Specification of the variable parameters in (27)
Maglev using bulk High-Tc superconductor can realize stable levitation without any active control (Brandt, 1989), and this facsinating property can reduce remarkably the complexity of the levitation system and therefore exhibits promising application in several fields such as maglev bearing (Hull, 2000; Ma, et al., 2003) and maglev transit (Wang, et al., 2002 ; Wang, J. & Wang, S., 2005; Schultz, et al., 2005; Sotelo, et al., 2010). To understand the electromagnetic interaction between the bulk high-Tc superconductor and its applied fields generated by various permanent magnetic devices and to provide a numerical tool to conduct the design for practical application, many methods have been proposed to numerically estimate the characteristics of the magnetic force of the bulk high-Tc superconductor.
The earliest method (Davis, et al., 1988) after the discovery of the high-Tc superconductor was basically established on the traditional mirror-image-model which uses Bean’s critical model (Bean, 1964). However, this model and the later frozen-image model (Kordyuk, 1998) can not reflect the important hysteresis property of the levitation force (Hull & Cansiz, 1999). Though this demerit can be overcome to some extent by introducing additional image dipoles (Yang & Zheng, 2007), this kind of model is essentially a phenomenological one and its applicable scope is also confined to miniature scale systems due to the essential dipole approximation of the levitated body in deducing the model.
Based on the principle of minimum energy, the current distribution in the high-Tc superconductor can be acquired by an iterative process, and then the magnetic force of the high-Tc superconductor can be calculated by Lorentz equation (Sanchez & Navau, 2001; Navau & Sanchez, 2001; Sanchez, et al., 2006). However, up to date, this method is used only to investigate the axisymmetric system with cylindrical high-Tc superconductor and permanent magnet (Navau & Sanchez, 2001) or 2-D translational symmetry system with rectangular high-Tc superconductor and permanent magnetic array (Sanchez, et al., 2006).
According to the state variables used in the governing equations, the methods describing the electromagnetic property of the high-Tc superconductor based on Maxwell’s equations can be classified into three types, i.e., A-
In this chapter, we report a 3-D finite-element model using current potential T as state variable. In this model, the anisotropic behavior of the high-Tc superconductor is contained in the 3-D governing equations by considering a tensor resistivity, and the finite-element technique is empolyed to numerically solve the mathmatical formulations on a VC++ software platform. The numerical results of both levitation force and lateral force were validated by the measured data. Lastly, one example using this 3-D finite-element model to optimize the magnetic rail is introduced to present its viable use for practical design of maglev system using bulk high-Tc superconductor.
2. Mathematical formulations
2.1. Formulations to model the anisotropy in high-Tc superconductor
The special microstructure, which consists of the alternating stack of superconductive CuO2 layers and almost insulating block layers, results in a remarkable anisotropic behavior in the present high-Tc superconductor (Dinger, et al., 1987). Due to this anisotropic behavior arising from the intrinsic pinning and other defects in the high-Tc superconductor, the flux-line curvature will always occur when the high-Tc superconductor is placed in a magnetic field.
Consequently, the critical current density
Many methods have been proposed to formulate the dependence of the critical current density
When the out-of-plane anisotropic ratio
Here, we will introduce an elliptical model, which has been used to investigate the electromagnetic problem involving the anisotropic ferromagnetic material (Napoli & Paggi, 1983), to describe the angular-dependence property of the critical current density
The resistivity of the high-Tc superconductor is also anisotropic (Wu, et al., 1991) and can be represented by a tensor while modelling the high-Tc superconductor. The tensor of the resistivity of the high-Tc superconductor can be reduced to a following diagonal matrix when only the out-of-plane anisotropy is considered,
2.2. 3-D governing equations
As a conducting material, Maxwell’s equations are also valid to describe the electromagnetic phenomena in the high-Tc superconductor. Thus, we have,
According to (4), the current density J is a divergence free vector with a quasi-static approximation in the low-frequency problem, i.e., and thus, a current vector potential T can be introduced and defined as,
The Coulomb gauge is applied to vector T to guarantee the uniqueness of the solution, i.e., Applying Helmholtz’s theorem to vector T yields the following equation:
According to the physical fact that the normal component of J must be zero on the surface of the high-Tc superconductor, i.e.,
Therefore, only the normal component
The induced field B
When an equivalent conductivity
When we replace by a tensor resistivity, (14) and consider that,
The following equality for the first term in the left side of (14) is satisfied,
According to the Coulomb gauge, we havei.e.,
The following identities can be derived from (17),
2.3. Nonlinear E-J relations
Typically, there are three different models to address the highly nonlinear relationship between E and J of the high-Tc superconductor, i.e., Bean’s critical current model (Bean, 1964), power law model (Rhyner, 1993) and flux flow and creep model (Yamafuji & Mawatari, 1992). For Bean’s critical current model, it fails to investigate problems such as force relaxation (Luo, et al., 1999) and drift under vibration (Gou, et al., 2007) due to the assumption that the current flowing in the superconductor is constant with time and the lack of material related parameters in its model. In addition, Bean’s critical current model can be considered as an infinite case of the power law model (Rhyner, 1993). This model is thereby not employed in the following calculation.
When an index
According to Anderson theory (Anderson, 1962), the responding behavior between E and J due to flux flow and creep model phenomena in the superconductor can be described as:
3. Numerical solution using finite-element technique
The previous work in handling linear eddy current problem has proven that Boundary Element Method is an effective method to numerically solve the governing equations including both differential and integral terms (Miya & Hashizume, 1988). Unfortunately, for the case studied here, the high-Tc superconductor is a highly nonlinear media, and this special property leads to difficulty when Boundary Element Method is employed to handle the 3-D governing equations. Consequently, the finite element method is a frequent choice to discretize the governing equation of the high-Tc superconductor in space (Pecher, et al., 2003; Uesaka, et al., 1993; Yoshida, et al., 1994; Luo, et al., 1999; Alonso, et al., 2004; Gou, et al.,2007a; Gou, et al.,2007b; Lu, et al., 2008). In particular, one format of the finite difference method, named Crank-Nicolson-
3.1. Finite-element matrices
The governing equations (22) to (24) incorporated with the boundary condition are numerically solved by finite-element technique via Galerkin’s method. The tetrahedral element is chosen to mesh the domain of the high-Tc superconductor. The final algebraic equations corresponding to (22) to (24) can be compactly expressed by the following matrix equation,
The finite-element matrices (27) for three components are integrated into one matrix in the numerical program, i.e.,
After applying Crank-Nicolson-
The disadvantage of the
In (30), the dense matrix [Q1] is related to the difference of unknown variables between the last and the previous two time steps. The value of the unknown at the adjacent time step will approach to each other as the continuous decrease of the time step size
3.2. Nonlinear equation solution approach
The common Newton-Raphson method is employed to solve the nonlinear equations obtained from (30). Basically, the nonlinearity of the equations is eliminated by introducing a linear residual, and the corresponding linear equations can be integrated after calculating the Jacobi matrix for each element. To improve the stability of the calculation, a relaxation coefficient is also introduced as suggested in (Grilli, et al., 2005). The relaxation coefficient is assigned with an initial value before calculation. During the calculation, it will be reduced to a smaller one once the convergence can not be achieved within a threshold of the total iterative steps, and in this case the current time step is recalculated with the new value.
Because of the significant increase of the order of the coefficient matrix when the problem is extended from 2-D to 3-D and also the element of the matrix with the anisotropy consideration involved (an additional second derivative in term of
3.3. Numerical procedure
The above-discussed numerical method is implemented by a self-written numerical program based on a VC++ platform with the following typical steps:
Step 1: Initial
Step 2: Calculating [K(
Step 3: The
At the end,
Step 4: Repeating steps 2 and 3 until the residual becomes less than a prescribed tolerance
Step 5: The current density J is obtained by (6), and then the magnetic force is calculated by Lorentz equation,
3.4. Numerical precision
Based on a levitation system composed of a bulk high-Tc superconductor（single-domain with a cubical shape）and magnetic rail（assembled by the permanent magnets with opposite magnetization direction as shown in the inset of Fig. 2）, the dependence of the computational precision of the levitation force on both mesh density and time step is discussed in this section. In the calculation, the bulk high-Tc superconductor was downward in a speed of 1 mm/s from the filed cooling position to the nearest gap, and then upward to its original position. On the basis of the geometrical and material parameters listed in Table 2 and power law model, the levitation force of the bulk high-Tc superconductor was calculated in this vertical down-and-up movement with different mesh densities and time steps.
|wSC (mm)||lSC (mm)||tSC (mm)||Jab c(A/m2)||Ec (V/m)||U0 (eV)||α|
Fig. 2 shows the dependence of the levitation force versus gap curve and the maximum levitation force
reduced, e.g., the rate of the increment is about 57.1% when the total finite element node is raised from 27 to 64, but it is only 2.1% when the node is raised from 343 to 512. This indicates that the computed result is consistent with the finite-element thoery, i.e., the computed value will approach to the real value with the continuous increment of mesh density. Fig. 3 plots the levitation force versus gap curve with different number of time steps and the dependence of the
4. Experimental validation
The experimental validation is of great importance to support the development of any theoretical model and to confirm the practical application of the theoretical mode to the real world. Compared with the previous validations of the model, we will validate the 3-D finite-element model in a more comprehensive way, i.e., in which two different types of motion are considered, i.e., vertical movement (perpendicular to the surface of the magnetic rail) and transverse movement (parallel to the surface of the magnetic rail), are considered, and the associated magnetic force computed with our model are compared with the experimental data.
|wSC (mm)||lSC (mm)||tSC (mm)||Jab c(A/m2)||Ec (V/m)||U0 (eV)||ρf (Ωm)||α|
4.1. Brief introduction of the experiment
The self-developed maglev measurement system was used to measure the magnetic force of the bulk high-Tc superconductor (Wang, 2010). The Y-Ba-Cu-O sample used here is of single-domain with a rectangular shape, and its geometrical parameters and photo as well as its schematic drawing are presented in Table 3 and Fig. 4 respectively. The geometric parameters and photos of the two magnetic rail demonstrators (Rail_1 and Rail_2) used to generate the applied field for high-Tc superconductor are also shown in Fig. 4.
In the experiment, the sample was firstly bath-cooled in a liquid nitrogen vessel for several minutes to to insure the superconductive state was established at a certain position above the center of the magnetic rail, and then, for the vertical movement, the sample was put downward to an expected nearest gap (distance from the bottom of the high-Tc superconductor to the upper surface of the magnetic rail) and then upward to its original position in the levitation case, whereas in the suspension case, the movement was opposite; For the transverse movement, the sample was put downward (levitation case) or upward (suspension case) to its levitation height, and then it was forced to move along the transverse direction parallel to the surface of the magnetic rail (
4.2. Experimental validation of the computed results
In the calculation, the magnetic rail were calculated by a 3-D analytical model in which the finite geometry of each magnet used in the magnetic rail is taken into account (Ma, et al., 2009). With the restriction of the available experimental tools, the material parameters involved in the
4.2.1. Numerical results with different E-J constitutive relations and angular- dependence of critical current density formulas
Firstly, we evaluated the levitation force versus gap behavior with different angular-dependence of the critical current density formulations and
In the following calculation, we choose the elliptical model for the purpose of introducing a new way to describe the anisotropic behavior of the critical current density and power law model to describe the
4.2.2. Comparison of the levitation force under vertical movement
The vertical force of the Y-Ba-Cu-O above the center of the magnetic rail1 with different field-cooled positions was calculated and compared with the measured data. From the compared results presented in Figs. 6-8, we can see that, the computed results agree well with the measured results in both hysteresis loop as well as detailed values at a certain gap.
For the levitation case shown in Figs. 6-7, we can find from both the computed and measured results that, on the downward branch of the levitation force versus gap curve, the levitation force and slope of the curve are continuously enhanced with the decrease of the gap. For the same gap, the levitation force of the downward branch is always larger than that of the upward branch, and this reveals an obvious hysteresis behavior of the levitation force. Furthermore, the levitation force versus gap behavior was calculated and measured another two times after the first one for the field-cooled test case at 25 mm above the magnetic rail1. It can be seen clearly that the computed results also compare well with the measured data for the second time and third time. This further confirms the validation of the 3-D finite-element method.
For the suspension test case shown in Fig. 8, the suspension force versus gap curve of both computed and measured cases indicates that, according to the stiffness defined in (Hull, 2000), the suspension force increases with the gap and its stiffness is always positive before the maximum absolute value of the suspension force is achieved at a certain gap. Therefore, the suspension system is always stable within this gap. The suspension force will decrease when the gap is further increased and the suspension system becomes unstable. Also, there is a clear hysteresis behavior of the suspension force by comparing the upward and downward branch of the curve. In addition, we also presented the computed results with flux flow and creep model, and the good agreement between the results of power law model and flux flow and creep model demonstrates that, the two
4.2.3. Comparisons of the magnetic force under transverse movement
In order to verify the robustness of the performance of the 3-D finite-element model, the Rail_2 shown in Fig. 4, which is a Halbach array (Halbach, 1985), was employed to produce the applied field in this section.
During the transverse movement, both the vertical force and transverse force are a function of the lateral displacement. The compared results between the numerical results and measured results for different cases, i.e., levitation case with field-cooled above the levitation position, field-cooled at the levitation position, and suspension case with field-cooled below the suspension position, are presented in Figs. 9-11, respectively.
Both the numerical results and measured results shown in Figs. 9-11 indicate that, the absolute value of the transverse force increases with the lateral displacement and the
direction of the transverse force is opposite to the transverse movement, which indicates an inheret stable levitation can be acquired. Also, the magnetic force (i.e., the vertical force and the transverse force) are hysteretic as a function of the lateral displacement. Despite that the compared results of the transverse case is not as good as that of vertical case, as a whole, the numerical results are well comparable to the measured results in quality especially for the suspension case shown in Fig. 11. The fitting value of the critical current density in the
5. Optimization of the magnetic rail using the 3-D finite-element model
Magnetic rail is a key component to privide the applied magnetic field for the present magnet levitation system using bulk high-Tc superconductor, and the cost spend in building the magnetic rail occupies most part of the entire investment because the magnetic rail is required along the whole line. It is thereby meaningful to optimize the structure and geometric parameters of the magnetic rail in the purpose of getting a magnetic rail that holds the required levitation capability with a reduced cost. In this aspect, a lot of previous work has been reported and the dependence of the levitation force/guidance force on the parametes of the magnetic rail has been invesigated. However, all of these results were concluded from the numerical data calculated by a 2-D model that can just fit the experimental results in quality but fails in quantity with a reasonable value of critical current density (Song, et al., 2006; Dias, et al., 2010).
|wSC (mm)||lSC (mm)||tSC (mm)||Jab c(A/m2)||Ec (V/m)||U0 (eV)||α|
In this section, basing on the 3-D finite-element model introduced in this chapter, we calculate the levitation force and guidance force of three Y-Ba-Cu-O bulks samples above two differnt magnetic rails deriving from the traditional Halbach array. The geometric parameters of magnetic rail such as height, width are variable in the calculation, and then the depedence of levitation capability of the bulk Y-Ba-Cu-O on those parameters was studied. Compared with the previous work, the merit of the present calculation is that, the computed levitation force/guidance force is comparable to the real system with reasonable vaule of the critical current density and thus, the computed results can be used to conduct the practical design directly.
The geometric and material parameters of the Y-Ba-Cu-O sample were shown in Table 4 The speed of the samples in both vertical and transverse direction is 1 mm/s and the magnetization
As for the structure of the magnetic rail, Halbach array is a better choice than the original type used in the high-Tc superconducting maglev train demonstrator because this structure can concentrate the magnetic field to its upper space where the high-Tc superconductors are placed, and thus can improve the utilization of the magnetic field (Jing, 2007). From the basic structure of the Halbach array shown in Fig. 12, we can derive two different types of magnetic rail, i.e., one has three permanent magnets magnetized in the horizontal direction and two permanent magnets magnetized in the vertical direction, the other has three permanent magnets magnetized in the vertical direction and two permanent magnets magnetized in the horizontal direction. These two magnetic rails derived from the Halbach array are presented in Fig. 12.
In the calculation, we ignore the possible interaction among the Y-Ba-Cu-O samples for simplicity, and calculate only two samples beacuse of the symmetry of the levitation system shown in Fig. 13. In the default case, the high-Tc superconductors were field-cooled at a position of 30 mm above the surface of the magnetic rail for the calculation of the levitation force, and for the calculation of the guidance force, the tranverse movement occurs at the same height as the field-cooled position, that was 12 mm above the surface of the magnetic rail. The main parameters that should be optimized in the two structure, i.e., Rail_A and Rail_B shown in Fig. 12, are the ratio between the width of two different magnetized magnets, the width of and the height of the magnetic rail. The following section shows the computed results of the optimization by varying those parameters.
5.1. Width ratio of the two different magnetized magnets
In this section, the levitation force and guidance force on the high-Tc superconductors with the variation of the width ratio, i.e.,
For the case of vertical movement, twenty-one different width ratios from zero to infinity were considered and the changing curve of the levitation force along with the width ratio at position of 5, 10, 15 and 20 mm above the Rail_A and the Rail_B was shown respectively in Fig. 14(a) and Fig. 14(b). Note that the extreme case with a width ratio of zero or infinity denotes that Halbach struture disappears and permanent magnets employed in the Rail only have one magnitized direction (vertical or horizontal direction). Both Fig. 14(a) and Fig. 14(b) display that, the levitation force, at all positions we presented, increases with the growth of the width ratio and reaches to a maximum value when the width ratio was ～0.83 for Rail_A and was ～1 for Rail_B and then drops with continuous growth of the width ratio. This finding indicates, the halbach array has a better performance because the levitation
force at the extreme case is always the smallest one as has been verified by experiment (Jing, et al., 2007; Sotelo, et al., 2010), on the other hand, the optimized struture for Rail_A is that the width of magnet magnetized in horizontal direction is slightly larger than that magnetized in vertical direction, but for Rail_B, the two type magnets have an identical width ratio.
For the case of the transverse movement, only eleven different width ratios around 1 were considered because larger levitation force can be obtained in that area according to the above computed results of levitation force. The high-Tc superconductors have a field-cooled height of 12 mm and then were drived transversely at the same height with a maximum lateral displacement of 6 mm. Fig. 15 presents the guidance force with respect to the width ratio for the Rail_A and the Rail_B. We can find from this figure that, the guidance force exhibits a same tendency with the growth of the width ratio as that found in the case of levitation force, but the width ratio where the largest guidance force occurs is found to be 1.22～1.5 for Rail_A and is still ～1 for Rail_B.
As a whole, we suggest that, for the Halbach array as the magnetic rail used in the maglev train, the optimized width ratio between the vertical and transverse magnetized magnet is ～1.
5.2. Total width of the magnetic rail
In this calculation, the total width of both rails was a variable parameter with a fixed height of 30 mm and a fixed width ratio of 1.
Fig. 16 shows the changing curve of the levitation force on the high-Tc superconductors at positions of 5, 10, 15 and 20 mm above the Rail_A and Rail_B with the growth of the total width from 60 mm to 170 mm. These figures show that, with the increase of the position, the total width where the maximum value of the levitation force appears is shift from small to large value, e.g., the levitation force increases almost linearly with the total width at the position of 20 mm for both rails and the maximum value of the levitaion force even does not appear within our calculational range. This figure also indicates that, the increase of the total width does not always bring an ehencement of the levitation force especially for the case at a
low position. Of course, if a larger levitaion capability is required at a high position, it is a viable way to lengthen the total width of the rail. For the typical position of 15 mm in the maglev train, it seems that, the optimized value of the total width appears around 130 mm for both rails because the slope of the curve begins to dcrease at this value.
Fig. 17 shows the changing curve of the guidance force on the high-Tc superconductors at a lateral displacement of 6 mm with the growth of the total width from 60 to 170 mm. From this figure, we can find that, the guidance force also increases firstly and then decreases with the growth of the total width, and the maximum value of the guidance force occurs around 120 mm for Rail_A and around 135 mm for Rail_B. Although the total width where the maximum value of the guidance force occurs is scattered above Rail_A and Rail_B, the variation of the guidance force above both rails in the range of 120～140 mm is not evident. It is therefore this range can be considered as the optimized range which is comparable to the total width of the high-Tc superconductors (126 mm) in determining the total width of the rail for a practical design.
5.3. Height of the magnetic rail
The height of the magnetic rail is another factor influencing the levitation capability of the high-Tc superconductor. Here, we fixed the width ratio to be 1 and total width to be 130 mm, and varied the height of the magnetic rail from 15 mm to 100 mm. The levitation forces above the Rail_A and Rail_B were plotted as a function of the height and the associate curves were given in Fig. 18. This figure displays clearly that, no matter the position where the high-Tc superconductors are placed, the levitation force increases drastically at first and then goes into gradually a saturated state with heightening the rail. This phenomenon indicates that, considering the cost of the rail, it is not reasonable to get a better levitation performance by increasing the height of the rail when the height is already high enough.
6. Conclusion remarks
On the basis of Maxwell’s equations and Helmholtz’s theorem, the 3-D governing equations containing the anisotropic behavior of the HTS were deduced at length by introducing a current vector potential T and a simplified expression of the resistivity tensor for the high-Tc superconductor. The two common models to handle the highly nonlinear
The computed results of the levitation force of a bulk high-Tc superconductor above a magnetic rail indicate that, the levitation force and associated hysteresis behavior will approach to a saturated state with the increment of the mesh density or the number of the time steps. This result is consistent with the finite-element theory, and also, supports the approach used to simplify the coupling problem between the differential and integral term presented in the governing equations.
Subsequentely, the 3-D finite-element model was validated by comparing the computed magnetic forces of a bulk Y-Ba-Cu-O sample with the measured data under vertical and transverse movements. Basing on the 3-D finite-element model, we also found that, the computed results of magnetic force of the high-Tc superconductor are almost identical for different angular-dependence of critical current density formulations (i.e., Yang’s model and elliptical model) and
Lastly, using this 3-D finite-element model, we conduct a preliminary numerical work with aim of geting an optimized geometric parameter of the magnetic rails derived from the Halbach array. The results show that, when the width ratio of the two different magnetized magnets used in the magnetic rail is approximately identical and the total width of the rail is roughly indentical to the width of the high-Tc superconductors, the rail exhibits a better performance in considering both the levitation capability and the cost (be proportional to the voulme of the rail). Moreover, the levitation force has a saturated tendency with increasing continuely the height of the rail, so it is not reasonable to get a better levitation performance by increasing the height of the rail when the height is already high enough.
This work was supported by the National Natural Science Foundation of China under Grant 51007076 and 50777053, and the Innovation Foundation of Southwest Jiaotong University for Ph.D. Candidate. The authors would like to thank Dr. Frank N. Werfel of the Adelwitz Technologiezentrum GmbH (ATZ) for providing the Y-Ba-Cu-O sample employed in the experiment and to thank Dr. Hong-Hai Song, Dr. Zi-Gang Deng, Dr. Yi-Yun Lu, Dr. Min-Xian Liu, Dr. Jun Zheng, Dr. Fei Yen, Mr. Wei Liu, Mr. Qun-Xu Lin, Mr. Dong-Hui Jiang for their many fruitful discussions
Alloui L. Bouillault F. Mimoune S. M. 2009Numerical study of the influence of flux creep and of thermal effect on dynamic behaviour of magnetic levitation systems with a high-Tc superconductor using control volume method.
Alonso D. R. Coombs T. A. Campbell A. M. 2004Numerical analysis of high-temperature superconductors with the critical-state model.
Anderson P. W. 1962Theory of flux creep in hard superconductor.
Bean C. P. 1964Magnetization of high-field superconductors.
Brandt E. H. 1989Levitation in physics.
Brandt E. H. 1996Superconductors of finite thickness in a perpendicular magnetic field: Strips and slabs.
Cui X. 1989A new preconditional conjugate gradient algorithm.
Davis L. C. Logothetis E. M. Soltis R. E. 1988Stability of magnets levitated above superconductors.
Dias D. H. N. Motta E. S. Sotelo G. G. Andrade Jr R. D. 2010Experimental validation of field cooling simulations for linear superconducting magnetic bearings.
Dinger T. R. Worthington T. K. Gallagher W. J. Sandstrom R. L. 1987Direct observation of electronic anisotropy in single-crystal Y1Ba2Cu3O7-x.
Fujiwara K. Nakata T. Fusayasu H. 1993Acceleration of convergence characteristic of the ICCG method.
Gou X. F. Zheng X. J. Zhou Y. H. 2007aDrift of levitated/suspended Body in high-Tc superconducting levitation systems under vibration-part I: A criterion based on magnetic force-gap relation for gap varying with time.
Gou X. F. Zheng X. J. Zhou Y. H. 2007bDrift of levitated/suspended Body in high-Tc superconducting levitation systems under vibration-Part II: drift velocity for gap varying with time.
Grilli F. Stavrev S. Le Floch Y. Costa-Bouzo M. Vinot E. Klutsch I. Meunier G. Tixador P. Dutoit B. 2005Finite-element method modeling of superconductors: from 2-D to 3-D.
Halbach K. 1985Application of permanent magnets in accelerators and electron storage rings (invited).
Hashizume H. Sugiura T. Miya K. Ando Y. Akita S. Torii S. Kubota Y. Ogasawara T. 1991Numerical analysis of a. c. losses in superconductors.
Hull J. R. Cansiz A. 1999Vertical and lateral forces between a permanent magnet and a high-temperature superconductor.
Hull J. R. 2000Superconducting bearings.
Jing H. Wang J. Wang S. Wang L. Liu L. Zheng J. Deng Z. Ma G. Zhang Y. Li J. 2007A two-pole Halbach permanent magnet guideway for high temperature superconducting Maglev vehicle.
Kershaw D. S. 1978The incomplete cholesky-conjugate gradient method for the iterative solution of systems of linear equations.
Kim Y. B. Hemptead C. F. Strnad A. R. 1962Critical persistent currents in hard superconductors.
Kordyuk A. A. 1998Magnetic levitation for hard superconductor.
Krusin-Elbaum L. Malozemoff A. P. Yeshurun Y. Cronemeyer D. C. Holtzberg F. 1989Temperature dependence of lower critical fields in Y-Ba-Cu-O crystals.
Lu Y. Y. Wang J. S. Wang S. Y. Zheng J. 20083D-Modeling numerical solutions of electromagnetic behavior of HIGH-TC SUPERCONDUCTORC bulk above permanent magnetic guideway.
Luo Y. Takagi T. Miya K. 1999Reduction of levitation decay in high Tc superconducting magnetic bearings.
Ma G. T. Liu H. F. Wang J. S. Wang S. Y. Li X. C. 20093D modeling permanent magnet guideway for high temperature superconducting maglev vehicle application.
Ma K. B. Postrekhin Y. V. Chu W. K. 2003Superconductor and magnet levitation devices.
Matsushita T. 2007
Mikitik G. P. Brandt E. H. 2000Critical state in thin anisotropic superconductors of arbitrary shape.
Miya K. Hashizume H. 1988Application of T-method to A.C. problem based on boundary element method.
Murakami M. Oyama T. Fujimoto H. Gotoh S. Yamaguchi K. 1991Melt processing of bulk high Tc superconductors and their application.
Napoli A. D. Paggi R. 1983A model of anisotropic grain-oriented steel.
Navau C. Sanchez A. 2001Magnetic properties of finite superconducting cylinders. II. Nonuniform applied field and levitation force.
Pecher R. Mc Culloch M. D. Chapman S. J. Prigozhin L. Elliot C. M. 20033D-Modelling of bulk type-II superconductors using unconstrained H-formulation.
Prigozhin L. 1997Analysis of Critical-State Problems in Type-II Superconductivity,”
Qin M. J. Li G. Liu H. K. Dou S. X. Brandt E. H. 2002Calculation of the hysteretic force between a superconductor and a magnet.
Rhyner J. 1993Magnetic properties and AC-losses of superconductors with power law current-voltage characteristics.
Sanchez A. Navau C. 2001Magnetic properties of finite superconducting cylinders. I. Uniform applied field.
Sanchez A. Valle N. D. Pardo E. Chen D. X. Navau C. 2006Magnetic levitation of superconducting bars.
Sawamura M. Tsuchimoto M. 2000Numerical analysis for superconductor in sheet and bulk form,”
Schultz L. Haas O. Verges P. Beyer C. Röhlig S. Olsen H. Kühn L. Berger D. Noteboom U. Funk U. 2005Superconductively levitated transport system-the SupraTrans project.
Song H. H. Wang J. S. Wang S. Y. Ren Z. Y. Wang X. R. Haas O. Fuchs G. Schultz L. 2006Studies of YBCO electromagnetic properties for high-temperature superconductor maglev technology. in
Sotelo G. G. Dias D. H. N. Andrade Jr R. D. Stephan R. M. 2010Tests on a Superconductor Linear Magnetic Bearing of a Full-Scale MagLev Vehicle.
Takagi T. Sugiura T. Miyata K. Norimatsu S. Okamura K. Miya K. 1988Iterative solution technique for 3-D eddy current analysis using T-method.
Ueda H. Azumaya S. Tsuchiya S. Ishiyama A. 20063D electromagnetic analysis of levitating transporter using bulk superconductor.
Uesaka M. Yoshida Y. Takeda N. Miya K. 1993Experimental and numerical analysis of three-dimensional high-Tc superconducting levitation systems.
Wang J. S. Wang S. Y. Zeng Y. W. Huang H. Y. Luo F. Xu Z. P. Tang Q. X. Lin G. B. Zhang C. F. Ren Z. Y. Zhao G. M. Zhu D. G. Wang S. H. Jiang H. Zhu M. Deng C. Y. Hu P. F. Li C. Y. Liu F. Lian J. S. Wang X. R. Wan L. H. Shen X. M. Dong X. G. 2002The first man-loading high temperature superconducting maglev test vehicle in the world.
Wang J. S. Wang S. Y. 2010
Wu J. Z. Hsieh P. Y. Mc Guire A. V. Schmidt D. L. Wood L. T. Shen Y. Chu W. K. 1991Anisotropic properties of the high-quality epitaxial YBa2Cu3O7-δ (110) thin film.
Yamafuji K. Mawatari Y. 1992Electromagnetic properties of high Tc superconductors: relaxation of magnetization.
Yang W. M. Feng Y. Zhou L. Zhang P. X. Wu M. Z. Chen S. K. Wu X. Z. Gawalek W. 1999The effect of the grain alignment on the levitation force in single domain YBa2Cu3Oy bulk superconductors.
Yang Y. Zheng X. J. 2007Method for solution of the interaction between superconductor and permanent magnet.
Yoshida Y. Uesaka M. Miya K. 1994Magnetic field and force analysis of high-Tc superconductor with flux flow and creep.
Wang Jiasu and Wang Suyu, 2005Synthesis of Bulk Superconductors and Their Properties on Permanent Magnet Guideway. In: Anant Narlikar Ed., Frontiers in Superconducting Materials (Springer Verlag, Germany), 885 912