4.2 mm, H1 ¼ 1.1 mm, H2 ¼ H3 ¼ 1.36 mm, H4 ¼ 1.36 mm,
L5 ¼ 6 mm, L6 ¼ 6.5 mm, L7 ¼ L11 ¼7.4 mm, L8 ¼ L10 ¼ 10
mm, L9 ¼ 10.6 mm, and L12 ¼ 12.5 mm. The experimental cir-
cuit is fabricated on a substrate with relative dielectric constant
of 2.65 and the thickness of 1 mm by standard PCB process.
The manufactured prototype of the proposed power divider is
shown in Figure 4. The size of the proposed power divider is
about 32 � 45 mm2, which does not include the size of 50-X
feeding line and the length of the transition between the SIW
and the microstrip. The measured insertion losses and the input
return loss for the two-way equal SIW power divider can be
observed in Figure 5, where they are compared with full-wave
simulated results provided by the commercial software Ansoft
HFSS. According to the measurements, the transmission
response for the proposed power divider falls to at 3.48 GHz
and at 5.2 GHz and the power divider has an insertion loss level
of 3.7 6 0.5 dB, which includes 3.01-dB inherent insertion loss
of two-way equal power divider. With regard to the input return
loss, the power divider has a minimum value of 10.6 dB
throughout the pass band. The out-of-band rejection is larger
than 40 dB at 2.35 GHz and at 6.12 GHz, respectively.
4. CONCLUSION
In this article, a compact two-way equal SIW power divider
with sharp out-of-band rejection has been presented. Experimen-
tal power divider has been built and measured. Good agreements
are observed between the measured results and the simulations.
This power divider is very suitable for application in low cost
and compact size microwave and millimeter-wave planar circuits
by traditional PCB technology.
ACKNOWLEDGMENT
This present work was supported by the Fundamental Research
Funds for the Central University (No. CDJRC11160001).
REFERENCES
1. J.-Y. Shao, S.-C. Huang, and Y.-H. Pang, Wilkinson power divider
incorporating quasi-elliptic filters for improved out-of-band rejec-
tion, Electron Lett 47 (2011), 1288–1289.
2. J. Wang, J. Ni, and Y.-X. Guo, Miniaturized microstrip Wilkinson
power divider with harmonic suppression, IEEE Microwave Wirel
Compon Lett 19 (2009), 440–442.
3. T. Skaik, M. Lancaster, and F. Huang, Coupled-resonator 3-dB
power divider, In: Proceedings of IET seminar on passive RF and
microwave components, Birmingham, UK, 2010, 21–22.
4. T. Skaik, M. Lancaster, and F. Huang, Synthesis of multiple output
coupled resonator circuits using coupling matrix optimization, IET
Microwave Antennas Propag 5 (2011), 1081–1088.
5. X. Zhang, J. Xu, and Z. Yu, C-band half mode substrate integrated
waveguide (HMSIW) filter, Microwave Opt Tech Lett 50 (2008),
275–277.
6. Y.Q. Wang, W. Hong, Y.D. Dong, B. Liu, H.J. Tang, J.X. Chen, and
K. Wu, Half mode substrate integrated waveguide (HMSIW) band-
pass filter, IEEE Microwave Wirel Compon Lett 17 (2007), 265–267.
VC 2013 Wiley Periodicals, Inc.
BROADBAND BANDPASS FILTER USING
PARALLEL-COUPLED MICROSTRIP LINE
AND COUPLED OPEN STUB RESONATOR
Jayaseelan Marimuthu, Amin Abbosh, and Bassem Henin
School of ITEE, The University of Queensland, St Lucia QLD 4072,
Australia; Corresponding author: j.marimuthu@uq.edu.au
Received 31 October 2012
ABSTRACT: A novel broadband bandpass filter with multiple resonant
modes based on parallel-coupled microstrip line is proposed. The
required cutoff frequency and out-of-band performance are achieved by
placing L-shaped capacitive cross-coupling open stubs at the middle
resonator with appropriate dimensions. A compact broadband bandpass
filter of dimensions 18 � 29 mm2 is fabricated and tested for
performance confirmation. The proposed filter demonstrates a wide
bandwidth (from 3 to 7 GHz), as well as excellent out-of-band
performance with more than 25-dB rejection up to more than 12 GHz
and sharp upper cutoff frequency due to the proper location of two
transmission zeros. VC 2013 Wiley Periodicals, Inc. Microwave Opt
Technol Lett 55:1640–1644, 2013; View this article online at
wileyonlinelibrary.com. DOI 10.1002/mop.27637
Key words: broadband bandpass filter; parallel-coupled microstrip
line; microstrip filter
1. INTRODUCTION
Compact broadband filters which are compatible with printed
circuit boards are highly demanded in most of the modern com-
munication systems. The filter size is usually constrained by the
number of resonators and size of the resonator structures used in
the design, whereas the filter bandwidth is mainly limited by the
achievable maximum coupling between its resonators. Various
compact resonator structures were introduced in literature [1–4].
Parallel-coupled microstrip line (PCML) structure has been used
as a coupling component in the design of bandpass filters [5, 6].
To achieve a broadband bandpass filter, a high-coupling PCML
structure constructed from narrow width parallel microstrip lines
with narrow gap in-between. Various broadband and ultrawide-
band (UWB) bandpass filters using PCML structure were
reported in literature [7–11].
A ground plane aperture technique for PCML structure was
proposed and developed to enhance the tight coupling over a
certain frequency range [7]. Multipole broadband microstrip
bandpass filter was realized by attaching a single-line high-im-
pedance resonator of uniform line section between two PCML
sections with backside aperture. The overall proposed design
required a ground plane aperture and a pair of capacitive open-
ended stubs. On the basis of impedance steps and PCML as
Figure 5 The measured results compared with simulated results for
the proposed power divider from 1 to 8 GHz
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1640 MICROWAVE AND OPTICAL TECHNOLOGY LETTERS / Vol. 55, No. 7, July 2013 DOI 10.1002/mop
inverter circuits, various designs of broadband bandpass filters
were presented in Ref. 8. The proposed design uses suspended
stripline of PCML structure to reduce the spurious response and
enhance the coupling factor. A novel microstrip-line UWB
bandpass filter with compact size was proposed in Ref. 9 by
forming a multiple-mode resonator and introducing quarter-
wavelength PCML in the input and output ports.
It has been demonstrated that a feeding network with low-
characteristic impedance is able to improve both the coupling
factor and operating bandwidth of PCML structure [10]. Similar
to the proposed filter in Ref. 7, a broadband PCML structure
was designed in Ref. 10 without having a backside aperture and
a pair of capacitive open-ended stubs. Based on the structure in
Ref. 10, a compact UWB bandpass filter with four resonant
modes was proposed in Ref. 11. The proposed filter was based
Figure 1 (a) Circuit model of the initial proposed design. (b) Layout
of the initial proposed design
Figure 2 Full-wave simulated response of the design for various val-
ues of Scle based on Figure 1(b). (a) S11 and (b) S21. [Color figure
can be viewed in the online issue, which is available at
wileyonlinelibrary.com]
Figure 3 (a) Circuit model of the proposed filter with a pair of L-
shaped parallel open stub. (b) Layout of the proposed filter
Figure 4 Full-wave simulated response of the design with parallel
open stub for various values of Los with Wos ¼ 2.2 mm. (a) S11 and (b)
S21. [Color figure can be viewed in the online issue, which is available
at wileyonlinelibrary.com]
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DOI 10.1002/mop MICROWAVE AND OPTICAL TECHNOLOGY LETTERS / Vol. 55, No. 7, July 2013 1641
on a PCML structure with L-shaped low impedance feeding net-
work and C-shaped low impedance middle resonators.
In this article, a compact broadband PCML structure similar
to Refs. 10 and 11 is designed. The proposed design uses a sin-
gle-line low impedance resonator of specific length and width
with a pair of cross-coupled L-shaped open-ended stubs attached
between the two PCML sections. Moreover, a low impedance
feeding network is introduced at the end of the structure. The
cross-coupled L-shaped open-ended stubs at the middle resona-
tor are used to improve the performance of the filter. It is also
used to improve the upper cutoff frequency based on creating
the transmission zero of the design in the required position; a
property that was not realized in Refs. 10 and 11. The position
of the PCML feeding at the middle resonator embedded with
open-ended stub forms quarter-wavelength open-ended stubs.
Those stubs produce a standing wave at a certain frequency to
initiate a transmission zero. In the higher stopband, the proposed
filter achieves a sharp cutoff response due to the transmission
zero of the proposed resonators. That response is based on the
length of the open-ended stubs and the cross-coupling between
the stubs. The structure of the filter is optimized using an ADS
momentum. The design is accomplished using the substrate
Rogers RT6006 with dielectric constant of 6.15 and thickness of
1.27 mm. The filter is then fabricated and tested to validate the
proposed method.
2. FILTER DESIGN
The initial design of the filter is based on the structure depicted
in Figure 1. In this case, a simple PCML broadband bandpass
filter is designed using quarter wavelength (k/4) resonators. The
initial filter design based on Ref. 10 uses a rectangular middle
resonator with Wrmr ¼ 2.6 mm (Zo2 ¼ 41 X) and Lrmr ¼ 7 mm
(�k/4 at 4.85 GHz). In addition to that, it uses a pair of tight
PCML structure with Lcl ¼ 7.3 mm (�k/4 at 4.85 GHz), Wcl ¼
0.4 mm, and Scl ¼ 0.2 mm with odd impedance Zoo ¼ 51.5 X
and even impedance Zoe ¼ 137.5 X. The structure is connected
to the middle resonator at Lp ¼ 0.8 mm with feeding network
Lfn ¼ 3.5 mm and Wfn ¼ 2 mm (Zo1 ¼ 48 X). A cross-coupling
capacitor C1, as shown in Figure 1(a), is then introduced
between the PCML structure and the middle resonator. The ca-
pacitor is added by creating a gap of Scle between one of the
strips of the PCML structure, which is connected to the feeding
network and the middle resonator. This capacitance is able to
produce multiple transmission zeros within the design. The
design based on Figure 1(b) with the above configuration is
simulated using ADS momentum full-wave simulator. The simu-
lation runs using the substrate Rogers RT6006 with dielectric
constant of 6.15 and thickness of 1.27 mm for various Scle.
Figure 2 shows the simulated transmission coefficient S21
and reflection coefficient S11 for the proposed design for various
Scle based on Figure 1(b). The simulated results for S11 show
multiple resonances at various frequencies. The first two
resonances f1 � 3.0 and f2 � 4.5 GHz can be considered as the
required band for the design while the higher resonances (fh1
and fh) can be classified as higher harmonics. The simulated
results for Ss1 show transmission zeros at �9.9 and �11.0 GHz.
When Scle ¼ 2.0 mm, the transmission coefficient is S21 � �1.9
dB and reflection coefficient S11 � �5.0 dB with operating band
from 2.7 to 5.5 GHz. When Scle ¼ 1.0 mm, the transmission
coefficient is S21 � �0.9 dB and reflection coefficient S11 �
�7.0 dB with operating band from 2.92 to 6.2 GHz. For the two
cases Scle ¼ 2.0 mm and Scle ¼ 1.0 mm, as Scle/Wcl
1, the
effect of the capacitive cross-coupling C1 is negligible. The
design shows weak coupling of the PCML structure which leads
TABLE 1 The Summary of the Design Based on Figure 4 for Various Stub Lengths
Los (mm) Cos (pF) Resonant Frequencies (f1 and f2) Harmonic Frequency (fh) Transmission Zero Further Harmonics
0 0.0 3.50 GHz, 5.76 GHz 9.35 GHz 9.52 GHz, 11.0 GHz No
1 0.186 3.52 GHz, 4.70 GHz 8.70 GHz 9.18 GHz, 11.24 GHz No
2 0.397 3.55 GHz, 4.44 GHz 7.85 GHz 8.73 GHz No
3 0.679 3.54 GHz, 4.23 GHz 6.90 GHz No 9.65 GHz, 11.30 GHz
4 1.140 3.53 GHz, 4.12 GHz 5.84 GHz No 8.55 GHz, 10.70 GHz
TABLE 2 Summary of the Design Based on Figure 5 for Various Extended Stub Length Lf and Gap Sg
Capacitance Due to Sg
Lf (mm)
Capacitance of (LosþLf)
Stub Cosf, (pF) Sg (mm) Cp (pF) [6] Cg (pF) [6] Sg/Wf
0.0 0.0 2.6 0 0 >>1
0.8 0.908 1.0 35.35 24.47 0.625
1.2 1.09 0.2 8.56 76.56 0.125
Figure 5 Full-wave simulated response of the design with parallel
open stub with extended length to form capacitive coupling for various
values of Lf with Wf ¼ 1.6 mm. [Color figure can be viewed in the
online issue, which is available at wileyonlinelibrary.com]
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1642 MICROWAVE AND OPTICAL TECHNOLOGY LETTERS / Vol. 55, No. 7, July 2013 DOI 10.1002/mop
to poor passband and stopband performances with poor upper
cut-off frequency.
On the other hand, when Scle ¼ 0.2 mm (Scle/Wcl
1), the
design shows a good passband and stopband performance with
transmission coefficient S21 � �0.5 dB and reflection coefficient
S11 � �11 dB with operating band from 3.0 to 6.6 GHz. It also
shows a sharp upper cut-off frequency with resonance frequen-
cies at f1 ¼ 3.5 GHz, f2 ¼ 5.76 GHz, and harmonic frequency
at fh1 ¼ 9.35 GHz. The design shows excellent capacitive cross-
coupling effects C1 and strong coupling on the PCML structure
which adds transmission zero at 9.52 and 11.0 GHz.
The circuit modal and the layout of the new proposed design
are shown in Figure 3. The design is developed from the origi-
nal structure in three steps. First, the design is improved by
placing a parallel open stub (Z03) of width Wos and length Los at
both ends of the middle resonator as shown in Figure 3. The
parallel open stub is designed by using width Wos ¼ 2.2 mm
(Z03 ¼ 45.5 X) and length Los < kg/4. Because Los < kg/4, the
input admittance of the stub is capacitive. Based on above con-
figuration, the design was simulated using ADS. Figure 4 shows
the transmission coefficient and reflection coefficient of the
design for various lengths Los of the parallel open stubs.
Table 1 shows the equivalent capacitance Cos [5] for the var-
ious stub length Los at 4.85 GHz. It shows that as the stub
length increases the equivalent capacitance Cos increases and the
resonance frequencies within the operating band and the har-
monic frequencies moves toward lower values. The first har-
monic frequency is initially at 9.35 GHz for Los ¼ 0 mm and
moves toward the operating band with increasing Los. When Los
¼ 4 mm, that frequency moves to 5.84 GHz and becomes part
of the operating band that has effectively three resonant frequen-
cies. As the stub length increases, no significant transmission
zero presents and multiple harmonics appear that affect the filter
performance in the stopband significantly.
Based on Table 1 and ADS optimization, the optimum stub
length required to produce a transmission zero is Los ¼ 2.9 mm.
The equivalent capacitance of the stub is Cos ¼ 0.645 pF at
4.85 GHz. This stub is used as a parallel open stub at both ends
of the middle resonator to design a broadband bandpass filter.
The transmission coefficient of S21 � �4.1 dB and reflection
coefficient of S11 � �2.4 dB are achieved throughout the oper-
ating band 3.1–7.1 GHz with sharp upper cut-off frequency. The
design has three resonant frequencies at 3.6, 4.2, 7.0 GHz, and a
transmission zero at 8.4 GHz.
The design is further improved by placing an extended stub
of high impedance Zo4 ¼ 54.5 X with a width of Wf ¼ 1.6 mm
and a length of Lf as shown in Figure 3. The added stub form a
capacitive cross-coupling Cg between the edge of both stubs and
a shunt capacitance Cp as listed in Table 2. The design is simu-
lated for various configurations of Lf and Sg. Figure 5 shows the
insertion and reflection coefficient of the filter without extended
stub and with extended stub of length Lf ¼ 0.8 and 1.2 mm. For
Lf ¼ 0.8 mm with a gap between the two edge of open stubs Sg
¼ 1.0 mm, the transmission coefficient is S21 � �1.6 dB, and
the reflection coefficient is S11 � �5.7 dB throughout a pass-
band of 3.1–6.7 GHz with a sharp upper cut-off frequency. The
filter has three resonant frequencies at 3.56, 4.16, 6.59 GHz, and
a transmission zero at 8.16 GHz.
By extending the stub length to Lf ¼ 1.2 mm with Sg ¼ 0.2
mm, the cross-coupling capacitance becomes Cg ¼ 76.56 pF.
This value is very high compared to Cosf ¼ 1.09 pF (Table 1)
and Cp ¼ 8.56 pF. The high capacitance value improves the
overall performance of the filter in the passband and stopband
with sharp upper cut-off frequency with excellent transmission
zero. The design with the above specifications has excellent
transmission coefficient S21 � �0.3 dB and reflection coefficient
S11 � �13.7 dB throughout the passband from 3.1 to 6.3 GHz.
It has three resonant frequencies at 3.5, 4.2, 5.96 GHz, and a
transmission zero at 7.3 GHz with S21¼�50 dB. The filter
Figure 7 Photograph of the fabricated filter. [Color figure can be
viewed in the online issue, which is available at wileyonlinelibrary.com]
TABLE 3 The Summary of the Optimized Design Parameters
Based on Figure 3(b)
Parameter Value (mm)
Wrmr 2.6 (Zo2¼ 41 X)
Lrmr 7.0 (�k/4 at 4.85 GHz)
LOS 2.9
WOS 2.2 (Zo3¼ 45.5 X)
Lf 1.2
Wf 1.6 (Zo4¼ 54.5 X)
Sg 0.2
Lcl 7.3 (�k/4 at 4.85 GHz)
Wcl 0.4
Scl 0.2
Scle 0.2
Lp 2.8
Lfn 3.5
Wfn 2.0 (Zo1¼ 48 X)
Figure 6 Full-wave simulated response of the proposed design for
various values of Lp. [Color figure can be viewed in the online issue,
which is available at wileyonlinelibrary.com]
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DOI 10.1002/mop MICROWAVE AND OPTICAL TECHNOLOGY LETTERS / Vol. 55, No. 7, July 2013 1643
shows excellent broad stopband from 6.3 to 12.6 GHz with S21
� �25 dB as shown in Figure 5.
The design is further improved by varying the position Lp of
the PCML structure on the middle resonator. Figure 6 shows the
transmission coefficient and reflection coefficient of the filter for
different values of Lp. As the Lp increases from its original
value 0.8 to 2.8 mm, the passband bandwidth increases with
highly sharper upper cut-off frequency and excellent transmis-
sion zero. The transmission zero is effectively shifted to higher
frequency which leads to increase in the bandwidth. That shift
in the transmission zero is due to the decrease in the effective
length of the distance between the open-ended stubs and the
feeding PCML. In the case of Lp ¼ 0.8 mm, the transmission
zero is at 7.1 GHz because the overall length of the open-ended
stubs is quarter wavelength at 7.1 GHz. Similarly when Lp ¼
2.8 mm, the transmission zero is at 8.1 GHz as the overall
length of the open-ended stubs is quarter wavelength at 8.1GHz.
The design is then optimized by placing a notch at both inner
corners of the middle resonator to reduce the losses due to sharp
edges at 4.85 GHz. The added notches, as shown in Figure 3(b),
improve the performance of the passband for both the transmis-
sion coefficient and the reflection coefficient as shown in Figure
6. The optimized filter has a broad bandwidth more than 4 GHz
centered at 4.85 GHz. The optimized design shows excellent
passband and stopband performance of transmission coefficient
and reflection coefficient with a sharp transmission zero at 8.0
GHz with S21 ¼ �63.44 dB as shown in Figure 6.
3. EXPERIMENTAL VERIFICATION
Based on the above simulations, the dimensions of the filter with
the best performance are determined as shown in Table 3. The
simulated results of the transmission coefficie