Table of Contents Author Guidelines Submit a Manuscript
International Journal of Antennas and Propagation
Volume 2013, Article ID 349817, 10 pages
http://dx.doi.org/10.1155/2013/349817
Research Article

Circularly Polarized Low-Profile Antenna for Radiating Parallel to Ground Plane for RFID Reader Applications

1Faculty of Engineering, King Mongkut’s Institute of Technology Ladkrabang, Chalongkrung Road, Ladkrabang, Bangkok 10520, Thailand
2Graduate School of Science and Technology, Kumamoto University, 2-39-1 Kurokami, Chuo-ku, Kumamoto 860-8555, Japan

Received 4 September 2013; Revised 4 October 2013; Accepted 5 October 2013

Academic Editor: Z. N. Chen

Copyright © 2013 Kittima Lertsakwimarn 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

This paper presents a low-profile printed antenna with double U-shaped arms radiating circular polarization for the UHF RFID readers. The proposed antenna consists of double U-shaped strip structures and a capacitive feeding line to generate circular polarization. A part of the U-shaped arms is bent by 90° to direct the main beam parallel to the ground plane. From the results, 10 dB and 3 dB axial ratio of the antenna cover a typical UHF RFID band from 920 MHz to 925 MHz. The bidirectional beam is obtained with the maximum gain of 1.8 dBic in the parallel direction to the ground plane at the 925 MHz. The overall size of the proposed antenna including ground plane is 107 mm × 57 mm × 12.8 mm (0.33 × 0.17 × 0.04 ).

1. Introduction

Radio frequency identification (RFID) systems in the ultra-high-frequency (UHF) band are getting a standard in widely used for many applications such as supply chain management, logistics, and tracking [1]. Different frequency ranges for the UHF RFID band have been allocated depending on countries and regions such as 865–868 MHz in Europe, 902–928 MHz in North and South Americas, 950–956 MHz in Japan, and 920–925 MHz in some Asian countries. Many linearly polarized reader antennas have been designed with small size and sufficient bandwidth and used for RFID systems; however, a problem of missing tag detection may take place due to a polarization mismatch. For avoiding this problem, the use of antennas radiating circular polarization (CP) can be a good option [2, 3].

On the other hand, portable RFID readers in addition to fixed type of readers have been actively used in recent years. Considering this situation, antennas for handheld RFID readers have been required to have a low-profile and a small size structure with light weight [49]. In fact, since 5-6 years ago, wearable RFID readers on a hand have appeared on the fields of health care and inspection services, so that they can use their both hands at their working places freely without holding their reader. For achieving such situation, a low-profile CP reader antenna is required for wearable devices with a compact design, and directing its main beam parallel to the ground plane can make the maximum use of the advantages of the low-profile design [10].

Recently, low-profile and small CP antennas have still received a lot of research attention, although other types of UHF RFID reader antennas with meandered, microstrip, and helical element have been published in the literature [49]. In [4], an antenna with four meandered monopole elements fed by a series feeding network has been reported, and another antenna with arrayed two bent elements is presented in [5]. In [6], double-sided, crossed-dipole antenna for CP radiation loaded with two metal strips for phase delay is published. A compact circularly polarized microstrip antenna has been presented in [7]. Furthermore, some microstrip antennas for typical commercial handheld readers are linearly or circularly polarized. However, such antennas based on microstrip antennas limit the size and the bandwidth, and the main beam of those is directed to the normal direction to the ground [8]. Some study groups have reported horizontally polarized printed loop antennas in [11, 12], and some groups have studied on open-loop antennas generating CP [13, 14]. Moreover, an inverted-L CP antenna and a slender CP antenna have been reported in [15, 16], respectively. However, the main beam direction is not parallel to the ground, and the bandwidth is not sufficient. A study group involving one of the authors has recently reported a low-profile antenna with high radiation efficiency in [17, 18], but the polarization is linear. For now, as far as the authors know, almost no one has reported on circularly polarized and low-profile antennas radiating parallel to the ground plane.

In this paper, a compact and low-profile antenna for radiating CP parallel to the ground plane is proposed for RFID readers at UHF band (from 920 MHz to 925 MHz). In Section 2, the antenna design and characteristics of the proposed antennas are discussed. The principle to generate CP in this antenna is also discussed in Section 3. In Section 4, the design process is presented. Finally, the discussions in this paper are concluded in Section 5.

2. Antenna Design

In this section, the antenna design is presented. The antenna is designed using the CST MW Studio [19]. Figure 1 shows the proposed antenna structure consisting of double U-shaped strips and a capacitive feeding structure of both sides of Arlon Diclad522 ( = 2.6) with a thickness of h = 0.8 mm. The dimension is L = 87 mm (0.27 )   W = 37 mm (0.11 ) in length and width. The air gap between radiating element and ground plane is chosen as 11.8 mm (0.036 ) as shown in Figure 1(b). The length and width of double U-shape are optimized because these dimensions affect the resonance frequency at which the length of U-shape is /4 as shown in Figure 1(c). One of the arms of the U-shape (bent element) is bent by 90° in the x-y plane from the radiating element. This forms a U-shaped slot with the ground plane on the bent element in the z-x plane. Figure 1(d) shows the capacitive feeding structure which is installed underneath the radiator (double U-shaped elements) and includes an L-shaped stub and an F-shaped stub with a capacitive gap for matching. A photograph of the fabricated antenna is shown in Figure 1(e). The ground plane size is chosen so as to minimize the axial ratio (AR) in the y-direction and not to allow the leakage current on the coaxial cable. The ground plane size is extended in the +x- and −y-directions with the same size by g = 20 mm, respectively from the substrate dimension. This effect will be discussed in Section 4.

fig1
Figure 1: Geometry of the proposed antenna. (a) Perspective view, (b) side view, (c) radiating element, (d) feeding element, and (e) photograph of the fabricated antenna.

The double U-shaped radiator determines the resonant frequency. Considering the principle to generate CP discussed later, the structure should have a half-cut structure of the split-ring resonator antenna [20] with the same resonant frequency as shown in Figure 2. For making a low-profile structure on the ground plane, the feeding structure shown in Figure 1(d) should be used so as to keep sufficient impedance characteristics as discussed later. Furthermore, a part of the arms should be bent by 90° in the x-y plane, so that the main beam can be directed in the y-direction. Table 1 shows the optimized structural parameters of the proposed antenna.

tab1
Table 1: The optimized structural parameters.
349817.fig.002
Figure 2: The antenna evolution.

Figure 3 shows simulated and measured characteristics. The simulated and measured bandwidth at −10 dB are found from 916 MHz to 934 MHz (1.8%) and 916 MHz to 930 MHz (1.4%), respectively, covering a typical UHF RFID band (920 to 925 MHz; Thailand). The simulated and measured radiation patterns of left-hand CP (LHCP) and right-hand CP (RHCP) at 925 MHz are shown in Figure 4 in x-y plane and y-z plane. The simulated and measured half-power beamwidth (HPBW) of RHCP are 105° and 110°, respectively, in y-z plane where the main beam (RHCP) direction is declined only by 20° from the y-direction (parallel to the ground plane). However, the obtained gain in the y-direction is slightly lower by only 0.6 dB than that in the main beam direction. The simulated and measured gains are 1.8 dBic and 2.8 dBic, respectively, in y-direction. The radiation patterns of RHCP and LHCP have been normalized by the simulated and measured peak gain of RHCP (copolarization), respectively. Therefore, we can understand that, in the y-direction, the cross-polarization of LHCP is more than 15 dB lower than RHCP. This indicates that the AR in the y-direction is less than 3 dB. Furthermore, considering the discussion below, it can be said that the measured results in the radiation patterns show reasonable agreements with the simulated results. As shown in Figure 5(a), the AR in y-z plane is less than 3 dB in the θ angle range from 70° to 95° and 70° to 90° for simulated and measured results, respectively. In the boresight direction at θ = 90°, the measured AR is higher by approximately 1 dB than the simulated AR, although the measured AR is at around 3 dB. Considering the results of radiation performances discussed above with Figures 4 and 5, we can find small differences between the simulated and measured results, although they show reasonable agreements. The small differences are mainly due to fabrication errors, especially those are related to our hand-made fabrications of U-shaped slot. As shown in Figure 5(b), the 3 dB AR in the y-direction can also be observed in the UHF band. As a result, we can understand that the proposed antenna can radiate CP in the y-direction covering the UHF RFID band.

349817.fig.003
Figure 3: Simulated and measured .
fig4
Figure 4: Radiation patterns at 925 MHz. (a) x-y plane and (b) y-z plane.
fig5
Figure 5: Simulated and measured AR pattern of the proposed antenna in y-z plane ( = 90°) at 925 MHz (a) as a function of θ and (b) as a function of the frequency at θ = 90°.

3. Principle of Generating Circular Polarization

The generation mechanism of CP is discussed in this section. The antenna elements have two metallic layers sandwiching the dielectric substrate to equip the radiator and the feeding structure with the L-shaped and F-shaped stubs. The radiator and the feeding structure have been overlapped as shown in Figure 1(c). The e-field (electric field) distributions at different phases are shown in Figure 6. At phase = 0°, the strongest field of Z-component is found mainly around the U-shaped slot on the bent element as shown in Figure 6(a). As shown in Figure 6(b), e-field directed to +z with high density can be found; however, the e-field to −z shows low density. This asymmetrical distribution is due to the difference in the presence of the radiator and ground plane. At phase = 90°, strong field directed in x- and z- directions can be found on the U-shaped slot as shown in Figure 6(c); however, the components in z directions finally are canceled out by each other in the far field. Since the length between the feeding point (around x = 0 mm) on the feeding line and the bent part of the U-shaped slot is about half wavelength, the voltage at the feeding line gets lower at 90° phase than that at the bent point in the U-shaped slot. Therefore e-field is pulled into the feeding line as shown in Figure 6(d) resulting in having a symmetrical distribution between z-directions. As a result, at phase = 90°, only the X-component at the bent part of the U-shaped slot contributes to radiate. With the same analogy, the e-field generates CP with 90°-phase difference of orthogonal e-field components at phase = 180° and 270°, respectively.

fig6
Figure 6: Electric field distributions in different phases at 920 MHz (a) in the x-z plane at phase = 0°, (b) in the y-z plane at phase = 0°, (c) in the x-z plane at phase = 90°, and (d) in the y-z plane at phase = 90°.

On the other hand, this antenna radiates the same sense of CP, although the 3 dB AR can be obtained at θ = −120°. This radiation is explained by the e-field behavior around the feeding point outside of the radiating element. At phase = 0°, the normal e-field can be observed by the same principle of the U-shaped slot mentioned above. At phase = 90°, the e-field is pulled into the feeding point following the same principle of the above explanation. Therefore, the e-field rotates in the clockwise direction with respect to the −y-direction.

4. Effects of Structural Parameters

The proposed antenna is a low profile and can radiate CP in the y-direction with respect to the ground plane. This section discussed the effects of structural parameters on the AR and antenna gain.

4.1. Effects of the Bent Element

One of interests in this antenna is a fact that CP is radiated in the y-direction with θ = 90°, even though the structure is low profile. Bending a part of U-shaped elements with a bent angle α (from 0° to 90°), as shown in Figure 7, contributes to increase the θ angle of main beam direction in the y-z plane ( = 90°). The input impedance characteristics can be kept the same, as shown in Figure 8(a), in this range of α. When α = 0°, the peak gain can be observed in the z direction at 0° as shown in Figure 8(b). With an increase in α from 30°to 90°, the main beam direction θ is shifted from 0° to 70° in the y-z plane. For α = 90°, the 3 dB AR can be observed at θ = 90° in the y-z plane as shown in Figure 8(c).

349817.fig.007
Figure 7: Direction of bending angle α on the element.
fig8
Figure 8: Simulated results of (a) input impedance characteristics with α, (b) antenna gain pattern, and (c) AR pattern of the proposed antenna in y-z plane at 925 MHz as a function of the bending angle α ( = 90°).
4.2. Effects of L-Shaped and the Capacitive Gap Feeding Structure

Effects of the stubs in the feeding structure are discussed. The use of a coupled feeding line with the radiator element is one of the techniques for designing low-profile antennas [17] to cancel the inductivity at a frequency range with around 50 Ω impedance. Figure 9 shows the evolution of feeding structure that starts from a simple rectangular strip to the proposed structure with adding the capacitive gap, the L-shaped stub on a lower edge of the line, the short stub, the long stub, and the F-shaped stub on an upper edge.

349817.fig.009
Figure 9: Feeding structure evolution.

For matching to 50 Ω with a sufficient bandwidth, the capacitive gap and the L-shaped stub are installed resulting in the shift of the characteristics as shown in Figure 10. With the simple rectangular feeding structure, the input impedance characteristic shows a small kink (with a dotted line) at the right side of the Smith chart centering the horizontal axis. When only the capacitive gap is installed, the kink is shifted to a different place (the kink shown with a dashed line) along the circle of a real axis counterclockwisely. After this, when the L-shaped stub having a parallel capacitance is installed, the kink, shown with a solid line, is magnified passing the center showing a narrow bandwidth since the kink size is still bigger than the circle of VSWR = 2.

349817.fig.0010
Figure 10: Simulated input impedance characteristics when the gap and L-shaped stub are installed.
4.3. Effects of F-Shaped Stub Feeding Structure

As the final step, the F-shaped stub is installed for enhancing the bandwidth. The F-shaped stub is a combination of short and long L-shaped stubs. Figure 11(a) shows the effect of installing the short and long L-shaped stubs on input impedance characteristics. When the short stub is installed, the impedance can be matched well to 50 Ω with a sufficient bandwidth; however, as shown in Figure 11(b), the main beam direction is around 60°. On the other hand, when the long stub is installed, the main beam direction is shifted closer to θ = 90° as shown in Figure 11(b); however, the impedance bandwidth is narrow as shown in Figure 11(a) with a larger kink.

fig11
Figure 11: Simulated results of (a) input impedance characteristics, (b) antenna gain, and (c) AR pattern with θ. = 90° in y-z plane at 925 MHz when the short, long, and F-shaped stubs are installed.

The F-shaped stub has the both functions of the short and long stubs; that is, the short stub is required for matching, and the long stub is for radiating CP in the direction at θ = 90°. Similarly, the F-shaped stub makes a small kink inside the circle of VSWR = 2 in the Smith chart and also makes the main beam direction closer to θ = 90° resulting in 3 dB AR in +y-direction as shown in Figures 11(b) and 11(c). With the metallic arm along the +y-direction of the long or F-shaped stub, the e-field inside the radiator can be perpendicular to the ground plane and the stub element nearby the U-shaped slot. This behavior leads to direct the main beam closer to θ = 90°. As a result, in the final structure, the simulated and measured impedance can be matched to 50 Ω as shown in Figure 11(a) with the simulated bandwidth of 18 MHz, and the main beam direction is at θ = 70° as shown in Figure 4. In the direction at θ = 90°, AR can be kept less than 3 dB with a sufficient simulated gain of 1.8 dBic.

4.4. Effects of Ground Plane Size

Figure 12(a) shows the variation in AR pattern with the ground plane size. Comparing the size (default) which is the same as the radiator in x-y plane, the ground plane is extended by g = 20 mm in +x- and –x-, +x- and –y-, −x- and –y-, and ±x- and y-directions at the same time. When the ground is extended in +x and –y-directions, the AR is minimized at around θ = 90°. This extension in the +x direction contributes to have the e-field, near the open end of radiator, directed in x- or z direction in wider area of x-z plane at phase = 0° or 90°, respectively. In this case, the HPBW is about 105° covering the θ = 90° direction as shown in Figure 12(b).

fig12
Figure 12: Simulated results of (a) AR pattern and (b) antenna gain in y-z plane at 925 MHz as a function of the ground plane size by g = 20 mm (ϕ = 90°).

For the extension in the +x and –y-directions, the main beam direction in which the minimum AR can be obtained gets closer to θ = 90° with an increase in g from 5 to 25 mm as shown in Figure 13(a). For g = 25 mm, the angle for the minimum AR is the closest to θ = 90°; however, the antenna gain at θ = 90° is smaller than that for g = 20 mm as shown in Figure 13(b). Therefore, the parameter g should be chosen as 20 mm for this design. Choosing g = 20 mm with the extension in the +x and –y-directions, we have confirmed that the ground plane size has a sufficient area enough to suppress the leakage current on the coaxial cable.

fig13
Figure 13: Simulated results of (a) AR pattern and (b) antenna gain in y-z plane at 925 MHz as a function of the extension in +x- and −y- direction g ( = 90°).

5. Conclusion

This paper has proposed a low-profile and circularly polarized antenna with double U-shaped arms considering an application for handheld RFID readers at 920 MHz to 925 MHz band. The structure consists of a modified double U-shaped radiator and ground plane. A part of the arms of the radiator has been bent by 90° in the x-y plane for directing CP radiation parallel to the ground plane (θ = 90°). For keeping the sufficient impedance bandwidth for the RFID band, some matching stubs and a capacitive gap have been installed on the feeding structure, and the design process has been discussed. In addition to them, effects of the ground plane size on the CP direction have been discussed, and a sufficient antenna gain has been also confirmed in this direction. The measured results show good agreements with the simulated results. Furthermore, the principle for generating CP has been analyzed taking notice of the e-field distributions. Based on this principle, the U-shaped slot can contribute to achieve a low-profile antenna for radiating CP parallel to the ground.

Acknowledgment

This work is supported by the Thailand Research Fund (TRF) through the Royal Golden Jubilee Ph.D. Program under Grant no. PHD/0324/2552.

References

  1. K. Finkenzeller, RFID Handbook, Wiley, New York, NY, USA, 2nd edition, 2004.
  2. X. Chen, G. Fu, S.-X. Gong, Y.-L. Yan, and W. Zhao, “Circularly polarized stacked annular-ring microstrip antenna with integrated feeding network for UHF RFID readers,” IEEE Antennas and Wireless Propagation Letters, vol. 9, pp. 542–545, 2010. View at Publisher · View at Google Scholar · View at Scopus
  3. W.-G. Lim, W.-I. Son, K.-S. Oh, W.-K. Kim, and J.-W. Yu, “Compact integrated antenna with circulator for UHF RFID system,” IEEE Antennas and Wireless Propagation Letters, vol. 7, pp. 673–675, 2008. View at Publisher · View at Google Scholar · View at Scopus
  4. J.-H. Bang, C. B. Ochir, H.-S. Koh, E.-J. Cha, and B.-C. Ahn, “A small and lightweight antenna for handheld RFID reader applications,” IEEE Antennas and Wireless Propagation Letters, vol. 11, pp. 1076–1079, 2012. View at Publisher · View at Google Scholar
  5. J. J. Yu and S. Lim, “Design of an electrically small, circularly polarized, parasitic array antenna for an active 433.92 MHz RFID handheld reader,” IEEE Transactions on Antennas and Propagation, vol. 60, no. 5, pp. 2549–2554, 2012. View at Google Scholar
  6. Y.-F. Lin, Y.-K. Wang, H.-M. Chen, and Z.-Z. Yang, “Circularly polarized crossed dipole antenna with phase delay lines for RFID handheld reader,” IEEE Transactions on Antennas and Propagation, vol. 60, no. 3, pp. 1221–1227, 2012. View at Publisher · View at Google Scholar · View at Scopus
  7. N. Nasimuddin, Z. N. Chen, and X. Qing, “Asymmetric-circular shaped slotted microstrip antennas for circular polarization and RFID applications,” IEEE Transactions on Antennas and Propagation, vol. 58, no. 12, pp. 3821–3828, 2010. View at Publisher · View at Google Scholar · View at Scopus
  8. P. V. Nikitin and K. V. S. Rao, “Helical antenna for handheld UHF RFID reader,” in Proceedings of the 4th Annual IEEE International Conference on RFID (RFID '10), pp. 166–173, Orlando, Fla, USA, April 2010. View at Publisher · View at Google Scholar · View at Scopus
  9. W.-I. Son, M.-Q. Lee, and J.-W. Yu, “Module integrated antenna with circular polarization for mobile UHF RFID reader,” IEEE Transactions on Microwave Theory and Techniques, vol. 59, no. 4, pp. 1157–1165, 2011. View at Publisher · View at Google Scholar · View at Scopus
  10. S.-H. Chang and W.-J. Liao, “A novel dual band circularly polarized GNSS antenna for handheld devices,” IEEE Transactions on Antennas and Propagation, vol. 61, no. 2, pp. 555–562, 2013. View at Publisher · View at Google Scholar
  11. K. Wei, Z. Zhang, and Z. Feng, “Design of a wideband horizontally polarized omnidirectional printed loop antenna,” IEEE Antennas and Wireless Propagation Letters, vol. 11, pp. 49–52, 2012. View at Publisher · View at Google Scholar · View at Scopus
  12. C. C. Lin, L. C. Kuo, and H. R. Chuang, “A horizontally polarized omnidirectional printed antenna for WLAN applications,” IEEE Transactions on Antennas and Propagation, vol. 54, no. 11, pp. 3551–3556, 2006. View at Publisher · View at Google Scholar · View at Scopus
  13. R.-L. Li, V. F. Fusco, and H. Nakano, “Circularly polarized open-loop antenna,” IEEE Transactions on Antennas and Propagation, vol. 51, no. 9, pp. 2475–2477, 2003. View at Publisher · View at Google Scholar · View at Scopus
  14. R. Li, G. DeJean, J. Laskar, and M. M. Tentzeris, “Investigation of circularly polarized loop antennas with a parasitic element for bandwidth enhancement,” IEEE Transactions on Antennas and Propagation, vol. 53, no. 12, pp. 3930–3939, 2005. View at Publisher · View at Google Scholar · View at Scopus
  15. X. Yang, Y. Z. Yin, W. Hu, and S. L. Zuo, “Low-profile, small circularly polarized inverted-L antenna with double-folded arms,” IEEE Antennas and Wireless Propagation Letters, vol. 9, pp. 767–770, 2010. View at Publisher · View at Google Scholar · View at Scopus
  16. Y. Zhang and T. Fukusako, “Design of circularly polarized low-profile and slender antenna with a helical element,” IEEE Antennas and Wireless Propagation Letters, vol. 11, pp. 523–526, 2012. View at Publisher · View at Google Scholar
  17. Y. Saito and T. Fukusako, “Low-profile and electrically small meander-line antenna using a capacitive feed structure,” IEEE Antennas and Wireless Propagation Letters, vol. 11, pp. 1281–1284, 2012. View at Google Scholar
  18. Y. Tanogashira and T. Fukusako, “Directional radiation pattern of surface wave antenna using dogbone structure,” IEICE Communication Express, vol. 1, no. 2, pp. 85–88, 2012. View at Publisher · View at Google Scholar
  19. CST-Microwave Studio and User's Manual, CST-Microwave Studio, Framingham, Mass, USA, 2006.
  20. K. Lertsakwimarn, R. Suwalak, and C. Phongcharoenpanich, “A compact loop antenna with parasitic split ring for UHF RFID application,” in Progress in Electromagnetics Research Symposium (PIERS '13), pp. 219–222, Taipei, Taiwan, 2013.