a planar end-fire circularly polarized · a planar end-fire circularly polarized ... c
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1
A Planar End-fire Circularly Polarized
Complementary Antenna with Beam in Parallel
with Its Plane
Wen-Hai Zhang, Wen-Jun Lu and Kam-Weng Tam
Abstract—Operation principle and design approach of a novel
planar, end-fire circularly polarized (CP) complementary
antenna is proposed. A vertically polarized printed magnetic
dipole and a horizontally polarized printed dipole are combined
on the same substrate, and a planar CP antenna with end-fire
beam in parallel with its plane is thus designed. Prototype
antennas centered at 5.80 GHz are then fabricated and measured
to validate the operation principle and the design approach. The
experimental prototype reported that the impedance bandwidth
(20log|S11| < -10 dB) is about 1.90%, from 5.75 to 5.86 GHz and
the 3-dB axial ratio (AR) bandwidth is about 14.48%, from 5.19 to
6.00 GHz. Therefore, the proposed design is applicable as a
low-profile, hand-held reader antenna in radio frequency
identification (RFID) systems.
Index Terms—Circularly polarized, end-fire, planar antenna,
complementary antenna, hand-held RFID reader.
I. INTRODUCTION
he circularly polarized (CP) antennas have been intensively
studied since 1940’s [1, 2]. The design approaches to
generate CP radiation can be basically categorized into five
distinctive types, according to their operation principles. The
first type is to use the superposition of complementary dipoles
[1-5], such as the combination of dipole/monopole and loop [1],
slotted cylindrical dipoles [3], printed strips and slots [4].
Generally, both broadside [1-4] and end-fire [5] CP radiation
beams can be realized by using these techniques. The second
one is to use the superposition of identically orthogonal dipoles.
The use of two orthogonally crossed dipole elements fed with
equal magnitude and 90° phase difference is a straightforward
way to generate broadside, CP radiations [6-9]. The third way
to generate CP radiation is to introduce the turnstile structures,
including the helices [10, 11] and the spirals [12-15]. In this
case, end-fire CP radiation beams can be obtained by using
relatively electrically large turnstile structures [10-15]. With
reference to planar spirals or helices configuration, the end-fire
beam is perpendicular to the plane of the antenna [13-15]. The
forth type is to excite two degenerate modes within a single
radiator, e.g., a patch [16, 17] or a dielectric resonator [18, 19],
by employing 90° hybrid couplers/dividers [16] or using
perturbations [17-19]. As similar to the previously described
three distinctive types of CP antenna design methods, the
Manuscript received June 24, 2015. This work is supported in part by FDCT
project 015/2013/A1, One-time Special Fund for PhD Student Support of
University of Macau and National Natural Science Foundation of China under grant no. 61471204.
W. H. Zhang and K. W. Tam are with the Department of Electrical and
Computer Engineering, Faculty of Science and Technology, University of Macau, Macao SAR, China (email:[email protected]; [email protected]).
W. J. Lu is with the Jiangsu Key Laboratory of Wireless Communications,
Nanjing University of Posts and Telecommunications, Nanjing 21003, China (email: [email protected]).
resulted radiation patterns of this method are also broadside.
The final one utilizes the traveling-wave or periodical
structures, such as the waveguide-fed horn antennas [20, 21],
the substrate integrated waveguide antennas [22-25], and the
metamaterial-based leaky wave antennas [26, 27]. Most of
them are electrically large and exhibit broadside CP beams. By
comparing the five types of CP antenna design approaches
according to their basic operation mechanisms and radiation
behaviors, it is found that to design a planar CP antenna with an
end-fire beam in parallel with its plane while keeping a planar
antenna structure, is a challenging task. Although an end-fire
CP beam in parallel with the major plane of the antenna can be
realized [25, 27], nonplanar configurations will be introduced
due to the inherent feed structure [5] or introducing pairs of
additional orthogonal elements [25, 27] .
On the other hand, due to broadside radiation characteristic,
the antennas are often assembled perpendicularly to the reader
to achieve front-directional radiation for handheld RFID
readers, which significantly increases the whole profile of
handheld reader [28, 29]. Recently, a new approach to design
planar, end-fire CP antenna having a beam in parallel with its
plane is studied [30]. Different from combining a pair of
orthogonally magnetic dipole together [30], a new planar
complementary antenna with a simpler structure is proposed in
this paper. The proposed antenna is combined with an aperture
and a printed dipole. To the best of our knowledge, this is the
first time using the complementary dipoles to achieve a planar
end-fire CP antenna with its beam in parallel with the plane.
This paper is organized as follows: In Section II, an equivalent
sources model is presented to deduce the dipole-aperture
combined antenna configuration, and the design guideline is
addressed as well. In Section III, the proposed antenna is
parametrically studied and optimal parameters are obtained. In
Section IV, prototypes are fabricated, measured and compared
to validate the design approach.
II. THEORY AND DESIGN GUIDELINE
Conceptual configuration consisting of a pair of paralleled
magnetic and electric dipole is shown in Fig.1 (a), which aligns
with the y-axis. The aperture element is equivalent to a virtual,
time-harmonic magnetic dipole. The electric-field at an
arbitrary observation point P in the far field can be obtained,
according to [31].
ˆ ˆcos cos sin0 04
jkrapertureI l
E E E j er
(1)
Where I0 is the amplitude, l is the length of dipole, η = 0 0
is the wave impedance, μ0 and ε0 are the permittivity and the
permeability of free space, respectively. On the other hand, the far field pattern of y-oriented electric
dipole is [31, 32]
ˆ ˆcos sin cos0 04
jkrdipoleI l
E E E j er
(2)
When the aperture and printed electric dipole are excited
with equal amplitude with a distance of d about 3λ/8 (λ is the
guided-wave wavelength, k = 2π/λ is the wave number). Here δ0
T
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indicates the temporal phase that caused by the current flowing
from the aperture to the printed dipole, and it equals to kd =
3π/4. The total far field of the complementary configuration
will be
( sin cos )
ˆ cos cos sin ( , )
ˆ cos sin cos ( , )
0
0 0
4
j kd
total aperture dipole
jkr
E E e E
fI lj e
r f
(3)
Where
( , ) cos sin cos sin sin cos3 3 3 3
4 4 4 4
f j (4)
When ,90 0 , the E-field along the +x-axis is
ˆ ˆ0 04
jkr
x
I lE j j e
r (5)
From (5) it is seen perfect circularly polarized radiation
characteristic can be obtained at the +x-direction, i.e., the
end-fire direction of the planar, aperture-dipole combined
antenna.
To more clearly reveal the mechanism for CP generation of
the proposed antenna, radiation patterns of a single microstrip
magnetic dipole at the resonant frequency is simulated in Fig. 2.
It is observed that the antenna produces an “8”-shaped radiation
pattern in the azimuth plane (xy-plane, H-plane), while an
“O”-shaped radiation pattern in the elevation plane (xz-plane,
E-plane). The result proves that the antenna resonates as a
vertically polarized (i.e., z-polarized) magnetic dipole
operating at its dominant, one-half wavelength mode. It
exhibits radiation maxima at the end-fire, +x-direction [33].
For a y-polarized electric dipole operating at its dominant mode,
it should have a complementary radiation pattern and
orthogonal polarization with the magnetic dipole. Therefore, if
90-degree phase difference is provided, end-fire, CP
characteristic can be achieved while a planar structure is
maintained.
x
Yz
Magnetic dipole Electric dipole E-field
P
r
Aperture
d
o
X
Y
Z
φ
θ
Dipole
(a)
x
Y
Feed point
Top layer Bottom layer
λ/4
Substrate
Shorting wall
Aper
ture D
ipole
(b)
Shorting
wall
Coaxial cable
xy
z
Top layer
Bottom layer
Substrate
(c)
Fig. 1. Planar end-fire complementary CP antenna, (a) equivalent sources
model, (b) conceptual design, and (c) sectional view of the proposed antenna.
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-30
-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
XY
-40
-30
-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
XZ
(a) (b)
Fig. 2. Simulated radiation patterns at 5.8 GHz. (a) xy-plane; (b) xz-plane.
Based on the theoretical and numerical analysis, the basic
structure of the planar CP complementary antenna can be
deduced: In Fig. 1(b) and (c), three edges of magnetic
microstrip dipole are shorted with one left opened [33] to form
an aperture. The aperture serves as a virtual magnetic
microstrip dipole which operates at one-half wavelength mode
with width of one-quarter wavelength [34]. A coaxial cable
probe is used to excite the magnetic dipole and is located near
its E-current’s antinode [30]. A pair of 3λ/8, broadside coupled
stripline [35] is placed between the aperture and printed electric
dipole to introduce a proper phase difference. In this way, a
planar, end-fire CP beam in parallel with the substrate’s plane
will be resulted in.
III. ANTENNA GEOMETRY AND PARAMETRIC STUDY
The geometry of the proposed antenna is shown in Fig. 3.
The proposed antenna with a total size of 38 mm×33.5 mm is
designed on substrate with relative permittivity of εr=2.65, tan δ
= 0.001, thickness h=2.0 mm.
The direction of CP of the proposed antenna can be
determined by the probe current’s path/loop [30]. Suppose the
probe is fed to the top layer of the magnetic dipole, and the
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current flows from the probe, then to the top layer of the
broadside coupled stripline, the top arm of the printed dipole.
To maintain the continuity of the current path/loop, it is
supposed the displacement current flows to the +x-direction,
and then turns back to the bottom arm printed dipole, the
bottom layer of the broadside coupled stripline, and finally
flows into the bottom layer of the magnetic dipole. If such a
virtual probe current's path obeys a right handed helix direction
with thumb point at +z-direction, a right handed circularly
polarized (RHCP) antenna is obtained. Otherwise, a left handed
circularly polarized (LHCP) one is resulted instead. In this
paper, a RHCP antenna is designed and investigated.
In order to increase the bandwidth, a printed fatter dipole is
adopted [36]. The initial parameters are determined according
to the design guideline and the empirical results in [30, 33] and
tabulated in Table I. In order to simultaneously achieve the
optimized impedance bandwidth and axial ratio characteristics,
a parametric studies are carried out to determine the optimal
parameters. The antenna is modelled by using Zeland’s IE3D
v12.0 with method-of-moment codes and finite substrate is
considered in simulations. When one parameter is studied, the
others are kept unchanged.
L
W1
L1
L2
W2
g
d
α
D
g1
W
X
Y
Z
Feed point
Metallic via
Top layer
Bottom layer
Fig. 3. Geometry of the proposed antenna.
TABLE I
ANTENNA PARAMETERS
Parameters Initial/Optimal Parameters Initial/Optimal
L(mm) 36.0/38.0 g(mm) 0.6/0.4
W(mm) 33.5/33.5 L1(mm) 11.9/13.5
W1(mm) 7.9/7.9 W2(mm) 7.9/16.0
D(mm) 0.6/0.6 L2(mm) 4.0/6.0
d(mm) 2.0/2.0 α 80°/84°
g1(mm) 0.3/0.3
5.2 5.4 5.6 5.8 6.0 6.2
-40
-35
-30
-25
-20
-15
-10
-5
0
|S11|(
dB
)
Frequency(GHz)
α=80° α=82° α=84° α=86°
Fig. 4. Effect of the angle of magnetic dipole α.
The effect of angle α on the antenna performance is studied
firstly in Fig. 4. It is observed that it has a significant effect on
impedance characteristic, the center frequency shifts up for a
larger α. Fig. 5 shows the effect of the distance of feed point.
As we can see better impedance characteristic can be achieved
when d equals to 2 mm. However, both of them have slight
effect on 3-dB AR bandwidth.
Fig. 6 shows the effect of length of broadside coupled
stripline on the performance of the proposed antenna. It is
observed that with the increasing of L1, it improves 3-dB
bandwidth significantly and the minimized AR shifts up
gradually. The effect of the width and the length of the printed
dipole are also studied. In Fig. 7, with the increasing of L2, the
minimized AR shifts down and better 3-dB AR bandwidth is
achieved when L2 equals to 6 mm. However, If L1 and L2 decrease continuously, AR will become worse. Fig. 8 shows
that when the length increases, 3-dB AR bandwidth becomes
much wider and minimized AR shifts down gradually.
In order to show mechanism for CP generation, simulated
surface current distributions at 5.8 GHz are investigated and
shown in Fig. 9. It is seen both of the magnetic and electric
dipoles are operating at their dominant mode, as theoretically
predicted in the previous section. When a 90-degree phase
difference properly introduced, end-fire CP radiation
characteristic can be achieved.
5.0 5.2 5.4 5.6 5.8 6.0
-20
-15
-10
-5
0
|S11|(
dB
)
Frequency(GHz)
d=1 mm
d= 1.5 mm
d= 2 mm
d= 2.5 mm
Fig. 5. Effect of the distance of feed point d.
5.0 5.2 5.4 5.6 5.8 6.0
0
1
2
3
4
5
6
Axia
l R
atio
(dB
)
Frequency(GHz)
L1=11.5 mm
L1=13.5 mm
L1=15.5 mm
Fig. 6. Effect of the length of broadside coupled stripline L1.
5.0 5.2 5.4 5.6 5.8 6.0
0
1
2
3
4
5
6
7
8
Axia
l R
atio
(dB
)
Frequency(GHz)
L2=4 mm
L2=6 mm
L2=8 mm
Fig. 7. Effect of the width of printed electric dipole L2.
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5.0 5.2 5.4 5.6 5.8 6.0
0
1
2
3
4
5
6
7
8
Axia
l R
atio
(dB
)
Frequency(GHz)
W2=14 mm
W2=16 mm
W2=18 mm
Fig. 8. Effect of the length of printed electric dipole W2.
Fig. 9. Surface current distribution at 5.8 GHz.
IV. SIMULATED AND EXPERIMENTAL RESULTS
Based on the parametric studies, prototypes of the proposed
antenna, shown in Fig. 10, are fabricated and measured to
verify the design approach. The reflection coefficient is
measured by using an Agilent N5230A vector network analyzer.
The radiation patterns, gain, efficiency and AR are measured in
a Satimo’s Starlab near-field antenna measurement system.
Fig. 11 shows the measured and simulated reflection
coefficient of the proposed antenna. The measured -10-dB
reflection coefficient bandwidth is from 5.75 to 5.86 GHz,
about 1.90% in fractional, while the simulated one is from 5.70
to 5.91 GHz, about 3.62% in fractional. The mismatch is caused
by the fabrication errors and measurement errors caused by the
non-ideal probe and the SMA connector. Fig. 12 shows the
measured and simulated 3-dB AR bandwidth of the proposed
antenna. The measured AR bandwidth is from 5.18 to 6.00 GHz,
which is larger than 14.48% in fractional, while the simulated
one is from 5.18 to 5.98 GHz, which is about 14.34%. Both of
them are wider than the corresponding impedance bandwidth.
The measured and simulated gain at +x-direction and efficiency
of the proposed antenna are illustrated in Fig. 13 and Fig. 14,
respectively. It is observed that the proposed antenna exhibits
stable gain at +x-direction of about 2.3 dBic within its
impedance bandwidth. The measured gain is in good agreement
with the simulated one in the low frequency regime and some
discrepancies can be observed in the high frequency band, i.e.,
above 5.80 GHz. The average measured efficiency is about
78%, slightly lower than the simulated one. The measured and
simulated results, including the reflection coefficient, AR, gain
and efficiency are in good agreement with each other.
The measured and simulated radiation patterns in xz-plane
and xy-plane at 5.65 GHz (the minimized AR) and 5.80 GHz
(the center frequency of impedance band) are plotted in the Fig.
15 and Fig. 16, respectively. It can be observed that the
simulated results are consistent with the measured ones. The
proposed antenna has a +x-direction, end-fire CP radiation
pattern, as predicted in the above. In both principal planes,
symmetrical radiation patterns and wide angle AR
characteristics are obtained. The measured half-power beam
widths of the proposed antenna is 155° and 75° in xz-plane and
xy-plane, respectively, while the corresponding 3-dB AR beam
width is 110° and 80° at 5.80 GHz, which is desirable for
wide-coverage RFID applications [37]. The measured and
simulated half-power and 3-dB AR beam widths of both
frequencies are summarized in Table II.
(a) (b)
Fig. 10. Top and bottom-view photographs of the prototype. (a) Top view; (b)
bottom view.
5.0 5.2 5.4 5.6 5.8 6.0
-20
-15
-10
-5
0
|S11|(
dB
)
Frequency(GHz)
Simulated
Measured
Fig. 11. Measured and simulated reflection coefficient of the proposed antenna.
5.0 5.2 5.4 5.6 5.8 6.0
1
2
3
4
5
Axia
l R
atio
(dB
)
Frequency(GHz)
Simulated
Measured
Fig. 12. Measured and simulated axial ratio at +x-direction (θ=90°, φ=0°) of
the proposed antenna.
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5.0 5.2 5.4 5.6 5.8 6.0
-8
-6
-4
-2
0
2
4
Gai
n(d
Bic
)
Frequency(GHz)
Simulated
Measured
Fig. 13. Measured and simulated gain of the proposed antenna.
5.0 5.2 5.4 5.6 5.8 6.0
0
20
40
60
80
100
Eff
icie
ncy
(%)
Frequency(GHz)
Simulated
Measured
Fig. 14. Measured and simulated efficiency of the proposed antenna.
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-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
LHCP,simulated RHCP,simulated
LHCP,measured RHCP,measured
XZ
(a)
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-30
-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
LHCP,simulated RHCP,simulated
LHCP,measured RHCP,measured
X
Y
(b)
Fig. 15. Measured and simulated radiation patterns at 5.65 GHz. (a) xz-plane;
(b) xy-plane.
-40
-30
-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
LHCP,simulated RHCP,simulated
LHCP,measured RHCP,measured
XZ
(a)
-40
-30
-20
-10
0
0
30
60
90
120
150
180
210
240
270
300
330
-40
-30
-20
-10
0
LHCP,simulated RHCP,simulated
LHCP,measured RHCP,measured
X
Y
(b)
Fig. 16. Measured and simulated radiation patterns at 5.80 GHz. (a) xz-plane;
(b) xy-plane.
A comprehensive comparison with other typical CP antennas
is also presented. The comparisons in terms of operation
principles, beam directions, geometry and 3-dB AR bandwidth
are tabulated in Table III. It is seen that most planar antennas
can only achieve CP beam which is perpendicular to the plane
except [30], and the new complementary antenna has an
end-fire, CP beam in parallel with its plane. Furthermore, the
CP operation bandwidth is increased to 14.48% compared to its
planar counterpart using orthogonally combined magnetic
dipoles [30]. This is possibly caused by the mutual cancellation
of reactance characteristics of the complementary dipoles [38].
TABLE II
BEAM WIDTHS OF THE ANTENNA
Frequency
Half-power beam width
(Simulated/Measured)
3-dB AR beam width
(Simulated/Measured)
xz-plane xy-plane xz-plane xy-plane 5.65 GHz 177°/156° 93°/75° 103°/106° 74°/87°
5.80 GHz 165°/155° 68°/75° 104°/110° 94°/80°
TABLE III FIGURE OF MERIT COMPARISONS
V. CONCLUSION
In this work, a novel planar dipole-aperture combined
antenna has been proposed, fabricated and tested. An end-fire
CP beam in parallel with its substrate plane is obtained. Our
study shows that the proposed antenna can achieve an
impedance bandwidth of 1.90% and a 3-dB AR bandwidth of
Reference Operation principle Beam Direction Beam relative to the substrate’s
plane Geometry 3dB-AR Bandwidth
[3] Complementary dipoles Broadside Perpendicular Non-planar Not available
[5] Complementary dipoles End-fire In parallel with Non-planar 12.50%
[10] Turnstile structures End-fire Perpendicular Non-planar Not available
[14] Turnstile structures End-fire Perpendicular Planar 6.70%
[21] Orthogonal modes within a radiator Broadside Perpendicular Non-planar Not available [22] Orthogonal modes within a radiator Broadside Perpendicular Non-planar 17.39%
[26] Orthogonal modes within a radiator End-fire Perpendicular Planar Low band:<0.56%
Upper band:<0.51% [27] Orthogonal dipoles End-fire In parallel with Non-planar 33.00% [30] Orthogonal dipoles End-fire In parallel with Planar 9.24%
[39] Orthogonal dipoles Broadside Perpendicular Non-planar 39.00%
[40] Orthogonal modes within a radiator Broadside Perpendicular Planar 0.65%(2dB-AR
bandwidth)
This work Complementary dipoles End-fire In parallel with Planar 14.48%
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14.48%. The measured results exhibit good agreement with the
predicted ones. The principle of end-fire CP beam realization
has been demonstrated and experimentally validated. Therefore,
the proposed antenna is advantageous for low-profile, handheld
RFID reader applications .
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