numerical modelling of ground surface topography: effect of traverse and helical superabrasive...
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MACHINE TOOL
Numerical modelling of ground surface topography: effectof traverse and helical superabrasive grinding with touch dressing
Shubham Kumar • S. Paul
Received: 18 April 2011 / Accepted: 10 February 2012 / Published online: 26 February 2012
� German Academic Society for Production Engineering (WGP) 2012
Abstract Grinding processes are often used for final
finishing of components because of their ability to satisfy
stringent requirements of surface roughness and dimen-
sional tolerance. Surface topography generated during
grinding depends upon many parameters like wheel
parameters, wheel velocity, downfeed, grit density etc. and
it also depends upon the type of grinding procedures (viz.
plunge grinding, traverse grinding, helical grinding, touch
dressing etc.) employed. Therefore, a correct examination
of the parameters and type of process employed to carry
out grinding are necessary. This paper is an attempt to
develop the relation between the different grinding
parameters and the grinding procedures like plunge, tra-
verse and helical superabrasive grinding with touch
dressing and the average surface roughness. For this pur-
pose, a numerical simulation technique has been imple-
mented to generate the grinding wheel topography. The
ground workpiece surface has also been generated by
simulating removal of work material depending upon the
trajectory of the abrasive grits on the grinding wheel
without taking rubbing and ploughing into consideration.
Keywords Grinding � Modelling � Surface topography �Surface roughness
List of symbols
a Semi apex angle of the square pyramidal grit
h Rotational angle of any grit
a Infeed or downfeed
b Base dimension of the grit
c Grit density per unit area
dg Average grit diameter
ds Diameter of the grinding wheels
h Height of the grit
ha Average grit depth of cut
x, z Coordinate of the grit tip
vg Grinding speed
vw Table speed in surface grinding
Ra CLA surface roughness
1 Introduction
Grinding is considered as a finishing operation in manu-
facturing and extensive studies have been carried out to
predict the surface roughness of the workpiece upon
grinding. This paper is concerned with the simulation of
wheel topography and the effect of various grinding
parameters and conditions on the roughness of the ground
workpiece. In this regard, research involving wheel
topography generation and surface roughness estimation
has been taken into consideration. The methods adopted for
estimation of surface roughness can be classified as
empirical and numerical [1]. The former method is based
on experimental results and the observations could only be
valid within the investigated experimental domain; there-
fore its universal usage is limited as the models developed
under a particular grinding condition that may not be
usable for roughness prediction under other conditions. The
numerical methods have been attempted to develop a
model which can be used universally.
S. Kumar (&) � S. Paul
Department of Mechanical Engineering, Indian Institute of
Technology, Kharagpur, West Bengal 721302, India
e-mail: [email protected]
S. Paul
e-mail: [email protected]
123
Prod. Eng. Res. Devel. (2012) 6:199–204
DOI 10.1007/s11740-012-0370-1
The methods reported in the literature for the estimation
of surface roughness using numerical techniques consist of
two processes [1–13]; namely, the simulation of the wheel
topography for a given grit density and grit size; and the
simulation of the surface topography involving the mod-
elling of the kinematic interaction of the wheel with the
ground surface. Pandit and Wu [2] have modelled grinding
wheel surface profile as a continuous autoregressive pro-
cess and validated the model by considering eight different
grinding wheels. They also concluded that the proposed
characterization can be used for surface roughness profiles.
Wang and Moon [3] proposed multi-resolution method to
simulate the grinding wheel, wherein the grinding wheel
and the grits are modelled as a convolution of random
waves. They have investigated plunge surface grinding.
Salisbury et al. [4, 5] have modelled the grinding wheel
surface as a set of Fourier spectrum and have studied the
effect of various levels of table speed, wheel speed, wheel
type and grinding wheel frequency characteristic i.e. the
amplitude on the surface roughness of the workpiece for
single pass surface grinding mode. Zhou and Xi [6]
developed a truncated model to simulate the grinding
wheel by taking into consideration the random distribution
of the grain protrusion heights and calculated the surface
roughness using this model for traverse surface grinding
mode. Cooper and Lavine [7] have studied the effect of
different grinding parameters on a cylindrical workpiece
using numerically assembled grinding wheel information.
Warnecke and Zitt [8] modelled the macro and micro
geometry of the grinding wheel using synthetic 3D-mod-
eling wherein the structure of grinding wheel was analyzed
using scanning electron microscopy (SEM). They also
studied the kinematic interaction between grinding wheel
and workpiece for different grinding processes such as
surface grinding, cylindrical grinding and internal cylin-
drical traverse and plunge grinding. Koshy et al. [9] in their
research paper concluded that the percentage of projected
area due to protruding abrasives is independent of the
abrasive grit size. Chen and Rowe [10, 11] generated
grinding wheel surface by single point diamond dressing
and studied the effect of dressing condition on the grinding
wheel and the generated workpiece after helical grinding.
The result was validated using the experimental result
available in the literature. Gong et al. [12] applied virtual
reality technology to simulate the grinding wheel and
studied the effect of cutting depth, axial feed and wheel
velocity on the surface roughness.
The different grinding parameters like grit density,
downfeed, wheel velocity, work speed etc. have significant
effect on the surface topography generated [1–13]. The
grinding procedures viz. plunge grinding, cross-feed
grinding, helical grinding and touch dressing also play an
important role in deciding the final surface finish of the
workpiece. Ghosh and Chattopadhyay [14, 15] have stud-
ied the effect of touch dressing on the surface roughness
using single layer brazed cBN wheels and they concluded
that a substantial improvement of transverse surface
roughness could be achieved on touch dressing. Vickerstaff
[16] has studied the effect of cross-feed on wheel wear and
surface roughness during surface grinding of hardened and
tempered Ni-Cr-Mo alloy steel by vitrified bonded alumina
grinding wheel. Iwai et al. [17] have studied the effect of
helical grinding on the surface finish and have inferred that
the better surface finish is achieved due to interference of
the trajectories of the multiple grits. Zhang and Uematsu
[18] have also studied the effect of helical grinding on
surface finish and found out that the surface roughness
value in case of helical grinding nearly becomes one-sev-
enth of the value in case of plunge grinding.
The work carried out by Chakrabarti and Paul [1]
involves the prediction of surface roughness for different
grinding parameters under plunge surface grinding. They
did not carry out any analysis for other grinding procedures
viz. traverse or cross-feed grinding, and helical grinding
with touch dressing. The aim of the present work is to
develop and implement numerical models for the predic-
tion of surface roughness for different surface grinding
operations namely plunge grinding, traverse or cross-feed
grinding and helical grinding with touch dressing. The
effects of different grinding parameters (grit density and
grit size) on the surface finish of the ground workpiece are
also studied. Further, the trend of the predicted results is
compared with experimental data available in the literature.
2 Simulation methodology
2.1 Generation of the wheel topography
The interaction between the abrasive grits and the work-
piece depends on the wheel topography and the grinding
parameters, thus affecting the surface roughness. The grits
distributed on the wheel surface differs in terms of their
shape, size, orientation and grit distribution density over
the wheel surface, which results in random variations in the
protrusion heights from the wheel surface. Chakrabarti and
Paul [1] have discussed different methods adopted by
various researchers to model the grinding wheel topogra-
phy. In grinding, it has been observed that the average rake
angle during chip formation can be taken as -60� [13].
Therefore, in this paper the grits have been modelled as
square pyramidal objects having an included angle of 120�.
The grit heights (h) were made to vary and the base
diameter of grits (dg) were changed in order to keep the
included angle constant. The grits have been placed ran-
domly on the periphery of grinding wheel of diameter ds
200 Prod. Eng. Res. Devel. (2012) 6:199–204
123
with a given grit density c. Figure 1 depicts the modelled
shape of an abrasive grit. The grit heights have been
assumed to vary by 5% and follow the relationship as
reported by Chakrabarti and Paul [1].
dg
2ffiffiffi
3p � 0:05dg \h \
dg
2ffiffiffi
3p þ 0:05dg ð1Þ
where, dg is the average diameter of the grits.
2.2 Simulating the grit interaction with the workpiece
Simulation of grit interaction with the workpiece involves
the simulation of the trajectory of a particular grit for a
period of time and to remove whatever workpiece material
is interfering with the trajectory of the grit. A detailed
kinematic analysis of the grit interaction with the work-
piece can be found in standard literature [13]. For com-
pleteness of the paper, a brief review is provided. First, an
x–z coordinate system is set with its origin O0 fixed on the
workpiece and coinciding with the grit G at the lowest
point, as shown in Fig. 2. Then, the trajectory of grit G,
which is a trochoid, can be described as:
x ¼ ds
2sin h� dsvw
2vgh ð2Þ
z ¼ ds
2ð1� cos hÞ ð3Þ
where, x and z are the coordinates of grit G after it has
rotated by angle h, vw is the velocity of the workpiece and
ds is the nominal diameter of the grinding wheel. To reduce
complexity during the simulation, the rubbing and
ploughing effects during grinding have been neglected
along with wear and tear of the grit during grinding.
The whole simulation process can be assumed to be
comprised of the two processes discussed above. The first
step is simulating the wheel topography and the second is
simulating the grit interaction with the workpiece. The
simulation is run in such a way that the trajectories of all
the grits are calculated and the interfering material is
removed in each run of the iteration. The simulation pro-
cess is carried out by discretizing workpiece surface into
very small rectangular areas and the entire surface infor-
mation (i.e. the depth of the workpiece at each of these
rectangular locations) is stored in a matrix whose dimen-
sions are equal to the number of rectangles along the length
and width of the workpiece. The surface roughness of the
simulated ground surface is calculated using Ra parameter.
3 Simulation results and discussion
The grinding process has been simulated by taking the
following parameters, viz. vg, vw, c, dg and a into consid-
eration. The effect of different surface grinding operations,
viz. plunge grinding, traverse or cross-feed grinding and
helical grinding with touch dressing, on the surface
roughness of the ground workpiece has been studied.
3.1 Plunge grinding
In plunge surface grinding, typically the width of the
grinding wheel is more than the width of the workpiece and
downfeed is given per stroke. The workpiece reciprocates
under the grinding wheel and the entire surface of the
workpiece is ground by the peripheral surface of the
grinding wheel. The surface roughness changes with
change in the input parameters like wheel speed, workpiece
speed, grit density etc. Similar work has been done by
Chakrabarti and Paul [1] and therefore, only the grit den-
sity and the grit size have been varied to study their effect
on surface roughness.Fig. 1 Modelled shape of an abrasive grit
Fig. 2 Trajectory of a single grain in grinding process
Prod. Eng. Res. Devel. (2012) 6:199–204 201
123
3.1.1 Variation in grit density (c)
Material removal in grinding can be thought of as collec-
tion of repetitive unit events. In grinding the unit event is
the generation of a grinding chip by the cutting action of an
abrasive grit and it can be quantified by the average grit
depth of cut (ha). Increase in grit density leads to reduction
in chip volume which results in the average grit depth of
cut (ha) becoming smaller. However, grit density cannot be
increased indefinitely for a given grit size. Moreover, high
grit density leads to less chip accommodation space
between grits, increasing probability of wheel loading.
Figure 3 depicts the effect of grit density on ground surface
finish. Expectedly, the increase in grit density provided
finer average grit depth of cut, i.e. finer chip volume
leading to improvement in the surface finish. A two fold
increase in grit density from 4 to 8 grits/mm2 provided
improvement in surface finish (Ra) from 0.46 to 0.30 lm
under plunge surface grinding.
Ghosh and Chattopadhyay [14] have studied the effect of
grit density on surface roughness in grinding using single
layer cBN wheels and have observed that choice of densely
packed wheels over regular grit density provided improve-
ment in surface finish. The effect of grit density has also been
observed by Heo et al. [19]. They observed that use of finer
grits (Mesh#100 to #500), i.e. higher maximum possible grit
density, yielded reduction in surface roughness (Ra) from
0.40 to 0.15 lm. Thus, it may be inferred that the proposed
model could capture the generation of surface roughness in
grinding and the effect of grit density in particular.
3.1.2 Variation in grit size
Increase in the grit size leads to an increase in its effective
height and, the grit density typically decreases with
increase in the grit size. Thus, with an increase in the grit
size, the unit event in grinding becomes larger. Figure 4
depicts the effect of grit size on ground surface finish.
Surface roughness (Ra) increases by two fold from 0.20 to
0.40 lm when the diameter of grit is increased from 150 to
300 lm. The other grinding parameters were kept same
during simulation and they were taken as: vg = 150 m/s,
vw = 150 mm/s, c = 6 grits/mm2, and a = 25 lm. Thus it
may be deduced that the proposed model could capture the
effect of grit size on surface roughness correctly.
3.2 Simulation results for touch dressing
Grinding wheels possess an inherent weakness of having
unequal distance of the grit tips from the wheel substrate
surface [14]. Certain percentage of the grits always remains
over-protruded which do not allow the underlying ones to
participate during grinding. It results into less overlapping
cuts of grit leading to transverse surface roughness, sub-
stantially higher than the acceptable value [15]. Further, the
single layer cBN wheels tend to produce rougher surface
due to high sharpness of the abrasive grits [14, 15]. Such
high workpiece surface roughness associated with the use
of single-layer cBN wheel needs to be reduced and this
problem can be appropriately solved by controlled dressing
of the overlying cBN grits with a suitable diamond tool.
The process is popularly known as touch-dressing [14, 15].
Touch dressing allows participation of large number of
grits, which remain inactive before the dressing. The touch-
dressed wheel not only reduces the roughness of the ground
surface markedly but also maintains roughness value
almost constant over a long span of grinding. Figures 5 and
6 shows the variation of the surface roughness with the
level of the dressing of the wheel. The grits used are square
pyramidal and dressing is done in steps. X-axis (abscissa)
Fig. 3 Variation in surface roughness with grit density for plunge
grinding
Fig. 4 Variation in surface roughness with grit size for plunge
grinding
202 Prod. Eng. Res. Devel. (2012) 6:199–204
123
shows the level of dressing, which is basically the amount
of material removed or dressed from the top of the grits,
which is a percentage of the diameter of the grit and is
varied from 0 to 7% for simulation. 0% implies that no
touch dressing has been done. The base diameter of the grit
is 250 lm and thus the dressing has been done up to 17.5
micron. The surface roughness was calculated for two
different grit density values viz. 6 and 16 grits/mm2. Ghosh
and Chattopadhyay [14, 15] have studied the effect of
touch-dressing on surface roughness in grinding using
single layer cBN wheels with 252 lm abrasive grits. They
have studied the effect of touch dressing on three different
wheels and have observed that after each step of touch
dressing of the brazed wheels, the surface roughness value
decreases. They have varied the cumulative dressing depth
from 0 to 22 lm. Initially, up to 13 lm, the rate of
reduction in surface roughness is high and gradually the
rate diminishes. With further dressing, there is negligible
effect on the surface roughness because the rate of reduc-
tion in surface roughness is very low in the final stages of
the dressing as most of the grits participate in grinding after
critical depth of dressing. Similar reduction in surface
roughness has been captured by the proposed model as
shown in Figs. 5 and 6. Also, it can be observed that the
surface roughness value for higher grit density is low
which is apparent and has been discussed above.
3.3 Touch dressing with cross-feed grinding
In case of plunge grinding no cross feed is provided to the
table, while in case of cross-feed grinding a cross feed is
provided to the table at the end of each stroke. Cross-feed
is common when the workpiece width is more than the
width of the grinding wheel. Figures 5 and 6 show the
variation of ground surface roughness in the case of cross-
feed grinding with the level of touch dressing done and are
for two different values of grit density viz. 6 and 16 grits/
mm2 respectively.
The other grinding parameters were kept unchanged
during simulation and they were vg = 150 m/s, vw = 150
mm/s, a = 25 lm. Cross feed of 1 mm/stroke was pro-
vided to the grinding wheel at the end of each stroke. It can
be inferred from Figs. 5 and 6 that for the same set of input
parameters, average surface roughness in case of cross-feed
grinding is less as compared to plunge grinding.
Vickerstaff [16] has studied the effect of cross-feed
grinding on surface roughness of the workpiece and has
observed that cross-feed grinding leads to reduction in the
average surface roughness values. Similar effects have been
demonstrated by the proposed numerical simulation. In case
of traverse or cross-feed grinding also, the effectiveness of
touch dressing has been effectively captured by the pro-
posed numerical model as can be seen in Figs. 5 and 6.
3.4 Helical grinding
In case of helical grinding, the table is provided with a
constant transverse speed, unlike in cross-feed grinding in
which the cross-feed is provided at the end of each stroke.
The table transverse speed used for simulation was 15 mm/
s and the other grinding parameters were kept unchanged.
Figure 7 shows the variation of ground surface roughness
with grit density in case of helical grinding and also pre-
sents a comparative picture between helical grinding and
plunge grinding for the same set of grinding parameters. It
can be observed that for the same set of grinding param-
eters surface roughness is less in case of helical grinding as
compared to the surface roughness in plunge grinding.
Zhang and Uematsu [18] have claimed reduction in surface
roughness upon helical grinding by a factor of seven.Fig. 5 Variation in surface roughness with touch dressing for plunge
and cross-feed grinding for low grit density (6 grits/mm2)
Fig. 6 Variation in surface roughness with touch dressing for plunge
and cross-feed grinding for high grit density (16 grits/mm2)
Prod. Eng. Res. Devel. (2012) 6:199–204 203
123
Though, in the present work, the improvement in surface
finish on helical grinding seems to be by a factor of two.
Iwai et al. [17] have observed improvement in surface
finish upon helical grinding due to the interference of the
trajectories of the multiple grits, which has been effectively
modelled in the present work as seen in Fig. 7.
Figure 5 indicates that plunge surface grinding without
touch dressing with a grit density of 6 grits/mm2, provided
a surface roughness (Ra) of around 0.33 lm, which reduced
to 0.20 lm on traverse or cross-feed grinding. Helical
grinding produced almost similar surface roughness (Ra) of
around 0.21 lm. Helical grinding does not require incre-
mental cross-feed after each stroke, which is the charac-
teristics of cross-feed grinding and thus helical grinding
would require much less cycle time enhancing the pro-
ductivity simultaneously providing improved surface finish
as compared to plunge surface grinding.
Further, Fig. 5 indicates that touch-dressing brings down
the surface roughness in case of traverse or cross-feed
grinding to around 0.17 lm, which is not much improved
from surface roughness of around 0.21 lm (refer Fig. 7)
achieved under helical grinding. Touch-dressing introduces
another operation prior to employing the single-layer cBN
wheels for grinding and in the process further increases the
cycle time. Over and above, touch dressing may lead to
increase in grinding forces [14, 15].
4 Conclusions
A model for generating the surface topography based on
the cutting conditions, wheel topography and initial
workpiece geometry has been developed. The model
developed has been implemented to study the effect of
different grinding parameters and operations, viz. plunge
surface grinding, traverse or cross-feed grinding with touch
dressing and helical grinding, on ground surface topogra-
phy. The proposed methodology captures the parametric
effect on surface roughness successfully both in degree and
nature as has been verified against experimental results
from previously published literature.
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