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Mathematical Problems in Engineering

Volume 2011 (2011), Article ID 927876, 28 pages

http://dx.doi.org/10.1155/2011/927876

## Exact Solution for the Time-Dependent Temperature Field in Dry Grinding: Application to Segmental Wheels

^{1}Cátedra Energesis de Tecnología Interdisciplinar, Universidad Católica de Valencia, 46002 Valencia, Spain^{2}Departamento de Matemáticas, Universidad de Pinar del Río, 20200 Pinar del Río, Cuba^{3}Instituto Universitario de Matemática Pura y Aplicada, Universidad Politécnica de Valencia, 46022 Valencia, Spain

Received 21 February 2011; Accepted 1 April 2011

Academic Editor: Ezzat G. Bakhoum

Copyright © 2011 J. L. González-Santander et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

#### Abstract

We present a closed analytical solution for the time evolution of the temperature field in dry grinding for any time-dependent friction profile between the grinding wheel and the workpiece. We base our solution in the framework of the Samara-Valencia model Skuratov et al., 2007, solving the integral equation posed for the case of dry grinding. We apply our solution to segmental wheels that produce an intermittent friction over the workpiece surface. For the same grinding parameters, we plot the temperature fields of up- and downgrinding, showing that they are quite different from each other.

#### 1. Introduction

A major technological challenge in the grinding of metallic plates [1–5] is how to avoid thermal damage to the workpiece. The grinding process transforms large amounts of mechanical energy into heat, which primarily affects the contact area between the workpiece and the wheel. It is therefore of great industrial importance to determine the temperature distribution within the workpiece, and its maximum, in order to avoid thermal damage.

Despite the fact that there have been studies of the temperature field solving the heat equation numerically [6, 7], an analytical approach is of great interest [8] for two reasons. Firstly, explicit expressions for the dependence of the temperature field with respect to the grinding parameters can be obtained. Secondly, the rapid presentation of results allows the industry to monitor the grinding process on line.

This paper is organized as follows. Section 2 presents the Samara-Valencia model [9]. This model is used in Section 3 to derive a closed analytical solution for the evolution of the temperature field in dry grinding, for any time-dependent friction profile between the grinding wheel and the workpiece. Section 4 applies the result obtained in the previous section to intermittent grinding, for both up- and downgrindings. Section 5 analyzes some important variables in continuous grinding, such as the location of the maximum temperature and the relaxation time, which can be applied to intermittent grinding. We compare also the stationary regime of continuous grinding with the quasistationary regime of intermittent grinding. In Section 6, we present some numerical results, comparing continuous and intermittent grinding. Our conclusions are summarized in Section 7.

#### 2. Samara-Valencia Model

The Samara-Valencia model setup is depicted in Figure 1. The workpiece moves at a constant speed and is assumed to be infinite along and , and semiinfinte along . The plane is the surface being ground. The contact area between the wheel and the workpiece is an infinitely long strip of width located parallel to the axis and on the plane . Both the wheel and the workpiece are assumed to be rigid. Although the equations below allow for the case of wet grinding, we will consider in this paper the case of dry grinding. The Samara-Valencia model [9] solves the convection heat equation subject to the initial condition, and the boundary condition, where and . The first term of (2.3) models the application of coolant over the workpiece surface considering as the heat transfer coefficient. The second term, , represents the heat flux entering into the workpiece. This heat flux is generated on the surface by friction between the wheel and the workpiece. The solution of the Samara-Valencia model (2.1)–(2.3) may be presented as the sum of two terms, where Notice that contains the friction function , and contains the temperature field on the surface and the heat transfer coefficient .

#### 3. Theorem for Dry Grinding

##### 3.1. Dry Grinding

When no coolant is applied to the workpiece, we can consider the workpiece to be isolated from the environment. According to Newton's cooling law, this means that there is no heat flux from the workpiece to the environment, thus the heat transfer coefficient is zero, In this case of dry grinding, the expression for given in (2.6) becomes In order to tackle the integral equation given in (3.2), let us define the following integral operators where Therefore, taking into account (3.3), we may rewrite (2.4) as

##### 3.2. The Operator

Let us calculate the operator over the frictional term of the temperature field. According to (2.5), may be expressed as Therefore, substituting (3.7) in (3.5), and reordering the integrals by Fubini’s theorem, we obtain Expanding the exponent of the integrand given in (3.8), we arrive at The last integral given in (3.9) can be calculated [10, Equation 3.323.2], so that, Once again, expanding the exponent of the last integrand given in (3.10) and simplifying, we arrive at Let us define We can calculate (3.12) performing the substitution, , and introducing the Heaviside function , so that, Substituting (3.13) in (3.11) and simplifying, we get

##### 3.3. The Operator

Substituting the expression obtained in (3.14) into (3.4) and reordering the integrals, we have Let us define Since , the integral given in (3.16) can be expressed in the following way: In order to calculate (3.17), we can perform the following substitutions: , and , leading to Therefore, substituting (3.18) in (3.15) and changing the integration order, we arrive at Remembering the expression for given in (2.5), we conclude

##### 3.4. Resolution by Successive Approximations

According to (3.2), in order to evaluate , we have to know the temperature field on the surface, . At zeroth order approximation, , we can consider that the temperature field will be given by the term involving friction only, that is, according to (2.5). So that, In order to get the first-order approximation , we can substitute the zeroth order (3.21) in (3.3), Thus, the temperature field at first order is or according to (3.22), In general, the th approximation is where the initial value is given by (3.21). Applying now (3.20) to (3.22), we can rewrite the first-order approximation as In order to evaluate the second order, we can substitute (3.26) in the recurrence equation (3.25) for . Taking into account that the integral operator is linear, we obtain where we have applied (3.20) once again. Repeating the same steps, we get at third order Looking at the coefficients appearing in the first orders, (3.26), (3.27), and (3.28), we may establish the following conjecture for the th order: that can be proved by induction, The temperature field will be the infinite order approximation, thus taking the limit of (3.29), results in Applying (3.20), we may check that (3.31) is a solution of the integral equation given in (3.6), Taking into account (2.5), we conclude that the time evolution of the temperature field may be expressed as

##### 3.5. Uniqueness of the Solution

###### 3.5.1. Bound Limit for *ℶ*_{0}

To prove the uniqueness of the solution of the integral equation (3.6), let us calculate first the value of the operator over a constant. According to (3.5), we have Performing the substitution: , (3.33) results in Applying (3.35) to (3.4), we have Performing the substitution: , we have Therefore,

Let us consider now a function whose maximum value taking is , that is, Applying to (3.39) and taking into account that is a linear operator, Thus, according to (3.38), Note that, if we apply to (3.39) and we take into account (3.37), we have So, in general, for all ,

###### 3.5.2. Resolution of the Uniqueness

If and are solutions of (3.6), we have Subtracting (3.45) from (3.44) and taking into account that is a linear operator, Taking in (3.46), Recursive substitution of (3.47) yields If we take in (3.43) as a function , according to (3.48), we have that, for all , where is the maximum value of . Taking the limit in (3.50), so that, Note that in (3.48) we can exchange labels and , Thus, taking now the function we obtain that that is, From (3.52) and (3.56), we conclude that both solutions on the surface are equal, Applying to (3.57), and substituting (3.58) in (3.44), we have that Comparing (3.45) with (3.59), we finally obtain Therefore, the solution given in (3.33) is the only solution of (3.6).

#### 4. Intermittent Grinding

Equation (3.31) is a generalization of the result presented in [11] since now the transient regime is considered and any type of time-dependent friction profile is allowed. In the next section, we will apply (3.31) to calculate the time-dependent temperature field produced by an intermittent grinding of a segmental wheel (Figure 2).

##### 4.1. Intermittence Function

Let us model the friction due to a toothed wheel, which can contact the workpiece within . Therefore, we will call this zone, *contact zone*. Figures 3 and 4 show the *friction zone* highlighted in red within the limits and for two different times and . The wheel has a spatial period , where is the distance between teeth and is the tooth width. The wheel teeth move at a speed , where is the angular velocity and is the wheel radius. When more than two teeth touch simultaneously the contact zone , the friction zone is split as Figure 5 shows. For a given instant , the incoming heat flux enters the workpiece through the friction zone: , , where indicates a wheel tooth. Notice that there can be up to teeth within the contact zone, where
Note, also, that the friction limits are time dependent: and . If the incoming heat flux is constant for every point where friction occurs, we may write the friction function as
where is the Heaviside function. In order to know the friction limits of the wheel teeth which enters into the contact zone, that is, and , let us define the spatial period,
According to Figure 5, the points, , are initially over the period ,
where we have defined a boolean variable , in order to define the rotation of the wheel: , downgrinding; , upgrinding, as Figure 6 shows. If we want a periodic repetition of the friction limits over the period , we may define the function
We want as well that , thus,
Similarly, since the tooth width is ,
The and functions are given by

##### 4.2. Temperature Field

Substituting (4.2) in (3.33), we obtain Let us evaluate the integral over the variable in (4.9), Performing the substitution, and taking into account the properties of the error function, we get where we have defined the function Substituting (4.12) in (4.9), we obtain the following expression for the temperature field:

#### 5. Continuous Grinding

##### 5.1. Stationary Regime

In order to calculate the temperature field for the case of continuous friction, we can take in (4.7)-(4.6) the constant values of the contact zone, Therefore, we can redefine (4.12) as obtaining, according to (4.13), the following temperature field: The stationary regime is reached when the temperature field does not vary in time, In the case of continuous grinding, the time derivative is Taking the limit of (5.4), knowing that erf, we can check that the stationary regime is reached when : so that,

##### 5.2. Quasistationary Regime

Notice that intermittent grinding never reaches a stationary regime, since the heat source produced by friction is pulsed. This is not the case of continuous grinding, where the stationary regime is reached asymptotically for . Therefore, for continuous grinding, we may define a relaxation time that provides us an idea of how rapid the stationary regime is reached in practice. It turns out that this relaxation time, defined for the continuous case, is a good temporal reference in order to plot the temperature field in the case of intermittent grinding. Even though intermittent grinding never reaches a stationary regime, we may define a quasistationary regime in which the temperature field is periodically stable. Since and are periodic functions (4.6)-(4.7), according to (4.14), we may define the quasistationary regime as According to Figure 5, the temporal period of the friction function in a fixed point is However, the global consideration of the plot indicates the following temporal period: In view of (3.31), we may conclude that possesses the same global and point periods and as the friction function .

##### 5.3. Maximum Temperature

Since the error function erf is an increasing function for all , we have Therefore, the temperature on a given point of the workpiece is a monotonically increasing function, Equation (5.12) means that the maximum temperature must be reached in the stationary state, . Moreover, as in (5.11), we have so that, for , Equation (5.14) indicates that maximum temperature must be localized on the surface, . From (5.12) and (5.14), we conclude that the maximum temperature must be reached on the surface in the stationary regime, This result agrees with [11].

###### 5.3.1. Location of the Maximum Temperature

Denoting the stationary regime in the case of continuous friction as according to [12], we have, where is the modified Bessel function of zeroth order [13, Section 9.6.], and are spatial dimensionless coordinates, and is a characteristic temperature, According to what we have seen in (5.15), the maximum temperature is reached on the surface at the stationary regime. Thus, we have to analyze the maximum of the function given in (5.17) taking , that is, In order to determine the location of the maximum on the surface, firstly let us calculate the points where has a null derivative (extrema points), Therefore, satisfies where When , the workpiece moves as indicates Figure 1, so that, now on we will consider . Since the incoming heat flux into the workpiece is a positive magnitude, , we have, . Moreover, since is positive for positive arguments [13, Section 9.6.], the integrand of (5.21) is also positive, thus,

*Location of the Extrema*

Assume first that , so that (5.19) results in
We may rewrite (5.24) as , where . Since is positive for positive arguments [13, Section 9.6.], we have for all ,
that is, , for . Therefore, we conclude

Assume now that , so that (5.21) becomes
Performing the change of variables , (5.27) is equivalent to , where . Due to the integral representation [13, Equation 9.6.24],
and since for all , , we have for all ,
So that, , for . That is, (5.27) is not satisfied for ,

Finally, assume that , so that and , and therefore, according to (5.22),
Since is a continuous function in and,
according to Bolzano’s theorem,

*Uniqueness of the Extremum and Identification as Maximum*

Since is a positive and monotonically decreasing function for positive arguments, , for , [13, Section 9.6.] we have that is a monotonically decreasing function for ,
Therefore, according to (5.33),
On the one hand, according to (5.26), (5.30), and (5.35), has a unique extremum in and this one always occurs within the interval . On the other hand, from (5.19) we can see that
Since is a positive (5.23), continuous and differentiable function, which satisfies (5.36), the only possibility is that the extremum corresponds to a global maximum. Therefore, just compute a root of (5.21) within the interval , that is taking (5.31), in order to get the location on the surface of the maximum temperature,
There is an equivalent, but more elaborated proof, in [14].

##### 5.4. Relaxation Time

In order to estimate how rapid the transient regime is, according to (5.4), we will be close to it when, for a certain time , is satisfied. Notice that (5.38) depends on the workpiece point chosen for the evaluation of . We can define the relaxation time , as the time that satisfies (5.38) over the maximum temperature point. According to (5.15), that point must be on the surface in the stationary state, , thus, Equation (5.39) can be solved numerically. In order to solve it approximately, we can expand the following function up to the first order, near the stationary regime , [13, Equation ]: Therefore, Substituting (5.41) in (5.39), we have the following approximated equation: Using the Lambert function [15], we can derive the relaxation time from (5.42), arriving at, Notice that in (5.43), the relaxation time is independent of the localization of the maximum on the surface , thus it can be computed much more rapidly.

#### 6. Numerical Analysis

For the plots presented in this section, we have taken as grinding parameters: , m/s, and . We have considered as well a VT20 titanium alloy workpiece, whose thermal properties are and [16]. Following the procedure described in Section 5.3, the maximum temperature in continuous grinding and its location on the workpiece surface is In order to evaluate the relaxation time, according to (5.38), we have taken a very small parameter K/s. Taking into account (6.1), we may solve numerically (5.39) and compute the approximation given in (5.43), obtaining Notice that the results given in (6.2) coincide in order of magnitude.

For the case of intermittent grinding we have taken in (4.1), (4.3), (4.4), and (4.7), the following wheel parameters: and , and a wheel velocity over the workpiece surface . According to this data, the point period of the quasistationary regime is , and the global period is . Figures 7, 8, and 9 show the time evolution of the workpiece surface temperature for , for continuous and intermittent up- and downgrinding, respectively. As can be seen, the temporal evolution of up and down grinding is quite different from each other, but in both cases, the continuous profile is a limit boundary. Figure 10 compares the temperature time evolution in of continuous grinding with intermittent up- and downgrinding. We may highlight that the relaxation time obtained for the continuous case is a good estimation for the transient regime in the intermittent case. We may notice also how upgrinding nearly saturates the maximum temperature of the continuous case, but this does not occur in downgrinding. We may evaluate numerically the maximum temperature, both intermittent up- and downgrindings,

Figure 11 shows the time evolution of the quasistationary regime on the surface for a friction period . For , the temperature oscillates as a wave. This is because the heat flux pulses produced at the contact zone are propagated along the surface just ground. Figure 12 shows the time evolution of the temperature in for . On the one hand, we may check that the quasistationary regime has a period , as it was commented in (5.9). On the other hand, we may notice that the quasistationary regime is reached when the temperature in the continuous case is saturated. Therefore, the relaxation time defined for the continuous case is a good measurement for the transient regime when we have a quasistationary regime in intermittent grinding. In Figures 14 and 15, we have plotted the temperature fields at , in the cases of up- and downgrinding, respectively. We may realize that both temperature fields are quite different from each other. Figure 13 shows the field temperature for the continuous case. If we compare the temperature field in the continuous case with the intermittent one (up- or downgrinding), we may observe that an intermittent friction distorts the temperature field producing thermic waves inside the workpiece.

#### 7. Conclusions

We have derived a closed analytical solution for the time evolution of the temperature field in dry grinding for any time-dependent friction function. Our result is based on the Samara-Valencia model [9], solving explicitly the evolution of temperature field for the case of dry grinding. We find this solution solving a recurrence equation by successive approximations. We have proved that this solution is unique. An analytical solution of this type has the advantage to be straightforwardly computable, plotting the graphs very rapidly. Also, the dependence of the grinding parameters on the temperature field can be studied. The latter is quite useful for the engineering optimization of the grinding process.

We apply our solution to continuous and intermittent up- and downgrinding. We have tested numerically that the time evolution of up- and downgrinding is quite different from each other. In continuous grinding, we have proved that the maximum temperature occurs at the stationary regime within the friction zone on the surface. In order to graph the evolution of the temperature field, we have obtained a useful approximation for the characteristic time of the transient regime. Comparing the plots of continuous and intermittent grinding for the same workpiece and grinding parameters, we conclude that the behavior of the intermittent case is more complicated in detail, but in general the magnitude of temperature field is lower. The latter is quite understandable because, in intermittent grinding, the amount of energy per unit time entering into the workpiece due to friction is less than in the continuous case. Therefore, the temperature plot for the continuous grinding acts as a boundary for the intermittent case.

Also, we have tested numerically that the relaxation time obtained for continuous grinding is a good estimation for the characteristic time of the transient regime in the intermittent case. Finally, we have obtained an expression for the quasistationary regime in intermittent grinding, in which the field temperature oscillates periodically.

#### Acknowledgments

The authors wish to thank the financial support received from *Generalitat Valenciana* under Grant GVA 3012/2009 and from Universidad Politécnica de Valencia under Grant PAID-06-09.

#### References

- S. Malkin,
*Grinding Technology: Theory and Applications of Machining with Abrasives*, Ellis Horwood Ltd. and John Wiley and Sons, 1989. - C. Guo and S. Malkin, “Analysis of energy partition in grinding,”
*Journal of Engineering for Industry*, vol. 117, pp. 55–61, 1995. View at Publisher · View at Google Scholar - S. Malkin and R. B. Anderson, “Thermal aspects of grinding: 1—energy partition,”
*Journal of Engineering for Industry*, vol. 96, no. 4, pp. 1177–1183, 1974. View at Google Scholar - A. S. Lavine and B. F. von Turkovich, “Thermal aspects of grinding: the effect of heat generation at the shear planes,”
*CIRP Annals*, vol. 40, no. 1, pp. 343–345, 1991. View at Publisher · View at Google Scholar - A. S. Lavine, “An exact solution for surface temperature in down grinding,”
*International Journal of Heat and Mass Transfer*, vol. 43, no. 24, pp. 4447–4456, 2000. View at Publisher · View at Google Scholar · View at Zentralblatt MATH - M. Mahdi and Liangchi Zhang, “The finite element thermal analysis of grinding processes by ADINA,”
*Computers & Structures*, vol. 56, no. 2-3, pp. 313–320, 1995, Proceedings of the 10th ADINA Conference of Nonlinear Finite Element Analysis and ADINA. View at Publisher · View at Google Scholar - A. G. Mamalis, D. E. Manolakos, A. Markopoulos, J. Kundrák, and K. Gyáni, “Thermal modelling of surface grinding using implicit finite element techniques,”
*International Journal of Advanced Manufacturing Technology*, vol. 21, no. 12, pp. 929–934, 2003. View at Publisher · View at Google Scholar · View at Scopus - K. T. Andrews, M. Shillor, and S. Wright, “A model for heat transfer in grinding,”
*Nonlinear Analysis*, vol. 35, no. 2, pp. 233–246, 1999. View at Publisher · View at Google Scholar · View at Zentralblatt MATH · View at Scopus - D. L. Skuratov, Yu. L. Ratis, I. A. Selezneva, J. Pérez, P. Fernández de Córdoba, and J. F. Urchueguía, “Mathematical modelling and analytical solution for workpiece temperature in grinding,”
*Applied Mathematical Modelling*, vol. 31, no. 6, pp. 1039–1047, 2007. View at Publisher · View at Google Scholar · View at Zentralblatt MATH · View at Scopus - I. S. Gradsthteyn and I. M. Ryzhik,
*Table of Integrals, Series and Products*, Academic Press, New York, NY, USA, 7th edition, 2007. - J. L. González-Santander, J. Pérez, P. Fernández de Córdoba, and J. M. Isidro, “An analysis of the temperature field of the workpiece in dry continuous grinding,”
*Journal of Engineering Mathematics*, vol. 67, no. 3, pp. 165–174, 2010. View at Publisher · View at Google Scholar · View at Zentralblatt MATH - J. C. Jaeger, “Moving sources of heat and the temperature at sliding contracts,”
*The Royal Society of New South Wales*, vol. 76, pp. 204–224, 1942. View at Google Scholar - M. Abramowitz and I. Stegun,
*Handbook of Mathematical Functions*, NBS Applied Mathematics Series 55, NBS, Washington, DC, USA, 1972. - J. L. González-Santander,
*Modelización matemática de la transmisión de calor en el proceso del rectificado industrial plano*, Ph.D. thesis, Universidad Politécnica de Valencia, Valencia, Spain, 2009, http://hdl.handle.net/10251/4769. - R. M. Corless, D. J. Jeffrey, and D. E. Knuth, “A sequence of series for the Lambert W function,” in
*Proceedings of the 1997 International Symposium on Symbolic and Algebraic Computation*, pp. 197–204, ACM Press, Maui, Hawaii, USA, July 1997. - S. G. Glasunov and V. N. Moiseev,
*Constructional Titanium Alloys, Metallurgy*, Moscow, Moscow, Russia, 1974.