coil surface needs to be wrapped and coated with insulating paint. So, a certain space should be left for the insulation later between turns. Therefore, the smaller the gap between the coil turns, the better, provided that the insulation is maintained.
The vertical magnetic intensity varies with the spacing between each turn.
The magnetic intensity and charge energy utilization with different cold crucible and coil structures in the ISM melting process were investigated by EM field numerical modelling. The conclusions are summarized as follows:
The crucible section number increase has a positive effect on charge energy utilization and magnetic intensity homogeneity. When the section number exceeds the threshold, further increases in the section number no longer significantly improve the magnetic intensity above the charge.
When there exist slits at the crucible bottom, the magnetic uniformity in the vertical direction of the charge increases, the magnetic flux is concentrated at the charge bottom and the current density converges at this position, playing an inductive heating effect. When the flat bottom crucible is changed to a curved shape, the EM force above the charge is increased.
Thinner wall and wide slits with the crucible bring a more positive impact on the charge energy efficiency. The new crucible structure has an 11.2% increase in energy utilization compared to the initial structure.
Rectangular cross section coil has a weaker edge effect and a more uniform excitation magnetic field than circular.
The parallel type coil has lower electrical loss compared to the series, the excitation magnetic intensity is higher, and the charge energy utilization is increased to 45.89%. In addition, the parallel coils also allow for better coil height control by manoeuvring whether power is input or not.
Reducing the coil turn spacing improves the charge magnetic uniformity and has an optimistic effect on the soft contact and uniform heating of the charge. Under the premise of ensuring safety, the turn spacing should be reduced as much as possible.
The data that support the findings of this study are available from the corresponding author upon reasonable request.
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Financial assistance was provided by the National Natural Science Foundation of China (No. 51827801), the “Head Goose” project of Heilongjiang Province (Nos. AUEA5640208620, AUEA5640200920) and the Fundamental Research Funds for the Central Universities (No. FRFCU5710001320).
National Key Laboratory of Precision Hot Processing of Metals, Harbin Institute of Technology, Harbin, 150001, China
Chaojun Zhang, Lunyong Zhang, Fuyang Cao, Zhishuai Jin, Guanyu Cao, Hongxian Shen, Yongjiang Huang & Jianfei Sun
School of Materials Science and Engineering, Harbin Institute of Technology, Harbin, 150001, China
Chaojun Zhang, Lunyong Zhang, Fuyang Cao, Zhishuai Jin, Guanyu Cao, Hongxian Shen, Yongjiang Huang & Jianfei Sun
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C.Z.: Conceptualization, methodology, software, formal analysis, validation, writing—Original Draft; L.Z.: Supervision, writing—review & editing; F.C.: Supervision, project administration; Z.J.: Investigation, visualization; G.C.: Project administration, formal analysis; H.S.: Supervision, data curation; Y.H.: Supervision, writing—review & editing; J.S.: Supervision, conceptualization.
Correspondence to Lunyong Zhang, Fuyang Cao or Jianfei Sun.
The authors declare no competing interests.
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Zhang, C., Zhang, L., Cao, F. et al. Optimizing energy efficiency in induction skull melting process: investigating the crucial impact of melting system structure. Sci Rep 14, 6303 (2024). https://doi.org/10.1038/s41598-024-56966-7
DOI: https://doi.org/10.1038/s41598-024-56966-7
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